INFORMATION TO USERS - University of Toronto T-Space...Table 1.3 Stanadyne injector calibration data...
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AN EXPERIMENTAL STUDY OF PREHEATED LIQUID FUEL INJECTION IN A PORT INJECTED ENGINE
Michael B. Hebbes
A thesis submitted in conformity with the requirements for the degree of Master of Applied Science
Graduate Department of Mechanical and Industrial Engineering University of Toronto
@Copyright by Michael B. Hebbes, 1998.
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Abstract
An experimentai investigation was perfcrmed in order to determine the effects of
pre-heating liquid fuel during injection in a multi-port hie1 injected engine configuration.
Iso-octane, a pure research grade hiel. has been injected through a modified fuel injector
at upstream temperatures ranging from 20°C to 220°C. An increase in fuel spray cone
angle and the amount of fuel atomization was observed to occur with increasing fuel
preheats. A rapid transition was observed in measured cone angle at a reduced
temperature of 0.73.
Acknowledgements
1 would like to thank Professor McCahan and Professor Wallace for keeping me
on track and providinp helpful advice over the past two years. 1 would like to thank
Richard Ancimer and Eric Brombacher for a great deal of help during the experimental
setup phase of the thesis. A special thanks to Hannu Jaaskelainen and Paul Salanki for
crucial advice, without which, this research would not have been possible. Finally, I
would like to thank my parents for their support throrighout my studies.
Table of Contents
Abstract
Acknowledgements
Table of Contents
List of Tables
List of Figures
List of Appendices xi
. . . Nomenclature xlll
1. Introduction 1
1 . l . Overview of the Problem ... ..... . ............... . .. . ............... ............ .... 1
1 2. Thesis Organization ... . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . .. 3
2. Theory 5
2.1. Thermodynamics.. . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . ..5
2.2. Intake Port Phenomena.. . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 1 2
22.1. Fuel Transport Phenomena.. . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . ... 13
2.3. Hydrocarbon Emissions.. . . . . . .. . . . ... .... ... . . - . . . .. . . . .. . . . . . . .. . . . . . 16
3. Previous Work 18
3.1. History of Fuel Metering Systems ... . .. . .. . . . . . . . . . . . . .. . . . . . . . . .. . . . . . . . . . . . . . . . 18
3.2. Previous Research.. . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . - 19
. . 3.2.1. Fuel Vaponzing Systems.. . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . .. . . . 19
3.2.2. Heat Transfer. . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . .. - 2 1
3.3.6. Fuel Sprays.. . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . .. 22
4 . Preliminary Experimental Work
........................................................... 4.1. Experimental Apparatus -26
....................................................................... 4.2. Data Acquisition 27
............................................................ 4.3. Experimental Procedure 28
............................................................ 4.4. Results and Conclusions 29
5 . Experimental Apparatus and Equipment 33
.............................................................. 5.1. Engine Specifications -33
........................................................................ 5.2. Nitrogen Flow 34
......................................................................... 5.3. Fuel Injectors 35
............................................. 5.4. Fuel Delivery and Measurïng System 37
................................................ 5.5. Ford Injector Fuel Supply System 40
......................................... 5.6. Stanadyne Injector Fuel Supply System -42
................................................................ 5.7. Fuel Heating System 44
.............................................................. 5.8. Exhaust Management -47
......................................................... 5.9. Data Acquisition Hardware 48
............................................................................... 5.10. Sensors 50
........................................................ 5.1 1 . Data Acquisition Software 54
........................................................ 5.12. Data Acquisition Triggers -55
..................................................................... 5.1 3 . Optical Access - 5 5
.......................................................... 5.14. Photographie Equipment 56
6 . Experimental Procedures 58
.............................................................. 6.1. Cali bration Procedures 58
........................................ 6.1.1. Stanadyne Fuel Injector Calibration 58
........................................................... 6.2. Experimental Procedure -60
....................................... 6.2.1. Ford Fuel Injector Expenmentation -61
62 .2 . Stanadyne Fuel Inject~
7 . Results and Discussion
................ 7.1. Overview
................................ Experimentation -62
64
..................................................... 64
................................................... 7.2. Ford Injector Experïmental Data 66
............................................ 7.3. S tanadyne Injector Experimental Data 66
....................................... 7.4. Examining Experimental Test Conditions -68
............................................. 7.4.1. Fuel-to-Air Equivalence Ratios 69
............................................... 7.4.2. Nitrogen Volumetric Flowrate 71
........................................ 7.4.3. Examining Fuel Injection Pressures -72
.......... 7.4.4. Stanadyne Injector Fuei Deiivery at Elevated Temperatures 74
........... 7.4.5. Exarnining Manifold Pressure and Secondary Temperatures 76
................................................. 7.5. Examining the Acquired Images -78
.......................................................... 7.6. Liquid to Liquid Injections 87
7.7. Preheated Fuel Flow through the Stanadyne Injector ........................... 58
8 . Conclusions and Recomrnendations 94
Refèrences 96
Appendices 99
List of Tables
.................................................. Table 5.1 Engine component dimensions 34
.......................................... Table 5.2 Data acquisition channel information 49
............................................... Table 5.3 Sensor locations and noise levels 50
......................................... Table 7.1 Mean data corresponding to figure 7.6 82
....................................................... . Table A 1 Listing of fuel properties -99
................................................................... Table D . 1 Calibration data I l l
....................................................... Table D.2 Calibration summary data 112
.......... Table H . 1 Temperatures and corresponding Jakob numbers for iso-octane 123
............................................. Table 1.1 Stanadyne injector calibration data 127
............................................. Table L2 Stanadyne injector calibration data 127
............................................. Table 1.3 Stanadyne injector calibration data 128
............................................. Table 1.4 Stanadyne injector calibntion data 128
............................................. Table 1.5 Stanadyne injector calibration data 129
........................... Table J . 1 Ford injector bottom view-port experimental data 130
................................ Table J.2 Ford injector top view-port experimental data 131
.......................................... Table J.3 Stanadyne injector experimental data 132
.......................................... Table 5.4 Stanadyne injector experimental data 133
.......................................... Table J.5 Stanadyne injector experimental data 134
.......................................... Table J.6 Stanadyne injector experimental data 134
.......................................... Table 5.7 Stanadyne injector experimental data 135
.......................................... Table J.8 S tanadyne injector experimental data 136
vii
.......................................... Table J.9 Stanadyne injector experimental data 136
......................................... Table J . 1 O Stanadyne injector experimental data 137
........................................ Table J . 1 1 Stanadyne injector experimental data 137
Table 5.12 Stanadyne injector experimental pressure data . Matching pressure data for ........................................................... the data listed in tables 5.3 to J . 1 1 138
List of Figures
Figure 2 .1 Pressure vs . specific volume for iso-octane .................................. 6
Figure 2.2 Pressure vs . enthalpy for iso-octane ........................................... 8
Figure 2.3 Possible fuel travel paths into the cylinder ................................... 13
Figure 3.4 Liquid fuel evolution through intake system ................................. 14
Figure 4.1 Apparatus schematic diagram .................................................. 27
Figure 4.2 Injections of iso-octane through the converging nozzle at 3.77bar and increasing upstream teniperatures: a) 30°C (0.56Tc) and b) 1 60°C (O.SOT,-). ........ 31
Figure 4.3 Injections of iso-octane through the converging nozzle at 10.00bar and ....... increasing upstream temperatures: a) 135°C (0.75 Tc) and b) 2 10°C (0.89Tcj 33
Figure 5.1 Ford Injector fuel supply system ............................................... 40
Figure 5.2 Ford fuel injector setup .......................................................... 42
Figure 5.3 Stanadyne Injector fuel supply system ....................................... .44
Figure 5.4 Heater control system ........................................................... 46
............................................................... Figure 5.5 Condenser system -48
Figure 5.6 Data acquisition signal connections ........................................... 54
Figure 7.1 Fuel line pressure as a function of time ....................................... 68
Figure 7.2 Mass fiowrate as a function of temperature .................... ,.. ........... 76
Figure 7.3 Ford injector fuel injections at room temperature shown frorn: a) the top view port. b) the bottom view-port ..................................................... 80
Figure 7.4 Schematic diagram illustrating a fuel spray capnired in the top view port ............................................................................................... 81
Figure 7.5 Schematic diagram illustrating a fuel spray captured in the bottom view .................................................... port .. ......................................... 81
Figure 7.6 Fuel injection through the Stanadyne injector shown from the bottomview port location at increasing upstream . temperature: a) 25OC (0.55 Tc). b) 80°C (0.65
Tc). c ) 135°C (0.73 Tc). d) 142OC (0.76 Tc). e) 173.g°C (0.8 1 Tc) and f) 306.9OC (0.88 Tc) ................................................................................................ 83
Figure 7.7 Schematic diagram illustratinp a fuel spray captured in the bottorn view port ............................................................................................... 86
Figure 7.8 Cone angle as a function of reduced temperature . + Iso-octane fuel injection data through the Stanadyne injecotor . O Iso-octane fuel injection data from the prelirninary experiments . SIoss dodecane fuel injection data .............................................................................................. - 9 1
Figure B . 1 Ford fuel injector calibration program front panel .......................... 100
Figure B.2 Ford fuel injector calibration program back panel.. ........ .. ............. IO1
Figure B.3 Stanadyne fuel injector calibration program front panel ................... 102
Figure B.4 Stanadyne fuel injector calibration program bclck panel ................... 102
Figure B.5 Fuel line pressure front panel ................................................. 102
Figure B.6 Fuel line pressure back panel .................................................. 103
Figure B.7 Experimental data acquisition front panel ................................... 104
Figure C . 1 Stanadyne injector modification ............................................... 107
Figure D . 1 Characteristic injector Flow curve ............................................ - 1 10
Figure E . 1 Nitrogen flowrate vs . voltage .................................................. 114
Figure E.2 Schaevitz tranducer pressure vs . voltage ..................................... 117
List of Appendices
A. Fuel Data 99
B. LabView Virtual Instruments 100
B. 1. Ford Fuel Injector Calibration Program ... . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . .. 100
B.2. Stanadyne Fuel Injector Calibration Programs ... . . . . . . . . . . . . . . . . . . . . . . . . . . . . . .. 10 1
8.3. Experirnental Data Acquisition Programs ... . . . . . . . . . . . . .. .. . .. . . . . . . .. . . . . . . . ... 103
C. Stanadyne Injector iklodifications 105
D. Ford Fuel Injector Calibration 1 08
D. 1. Ford Fuel Injector Calibration Procedure.. . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . .. 108
D.2. Ford Injector Calibration Data .... . . .. ...... . . . . .. . . .. . .. . . ... . ... . . . . . . . -. . . . . . -.. 1 1 1
E. Transducer Calibration Procedures and Curves 113
F. Data Sheets 118
F. 1. Ford Injector Calibration Sheet ... . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . .. 1 18
F.2. Stanadyne Injector Calibration S heet.. . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 1 19
F.3. Experimental Data Sheet.. . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 1 20
G. Calculations 121
G. 1. Volumetric Flowrate ... . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . - . . . . . . . . . . .. 12 1
G.2. Ford Injector Pulse Width Calculation .... . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . .. 12 1
H. Jakob Number Data 123
1. Stanadyne Injector Calibration Data 127
J . Expenmental Data 130
J . I . Ford Injector Experimental Data ................................................... 130
5.2. Stanadyne Injector Experimental Data ............................................ 132
xii
Ab breviations
cm
D AQ
EOS
EVC
EVO
FIA
FI
HC
IVC
IV0
MPFI
MAP
PTC
P D
SBR
slpm
SSR
TTL
VI
computational fluid dynarnics
data acquisition
equation of state
exhaust valve open
exhaust valve closed
fuel-to-air ratio
fuel injection
h ydrocarbons
intake valve close
intake valve open
muhipoint fuel injection
manifold absolute pressure
positive temperature coefficient
proportional, in tegral, differential
Simonet-Behar-Rauzy
standard liters per minute
solid state relay
transistor-transistor logic
virtual instrument
Symbols
CP liquid specific heat evaluated at the bulk fluid pressure
duty cycle
heat of vaporization evaluated at the bulk fluid pressure
Jakob nurnber
cycle number
critical pressure
system free surface pressure
liquid vapour pressure at a given tempenture
normal boiling temperature
critical temperature
reduced temperature
specific volume
liquid superheat
volumetric et'ficiency
equivalence ratio
liquid surface tension
rotational speed
xiv
1. Introduction
1.1. Overview of the Problem
In a typical gasoline engine, liquid fuel is injected into a relatively low pressure
environment of approximately 1 atm absolute pressure or less. After injection, the fuel
will break up into liquid droplets. The liquid fuel would ideally vaporize and mix with
the airstream into which it is injected. As there is normally not enough energy available
in either the fuel or the air to facilitate complete vaporization, a more realistic picture is
that the liquid fuel impacts on the valve stem and cylinder head wall surfaces and
evaporates. The high temperature impaction surfaces help to vaporize the liquid fuel,
preparing it for the combustion process to follow.
Under a variety of engine operating conditions, it has been found that the injected
fuel undergoes a process quite different from the ideal situation. Specifically, and most
irnportantly, during cold engine start up conditions, the impaction surfaces are not hot
enough to vaporize the liquid fuel Stream. This leads to the formation of a liquid fuel
film on the valve and cylinder head surface. The liquid fuel film can then proceed to flow
into the engine cylinder. Ideally, al1 the fuel entering the cylinder would be in vapor form
for efficient combustion but when liquid fuel is present this leads to problems including
non-homogeneous mixtures and the need for fuel enrichment. In extreme cases, the flame
can pass over the liquid fuel in the cylinder. The film then evaporates into the hot
product gases resulting in the exhaust of raw hydrocarbons (HC). In fact, engine cold
start conditions have been shown to be important in HC emissions production, with
approximately 80 percent of automotive tailpipe HC ernissions in the Federai Test
Procedure occumng in the first five minutes of engine operation [ I l . In recent yenrs a
number of experimental investigations have been carried out in order to study this
phenornenon and these Xe discussed in more detail in the Previous Work chapter of this
document.
The problem of wall wetting or fuel film formation is just now being thoroughly
investigated. To reduce or eliminate wall wetting, we atternpt to take advantage of the
thermodynamic properties of the fuel. Fuel injectors are designed to atomize the fuel
during the injection process. Preheating the liquid fuel prior to injection is anticipated to
superimpose therrnodynarnic vaporization effects ont0 the mechanical atomization
process. Superheating of a liquid, in the context of fuel sprays, occurs when a single-
phase liquid exits the nozzle of an injector at a temperature higher than the saturation
temperature at the bulk liquid pressure. When a liquid is superheated, it enters a non-
equilibrium metastable state, from which some or al1 of the liquid wilI undergo a phase
change to vapour. This is commonly referred to as flashing.
Heated fuel injectors have been utilized in the past as a means of fuel preparation
in direct injection compression ignition engines. In the present research, using a
preheating fuel system in a port injected spark ignition engine is the ultimate intended
goal. In the present study the spray performance was evaluated in an isolated, controlled
research environment using comrnercially available automotive injectors.
1.2. Thesis Organization
This work involves an experimental investigation of preheated liquid fuel
injection. A 1990 Ford Escort 1.9 L, four cylinder, port fuel injected engine was
converted to a single cylinder research engine. Due to the complexities involved with a
fully functional firing engine the investigation was first simplified to a steady state
problern in order to isolate and uncouple the fuel injection process from the effects of any
pulsed intake port flows. The experimental apparatus has been designed and büilt to
cIosely approxirnate a cold engine w m - u p condition at 1000 rpm. Three sets of
experiments were carried out; one using a standard Ford pintle-type injector at ambient
temperatures for base line tests, a second using a modified Stanadyne pencil-type diesel
injector at ambient fuel temperature and a third using the same modified injector at high
fuel temperatures. The primary objective of this study was to obtain photographie images
in order to both characterize the injection event and illustrate the effects of fuel
preheatinp. In addition to image acquisition, the experiments involved acquiring
numerical data in the f o m of injection and intake gas pressures, temperatures and flow
rates in order to fully characterize the injection event.
A detailed discussion including thermodynamics, heat transfer, phase change and
other relevant fuel spray topics are discussed in the Theory chapter of this document. A
summary of the previous work carried out in this field is presented in chapter 3. Section
4 provides a proof of concept obtained from a preliminary set of experirnents. Th3 details
of the expenmental apparatus and experimental procedure are provided in chapter 5 and
6, from which the results of chapter 7 were obtained. A discussion of these results and
the conclusions that can be made are covered in chapters 7 and 8 respectively.
2. Theory
Before dealing with specific examples concerning the developrnent of fuel spray
technology in MPFI engines, a more fundamental discussion dealing with the relevant
thermodynamics of fuel sprays is a necessary first step. Following an explanation of the
fundamentals, characterization of the intake port environment and how the fuel delivery
into this environmznt affects hydrocarbon emissions are discussed.
2.1. Thermodynamics
To understand a preheated liquid spray, a description of the thermodynamics
involved is necessary. A pressure versus specific volume diagram is shown in figure 2.1.
The important features in the diagram are the liquid and vapour saturation boundaries, the
liquid and vapour spinodal lines, the critical point and a metastable isotherm. These lines
are generated using an equation of state (EOS). Liquid and vapour spinodal lines are
essentially the limit of intrïnsic stability and represent the absolute themodynamic limit
of stability for a single-phase fluid. The spinodal curve is composed of the locus of
spinodal limit points and the equation that describes these points takes the following
form:
cntical point
, < saturation boundary \
1 <-- iso thern- \
\ -..
/ Iiauid sr
1 O 1 O 1 O 10 Log volume [rnA3/kg]
Figure S. 1 Pressure versus specific volume for iso-octane.
As shown in figure 2.1, the liquid spinoda1 is constmcted from the metastable isothem
local minima and the vapour spinodal is constmcted from the metastable isotherm local
maxima. The States on a metastable isothem between the liquid spinodal and the vapour
spinodal are non-physical. In this region the fluid can only exist as a two-phase mixture.
A fluid that is fully liquid and exists between the liquid saturation boundary and the
liquid spinodal is in a metastable state and is generaily referred to as a superheated Iiquid.
An important characteristic of a metastable state is that it is a non-equilibrium state. An
ideal equilibrium phase change is considered to be a spontaneous process but in actual
fact some degree of liquid superheating or vapour subcooling will occur before phase
transition. A superheated Iiquid, if pertwbed, will undergo a phase change to a liquid-
vapour mixture or a vapour depending on the conditions [2].
The thermodynarnics of superheated fuel sprays are most readily described with
the aid of a pressure versus enthalpy diagram, as shown in fipure 2.2. Labels included on
the diagrarn are the liquid saturation boundary, the liquid spinodal, the critical point and
two injection events. The liquid saturation boundary was extrapolated up to the critical
point. A thinner line than the computed saturation boundary represents the extrapolation.
The expansion processes during a conventional fuel injection and of a heated injection
have been approximately placed on figure 2.2. The conventional injection process simply
expands the fuel from point 1' to 2', al1 of which occurs in the liquid region. This is often
referred to as a liquid-to-liquid injection.
In a preheated injection, the fuel starts as a subcooled liquid at 1 , expands below
the equilibrium saturation pressure at 2, remains as a superheated Iiquid while expanding
down to approximately point 3 and then liquid and vapor coexist from 3 to 4. The figure
as shown is based on a nearly isobaric phase transition. From position 2 to 3 the liquid is
said to exist in a metastable state. A liquid can exist for a limited time as a superheated
liquid without phase transition depending on the injection conditions. Vapor bubbles wil l
begin to nucleate and expand in size if the time the fluid remains at state 3 is sufficient
and nucleation sites are available. This growth will continue until ail equilibrium vapor
fraction is achieved [3]. Realistically, a critical nuclei must form as the kinetic limit at
state 3 is approached.
2-50 t conventional <- liquid fuel
injection
. 1 critical point
<-- flash boiling fie1 injection
liquid spinodal >
liquid saturation boundary
Figure 2.2 Pressure versus enthaipy for iso-octane.
The degree of superheat is defined in terms of the location of a particular
metastable state between the liquid saturation boundary and spinodal. The maximum
superheat occurs at the liquid spinodal, where the liquid is completely unstable and must
undergo a phase change. The minimum superheat value occurs at the liquid saturation
boundary and is equal to zero at that point. The degree of superheat at a given metastable
state can be described by the Jakob number which is defined as:
In equation 2.2, c, is the liquid specific heat evaluated at the bulk fluid pressure, hl,, is the
heat of vaporization evaluated at the bulk fluid pressure and AT is the superheat.
Superheat is defined as:
TI is the bulk liquid temperature of the metastable liquid and T, is the saturation
temperature at the bulk liquid pressure. The Jakob number is physically described as the
ratio of energy avaiIable for vaporization in a metastable liquid relative to the latent heat
of vaporization of the fhid at a given pressure. A Jakob number equal to or greater than
1.0 indicates that the metastable Iiquid theoretically has enough energy to undergo
complete adiabatic isobaric phase change. A Jakob number of l e s than 1 .O corresponds
to metastable States where the Iiquid contains an inadequate amount of energy to undergo
complete evaporation. In this case the liquid will transition to a liquid/vapuur
equili brium mixture.
Nucleation or vapor formation, which is the onset of the flashing event, does not
necessarily have to occur on the surface of the liquid phase. The transition of a
metastable liquid to a liquid/vapour mixture is initiated by a nucleation event. Nucleation
is the formation of a critical sized vapour bubble in the liquid, which can be initiated by
either a heterogeneous or homogeneous event. Heterogeneous nucleation occurs at low
Ievels of superheat where an interface perturbation acts to initiate the transition from
Iiquid to vapour. Heterogeneous nucleation sites exist at the interface between the
metastable phase and another phase, either liquid or solid. With a sufficient degree of
superheat, and in the absence of heterogeneous nucleation sites, the random rnolecular
fluctuation in the bulk fluid can create a local vapour bubble greater than the critical
nuclei size. This type of bubble formation is known as homogeneous nucleation. Once
homogeneous nucleation is initiated, conversion of liquid to vapour can proceed very
rapidl y.
Brown and York carried out one of the most widely referenced liquid spray
studies in 1962 at the University of Michigan [4]. The study includes a description of the
thermociynamic processes involved in liquid spray analysis and some important
conclusions that can be made with respect to flashinp sprays. Brown and York point out
that this process is comrnon in many applications but has received Little attention as a
topic for research. Brown and York looked at sprays composed of water and Freon- 1 1.
lets were analyzed for drop size, drop velocities and spray patterns. A critical superheat
was found, above which the jet liquid is shattered by rapid bubble growth within the jet
itself. The bubble growth rate was correlated with the Weber number and degree of
superheat of the liquid. Three different spray nozzles with different surface roughness
charactenstics were used to investigate the effect of orifice roughness on jet break-up.
With water it was found that a substantial increase above the saturation temperature was
necessary in order to induce significant shattering. The nozzle with the roughest surface
was able to disintegrate a water jet even when unheated. A sharp-edged orifice delayed
the onset of jet break-up due to the limited liquid-to-nozzle contact surface. Ln the longer
nozzle, without a s h q edged exit, the fuel contacts the nozzle for an extended penod,
which was hypothesized to induce eddies. These eddies produced low pressure regions in
the flow field that Ied to bubble nucleation [43.
Further research into flash boiling of liquid fuel was carried out at General Motors
by R.D. Oza [5] . Oza was able to build on the previous findings presented by Plesset and
Zwick [6]. Plesset and Zwick found that a bubble in a Iiquid with a low degree of
superheat will have a longer idle time and a sIower growth rate than that for a bubble in a
liquid with a high degree of superheat. Idle time is interpreted to mean the time period
before bubble growth occurs. A iiquid with a lower degree of superheat will take ionger
to shatter after emerging from the nozzle [6 ] . Such a liquid jet, with a small degree of
superheat, would not be suited for a practical engine due to the presence of relatively
high-speed intake airfiows. The intake airflow wouid disturb the spray before flashing
could occur and for that reason Oza focused on higher degrees of superheat. Oza used a
speciaily developed injector to deliver propane, indolene and methanol into a constant
volume vessei at a relatively high degree of superheat. Two flash boiling injection
regimes were concluded to exist from the images obtained; the first regime was
characterized as flashing with constant spray cone angle and the second regime was
characterized as flashing with external expansion. The first regirne was attributed to flash
boiling inside the nozzle due to a local pressure drop beIow the fuel saturation pressure
leading to bubble nucleation and a two-phase flow. For the external expansion regirne,
the spray cone angle increased with pressure ratio (ratio of upstream to downstream
pressure across the injector) indicating an expansion of a two-phase flow. There are a
number of benefits that corne with flash boiling injection including enhanced
atomization, increased initial spray-cone angle for faster fuel-air mixing and reduced
spray penetration [3].
Flash boiIing phenomena may have applicability to both current and future engine
technologies. The present MPR study is an attempt to reduce the flash boiling injection
problem to a manageable state for investigation. In sirnplifying the experirnent to a
steady state problem, the intake port environment must be analyzed to determine which
phenornena are significant.
2.2. Intake Port Phenornena
To characterize the injection event for the purpose of experimental design and to
determine the effects of reducing the injection environment to a steady state system it is
necessary to discuss the nature of the flows within the intake port. In a MPFI engine
there is a fueI injector in each engine intake port. In MPFI spark ignition engines three
major intake-port flow processes can be established [7].
1. Overlap backflow is the reverse flow blowdown period just after the inlet valve has
opened when the cylinder pressure is higher than the intake manifold pressure.
2. Mixing between the backflow and fresh charge occurs in the intake. so these two gas
mixtures do not rernain segregated. This is often referred to as a forward induction
flow.
3. It is normal design practice to have the intake valve closed well after bottom center to
take advantage of the air's inertia. At lower speeds, however, the intake air velocity is
low and inertia effects are small. As the piston moves up from bottom center, it
displaces some of the cytinder contents back into the intake port producing a
displacement backflow.
Al1 of these processes have an influence on the intake environment and therefore have
relevance to the present study. The thermal environment produced by the factors listed
above and the engine operating conditions will have a strong effect on what f o m the fuel
transport will take. In schematic fom, the possible paths of the injected fuel tbrough the
inlet port may be represented as follows:
vapour and smaiiest droplets entrained in gas flow l
impinges on port walls
impinges on inlet valve
and/or back flow andor backflow
Figure 2.3 Possible fuel travel paths through into the cylinder 171.
The focus of the present study is to observe the fuel sprays thernselves rather than looking
at the port walls and the valve surface. The air flow and backflow through the port
effects the fueI that impinges on the port and valve surfaces but would have a lesser effect
on the fuel spray itself.
2.2.1. Fuel Transport Phenornena
Research at a number of institutions has Ied to the development of theories on fuel
transport phenomena. The fuel transport phenomena described here is based on ectual
engine operation [8]. Fuel behaviour rnechanisms include:
1. Strip-atomization of film fuel by the intake flow.
2. Squeezing of the fuel film between the intake vdve and valve seat surface as the
valve closes, to form large droplets.
3. Deposition of liquid fuel as films distributed on the intake vdve and head region.
In this study it was found that injection geometry, injection timing, fuel-to-air ratio and
port surface temperature d l influence the fuel behaviour [8]. The following flow diagram
shows the sequence of events that determine the liquid fuel evolution through the intake
systern to the cylinder.
1 intake valve open j
entq of visible dropIet j Stream md liquid film
intake valve closed : film squeezing droplets splashing
liquid film deposits on walls
combustion I I
1 survival of films
I 1
into next cycle 1 - --
Figure 2.4 Liquid fuel evolution through intake system [8].
When the intake valve opens (NO), the cylinder pressure is initially higher than the
intake manifold pressure leading to a backflow into th3 intake manifold. When the
pressure differential between the cylinder and the intake manifold reaches equilibrium,
the backflow stops. When the piston starts to move down, the induction phase of the
cycle begins and a high-speed airfiow into the cylinder is produced. A visible Stream of
liquid fuel droplets and liquid film wall flow has been observed to enter the cylinder
before the intake valve closed [8]. The closing of the intake valve was found to produce
an interesting flow pattern in the cylinder. When the valve closed, any fuel film present
on the valve seat was squeezed out and produced a splashing effect that introduced
relatively large droplets into the cylinder. Some of the liquid fuel that reaches the
cylinder can f o m isolated puddles that are not cornbusted [8]. Further investigation in a
transparent research engine again showed the three distinct phases of fiel droplets p s t
the intake vdve as descnbed in figure 2.4 tg].
The most significant fuel atomization process was concluded to be strip-
atomization. The fuel injection event produces fuel films on the port, intake valve stem
and the back of the intake valve surfaces. Strip-atomization is the hydrodynamic
stripping of droplets frorn these fuel films by the shear stress of the intake flow. This
process was found to be dominant for both closed and open intake valve injections.
Furthermore, the reverse blowdown process has been identified as an important factor in
the mixture preparation process at part load and has a direct link to stnp-atomization [IO].
The reverse blow-down process significantly strip-atomizes the liquid fuel in the vicinity
of the intake valve and changes the thermal environment of the intake port, which aids in
liquid fuel evaporation [a]. The fuel deposited on the valve and the port surfaces was
found to be pushed towards the cylinder by the shear stress applied by the intake airflow
and by gravity. Large quantities of liquid fuel reaching the cyIinder can cause increases in
hydrocarbon emissions. This illusrrates a need for improvement of port fuel injection
technology under warm up conditions.
2.3. Hydrocarbon Emissions
Although the preliminary phase of this project did not involve fired engine
conditions, the ultimate goal is to fire an engine and acquire HC emissions information.
HC emissions are at the greatest concentration during the starting, warm-up and transient
processes in spark ignition engines [ I l . The main reasons for these increased HC
emissions are:
1. Fuel enrichment is used to achieve desired driveability and performance levels.
2. It takes a finite amount of time to warm up a catalytic converter rendering it
inefficient for the first few minutes of operation.
3. Crevice volumes are largest when the engine is cold.
4. Mixture non-uniformity and quenching is more pronounced in a cold engine which
can lead to incomplete combustion.
5. Liquid fuel effects - liquid fuel can reach the cylinder as described in the previous
section.
It is hypothesized that HC emissions levels would drop with the implernentation
of the fuel preheating systern developed for the present work. The mechanisms for HC
formation due strictly to the evohtion of liquid fuel through intake port are described in
the paragraphs to follow.
In port-fuel injected engines, the injector wil1 normalIy direct the liquid fuel
towards the back of the intake valve and the surrounding port surfaces [ I l ] . Most of the
injected fuel will impinge on a surface, while a small arnount may evaporate from the fuel
droplets formed in the atomization process. Fuel vaporization that occurs when droplets
impinge on cylinder head waIls is strongly effected by the wall temperature. When the
fuel is injected on a closed intake valve, the fuel vaporization process is aided by a rapid
backflow of burned gases from the cylinder when the intake valve opens. If the fueI is
injected on an open intake valve, the vaporization of fuel off impaction surfaces is
decreased and a greater amount of liquid fuel can enter the cyIinder in the f o m of
entrained droplets or rivers. A large part of the liquid would evaporate and mix with the
in cylinder air, fuel vapor and residual gas to form a normal combustible mixture during
intake and compression. Any liquid remaining, particuIarIy less volatile components,
may be stored in deposits, oil Iayers or crevices and corne out into the bulk gases during
expansion and exhaust increasing HC emissions.
A number of studies have been carried out to investigate the possibility of
irnproving the fuel injection process in a port injected engine. Most studies focus on
vaporizing liquid fuel after injection, whereas the focus of this study was to preheat the
liquid fuel prior to injection in order to induce improvernents in vaporization.
3. Previous Work
Automotive fuel metenng systems have undergone numerous modifications over
the last LOO years. From carburetion to fuel injection, many of these modifications have
been necessary due to ever increasing engine performance standards including exhaust
emissions level regulations and power requirements. The history of fuel metering
methods are discussed bnefly as an introduction to the previous work done in the field of
fuel delivery.
3.1. History of Fuel Metering Systems
One of the original methods of fuel preparation was the surface carburetor
designed by KarI Benz. The carburetor was used extensively but it was soon discovered
that a tight control of fuel-to-air (F/A) ratio could not be achieved. In 1898, the Deutz
engine factory developed a fuel injection pump. As early as 1903, the Wright Brothers
used port injection in a four-cylinder engine to power their first flight. In 1930 the
German Aviation Research Institute initiated a direct injection development program due
to the introduction of a diesel fuel pump. The possibility of fillinp the cylinders more
completely with air without the hindrance of a throttIe plate provided increased power
gains. Even with port injection there is a gain in air induction over carburetors. In the
late 1950's Daimler Benz switched from direct injection to port injection for the first time
in a production vehicIe, the Mercedes-Benz 300. In the 1950's Bendix published its
electronic fuel injection systern and Bnsch developed technical solutions to the electronic
systern. In 1967 the D-Jetronic unit was introduced and many automotive manufacturers
implemented the system. This well adapted system couId simply replace the carburetor
without a lot of other add-ons. When ernission control legislation became more stnngent,
exhaust gas recirculation (EGR) and new control systems became necessary. This Ied to
the mechanically controlled continuous injection K-Jetronic system and the electronically
controlled intermittent injection L-Jetronic system that are still used today in rnany
engines. Single point and multipoint injection systems in various configurations have
been under development since their originai introduction over one hundred years ago
[ E l .
3.2. Previous Research
3.2.1. Fuel Vaporizing Systems
Vaporizing fuel just after injection has been studied as a means of reducing engine
HC emissions. This process has been referred to as pre-vaporization meaning that the
fuel is subjected to a vaporizing technique prior to induction into the cylinder. It has been
shown that pre-vaporization effectively decreases fuel droplet size or eliminates droplets
altogether which can irnprove the mixture preparation process and decrease the need for
over-fueling during engine start up and transient operation. Decreased fuel droplet size
has also been shown to reduce HC emissions during steady state engine operation [13].
Pre-vaponzation is essentially a post injection technique to reduce HC emissions while
the proposed preheating method is carried out prior to injection.
The effect of heating a fuel impaction surface prier to fuel and air entry into the
manifold was investigated at Ford Motor Company [14]. Heating the manifold in an
atternpt to preheat the intake air was investigated experimentally and analytically. It was
found that heating the intake air is not the best method for improving fuel air mixture
preparation because the heat of vaporization rnust transfer from the air to the fuel in a
Iimited time period. In order to achieve this, there rnust be an excessively high
temperature gradient between the air and the fuel. It was found that only 5 to 40 % of the
fuel was evaporated depending on engine operating conditions used and the mode1
assumptions. To investigate the possibility of using this locd heating method a test
fixture was designed. The fixture included a standard Bosch injector placed upstream of
a throttle plate. A coil-heated section was placed just downstream from the throttle plate.
It was found that local heating vaporizes the fuel before it enters the intake manifold and
eiiminates most of the fuel delivery problems in a Iaboratory situation [14].
Unfortunately, system response times, w m - u p time and efficiencies were nci included
in this study but would prove to be important in determining if the system is feasible in
practice.
A study by Heywood used a single cylinder research engine and a pre-vaporizing
system with a set of test variables including fuel injection schedule, inlet pressure, engine
speed and enrichment [l] . The system used a separate injector in order to carry out fuel
vaporization. Just downstream of the secondary pre-vaporizing injector a heating coi1
was wrapped around a tube and used to quickly heat the fuel. Compressed air was used
to create swirl and displacement flows within the tube and thereby entrain vaporized fuel
into the engine cylinder. When the pre-vaporization system was used, the port injector
was deactivated. The most significant conclusion made with respect to pre-vaponzation
fuel injection was that stable engine firing was achieved at the first engine cycle of
injection without enrichment and with reduced HC emissions [l].
ln a third study of fuel pre-vaporization, some preliminary computer modeling
work was cited as a proof of concept for experimental investigation [I5]. The computer
model showed that the light constituents of hydrocarbon fuels are the main components
that evaporate during cold start conditions. It was found that as little as 20 % of the
metered fuel is evaporated before reaching the inlet valves.
Other methods have been investigated as a means of improving the fuel delivery
process. Attempts have been made to study the effects of heat transfer, specifically
heating the injector body, as a means of improving fuel delivzry characteristics.
3-2.2. Heat Transfer
In recent years a number of investigations were carried out in the area of heat
transfer as it relates to fuel preparation in a port injected engine. Positive temperature
coefficient (PTC) heaters were investigated as a method of fuel injector heating. These
self-regulating cerarnic heater devices have been used in the past for the purpose of
preventing wax formation in diesel fuel filters [Io]. The PTC heater was tested using a
CFD approach to investigate heat transfer characteristics to a pintle type injector [17].
The model included two heaters, one at the injector inlet and one at the outlet and
assumed a wide-open injector for maximum flow rate and therefore maximum required
heat transfer. It was found that heat transfer rates were significantly lowered when the
injector body temperature was increased with the PTC heaters. When a layer of fuel
vapour formed between the liquid fuel and the injector it acted as an insulator and
prevented the necessary heat transfer [17]. The main problem with such a system for the
purposes of this research is that the upper temperature limits of PTC heaters do not
appear to be high enough so a more advanced control strategy was designed for fuel
heating purposes.
3.2.3. Fuel Sprays
The quality of a given fuel spray is controlled by a variety of factors including fuel
injector nozzle type and geometry, the injected liquid fuel properties and the gas
properties into which the liquid fuel is injected. Two injectors have been used in the
present study. Obtaining an understanding of the fuel sprays each injector develops with
a certain fuel is important before comments on any changes that arise due to preheating of
the fuel can be made.
It has been shown that the combination of liquid properties suc11 as density,
viscosity and surface tension influence the ability of a given fuel injector to produce an
atomized spray under low manifold pressure conditions [Ml. In some cases, with pump
grade gasoline as the injected liquid, the injector will achially produce a pencil-jet spray.
In a pencil-jet spray the fuel is not well atomized but instead it is in the fom of a thin
liquid stream that breaks down into large irregular liquid droplets. It was found that
pump grade gasoline was more likely to forrn a pencil-jet than a pure fuel. In this study
no real concIusions were made as to why this was the case but it rnay be due to the
heavier HC components present in the gasoline. In addition, gasoline may have other
additives that could influence the fuel spray break-up 1181. This evidence indicates that
choosing a pure hydrocarbon test fuel may be beneficial in tems of fuel spray
repeatability.
Fuel injectors that are used in MPFI applications are known to produce sprays that
are not very welI atomized. In fact, the first step in the present study was to look at the
spray developed by a Ford fuel injector in order to show the possible room for
improvement in a qualitative sense.
Saito et al. developed a method for observing fuel behaviour in the intake
manifold [19]. A section of the lower intake runner was replaced with a transparent
acrylic material for observation purposes. It was found that droplets with a diameter of
approximately 30 pm or less were transported by intake air into the combustion chamber.
Droplets larger than this threshold value impacted on port and valve surfaces. Port wall
wetting has been established as a major cause of start-up and transient HC emissions
increases.
A wide range of liquid fuel spray patterns can be achieved depending on the
injector used. One study in particular investigated the effects of droplet size, intake valve
lift (open or ciosed valve injection) and coolant temperature on engine HC ernissions
[20]. Three different fuel injectors were used in order to Vary the fuel droplet sizes.
Yang et al. concluded that, in generaI, decreased Fuel spray droplet size Ieads to a
decrease in HC emissions. Similar resuits were obtained in another experimental study
done by Shayler et al. [21] where it was found that HC and CO emissions are influenced
by both injector type and fuel composition.
A third study looked at the intake fuel preparation system from an analytical
perspective [22]. The simulation model treated the process as a multiphase flow
phenomenon with a gaseous (air and fuel vapor) phase, a dispersed phase (droplet
population) and a continuous phase (liquid film flowing on the wall). In accordance with
experimental studies carried out in the past, the multi-component fuel-droplet model
indicated that droplet size is the most important factor related to fuel vaporization. As the
droplet size decreases the vapor fraction increase was found to be exponential [22].
These trends illustrate a need for improved injector performance in the form of
improved fuel atomization. Specifically, improvement is required dunng engine w a m up
conditions and might be achieved with the aid of a fuel preheating technique.
4. Preliminary Experimental Work
A previous experimental investigation looked at improving residential oil furnace
burner operation [23] . In oil furnace burner applications, emphasis is typically placed on
providing a mechanical break-up mechanism of liquid sprays. In the study camed out by
Sloss. the possibility of exploiting themodynamic properties as a means of enhanced fuel
spray atomization and evaporation was investigated. The main objective of this research
was to carry out a photographic study on the phenornenon of flashing injection and rapid
evaporation of heavy hydrocarbon fuel sprays. A method was devised to control the
pressure drop across the nozzle and the temperature upstream of the nozzle and thereby
set the thermodynamic state of the fuel spray. This technique of superheating the fuel
prior to injection is quite similar to the methods proposed in the present study. In fact.
with the steady fuel spray and the use of a simple converging nozzle the problem was
simplified as much as possible. In a port injected engine, the fuel spray is a pulsed flow
through a nozzle with a more complex geometry. For that reason i t was decided to begin
the present study with a set of preliminary experirnents utilizing the apparatus designed
and construcred by Sloss. The SBR (Simonet-Behar-Rauzy) equation of state
[24,25,26,27] was used to develop a pressure versus volume and a pressure versus
temperature plot and to calculate Jakob numbers for iso-octane. A list of data for iso-
octane has been included in Appendix A. The plots and Jakob numbers were used to
Iocate a given fuel state dunng experimentation. It was anticipated that these
experiments would provide a proof of concept for the present study as well as aid in the
development of a functional preheating port injection system in order to expand this line
of research.
4.1. Experimental Apparatus
A basic schematic diagram of the system used is shown in figure 4.1. The details
of the apparatus and the hardware used can be found in reference [33]. The nozzle was
mounted at the top of an injection chamber facing downward. A 1.0 bar nitrogen
environment was maintained within the injection chamber to prevent the formation of
combustible mixtures. Two sides of the injection chamber were equipped with view
ports for optical access and lighting of the nozzle exit and the fuel spray. A single shot
photography system acquired images of the spray event. The f~irnace section, constmcted
of refractory brick, heated the fuel line to the desired temperatures. A 1450 W finned
heater was the primary heating method and a 150 W band heater the secondary heating
method. The nozzle was a simpIe conical body converging nozzle with an exit diameter
of 0.2 1 mm with a converging half angle of 45 degrees.
fuel in
capillary tube
injection - chamber
4 drain
Figure 4.1
J- accumulator
Apparatus schematic diaoram f251.
fuel reservoir
4.2. Data Acquisition
A number of important parameters were monitored during the experirnents.
National Instruments hardware and software were used to acquired data for the
experiment. A detailed discussion of the LabView programs, tnggering methods and
event coordination techniques can be found in reference [23]. Thermocouple
measurements of furnace temperature and nozzle fuel temperature were acquired.
Injection pressure was measured with a strain gauge pressure transducer. The
corresponding data and photographs for each experiment were saved and recorded after
each run for later development and analysis.
4.3. Experimental Procedure
The detailed procedure carried out for each experiment is laid out in reference
[23]. A brief description is included for clarity. Although the experiment was originally
constructed for relatively heavy hydrocarbon fuel sprays, no hardware modifications
were necessary to produce an iso-octane spray. Iso-octane is a relatively light
hydrocarbon and was the research fuel used for a11 experiments camied out in this thesis.
A general description of the experimental procedure used is as foIlows:
1. The fuel supply systern was flushed clean of any previous experimental fuel.
2. The computer data acquisition system, camera, microflash and sensors were powered
up and prepared.
3. The upstream pressure was set and verified. (Note: Only one upstream pressure was
used for any given experiment. In other words, upstream temperature was the
variable that was incremented dunng an experimental run.)
4. The heaters were powered up and aIlowed a significant arnount of soak time
(approximately 1 hour or more) to reach the desired steady state upstream fuel
temperature.
5. A nitrogen environment within the spray chamber was maintained for safety reasons.
6 . A control valve was then opened producing a steady fuel spray. The upstream fuel
line pressure provided a threshold triggering signai to the data acquisition system.
7. A single photograph and the corresponding temperature and pressure data were
acquired with the aid of the data acquisition software.
The experirnental test matrix for the steady spray experiments included at least ten fuel
temperatures at each of the two pressures. Two sets of data, including a photopraph,
were acquired at each ternperature to ensure that a good quality image was obtained.
4.4. Results and Conclusions
Figure 4.2 shows the developrnent of the spray as the upstream ternperature is
increased. The normal boiling point for iso-octane is 99OC. In this case the upstream
pressure is 3.77 bar which is a typical value for the pressure in the fuel rail of a port
injected engine. The Jakob numbers corresponding to figure 4.2 are 0.00 and 0.59
respective 1 y. The Jako b nurnbers are calculated using upstream temperature and a
downstream pressure of 1 atm to characterize a given fuel spray. In figure 4.2, the first
image shows a thin fuel Stream at an upstream temperature of 30°C while the second
image shows a finely atornized spray with a large cone angle at an upstream fuel
ternperature of 160°C. The Jakob numbers corresponding to figure 4.3 are 0.33 and 1.14
respeciively. Figure 4.3 shows a similar development trend at an upstream pressure of
1 Obar with an upstream fuel temperature range of 135°C to 2 10°C-
Both of the figures illustrate a transition or a chznge in the fuel spray appearance.
Figure 4.2(a) shows a thin Stream of liquid fuel issuing from the nozzle while the
rernaining pictures illustrate different flashing flows. In figure 4.2(a) the jet appears to be
slightly larger in diameter in the upper section of the image. Surface instabilities become
visible just after the fuel exits frorn the nozzIe. The jet appears to be quite unstable
further downstream from the nozzle and break up into individual droplets is beginning to
occur. Preheating of the fuel to 160°C changes the fueI properties and causes the jet to
break up just downstream from the nozzle exit. Vapour bubbles nucleate and grow
within the superheated liquid, expanding the jet. Relatively large liquid droplets stiil
appear visible in the spray.
Figure 4.3 illustrates fuel sprays at different upstream fuel iemperatures chan
figure 4.2 at an upstream pressure of loba . A photograph of the coid liquid jet was not
included at this upstream pressure because there was little difference between this jet at
the two test pressures. Figure 4.3(a) shows a coherent fiashing spray at 135°C while an
increase in temperature to 2 10°C in figure 4.3(b) shows an increase in the jet cone angle
and a decrease in the coherent jet spray penetration distance. Both sprays appear to be
finely atomized at the elevated temperatures and liquid droplet size appears to decrease
from figure 4.3(a) to figure 4.3(b).
After preliminary results were obtained, it was hypothesized that a sirnilar result
would to be beneficial in a port injected engine configuration. In order to prove the
beneficial effects of preheating liquid fuel prior to injection it was first necessary to
observe similar fuel spray characteristics in a functional intake manifold.
Figure 4.2 Injections of iso-octane through the converging nozzle at 3.8 bar and increasing upstrearn temperatures: a) 30°C (0.56 Tc) and b) 160°C (0.80 Tc).
Figure 4.3 Injections of iso-octane through the converging nozzle at 10.0 bar and increasing upstream temperatures: a) 135OC (0.75 T c ) and b) 2 10°C (0.89 Tc).
5. Experimental Apparatus and Equipment
A port fuel injection system was designed to deliver fuel with variable liquid
temperatures upstream of the injector. The experimental setup was developed to simulate
a variety of engine operating conditions with a focus on a cold engine start condition at
1000 rpm. In order to simulate the desired engine test conditions a number of parameters
were set and monitored. These parameters inciude; cylinder head temperature, fuel
supply temperature upstream of the injector, fuel pressure upstream of the injector,
throttle position, the gas flowrate through the intake port and the delivered fuel mass
flowrate. For the purposes of this research, the engine was not motored or fired, the
engine airflow was sirnulated with steady nitrogen flow through the single cylinder intake
system. Two injectors were used for the experiments; a computer controlled injector for
low temperature injections and a modified mechanically actuated injector for both low
and high temperature injections. A modular approach was taken with the fuel injectors
and fuel delivery systems in order to allow for simple changes between systems.
5.1. Engine Specifications
A 1.9 L four cylinder MPFI Ford spark ignition engine has been converted to a
single cylinder steady flow research engine. This engine was chosen because it was a
four cylinder, single overhead Cam, port injected engine with an aluminum cross flow
cylinder head and alurninum upper and Iower intake manifolds. An engine with a single
overhead Cam was appropriate because with this configuration push rods are eliminated
leaving more room for instrument accessibility around the periphery of the cylinder head.
An in-line cylinder configuration with aluminum accessory parts allowed for easier
machining modifications and opticai access. The engine specifications are as follows:
Table 5.1 Engine cornponent dimensions.
Engine Component Dimension (mm)
cylinder bore
- - - - - -- 1 intake valve head diameter
stroke
intake valve Iift 11.0 1
87.9 l
intake valve stem diameter 8 .O
The Ford cylinder head was mounted to a custom made block plate that was matched to
the engine cylinder diameter. The engine was used in a single cylinder configuration so
the block plate mated with the cylinder deck to simulate an engine cylinder. The
remaining cylinders were not in use so the plate covered cylinders 2, 3, and 4. The
exhaust and intake systems are discussed in a later section.
5.2. Nitrogen Flow
Under normal operating conditions, atmospheric air is the working fluid for an
engine. Achieving combustion was not a goal for this research and since nitrogen closely
approximates air it was the best choice as the working fluid. The experiment was set up
in an engine test ce11 that was previously equipped with a high flowrate hydrogen fuel
supply system. This hydrogen systern was equipped with nitrogen purge capabilities and
was ideal for producing the needed flowrates of up to approximately 1000 slpm. A gas
rail with a single, high flowrate regulator was capable of adapting to six bottles of
compressed nitrogen sirnultaneously. The compressed gas was located extemal to the
building with a 45 psia pressure relief valve on the gas rail to prevent over-pressure. The
nitropen supply line was equipped with a gas filter and three gas solenoid valves. The
solenoid valves were actuated by a 12 VDC relay that was controlled with a simple off/on
toggle switch. Once the test ce11 power supply was turned on, the nitrogen flow started
when the toggle switch was set to on. The nitrogen flow was metered with a 12.7 mm
Nupro baIl valve.
5.3. Fuel Injectors
The low temperature injection experiments were camed out using a Ford
~Motorcraft CM-4488 EF6FZ-9F593-A fuel injector. The injector nozzle was a pintle type
with a converging geometry at the tip. Custom made injection control circuitry was
assembled. The circuitry used a 17 VDC battery input and T ï L pulses from the LabView
software and the data acquisition board to produce peak and hold injection pulses at the
injector input. Electronic control of the injector allowed for accurate pulse width and
frequency settings. The Ford injector was not suitable for delivering high temperature
fuel because of the method of injector actuation. A soIenoid-actuated injector would not
function in an elevated temperature environment because the heat could damage the
electronics and alter the induced magnetic field. It was necessary to develop a high
temperature mechanical injector to deliver fuel over a large temperature range.
The high temperature injection experiments were carried out with a custom
modified Stanadyne pencil type injector (mode1 9.5). This injector is nomally used in
compression ignition engines with direct cylinder injection. The injector was a pintle
type with a converging geometry at the tip. Injector control parameters such as lift
pressure, injection frequency and pulse width are independently set with this particular
injector which allows for the approximation of port injection conditions. The injector
was chosen for this research because its structure and method of actuation alIowed for
modifications and operation at elevated temperatures. It was composed entirely of
metallic compounds that allowed fuel delivery in the desired temperature range without
risk of interna1 component damage. Using a mechanically actuated injector, however,
increased the control problems discussed earlier. A Bosch fuel purnp was used to
develop the necessary injector cracking pressure. Lift pressure was set with the threaded
compression screw at the end of the injector. The screw compresses the spring inside the
injector, which changes the force holding the needle against the seat. As the spring is
compressed, a higher fuel line pressure is developed by the fuel pump in order to produce
a fuel spray. Three modifications were made to the injector in order to meet the operation
requirements and are described in Appendix C. One negative aspect that came with using
this mechanical injector was loss of precision control. Unlike the Ford injector, pulse
width and frequency were difficult to accurately control when using the Stanadyne
injector and Bosch fuel pümp. A second compromise that had to be made with the
Stanadyne injector was that it had an opening pressure lower limit of approximately 500
psig which is on the order of ten times Iarger than the upstream pressure of the Ford
injector.
5.4. Fuel Delivery and Measuring System
A versatile fuel delivery system was needed in order to carry out a nurnber of
important functions during experimentation. The system was required to pressurize the
fuel rail for the Bosch fuel injector, supply fuel to a mechanical fuel pump for the
Stanadyne fuel injector and act as a mass flow calibration device for the two injectors.
Schematic diagrarns for the fuel delivery systems are depicted in figure 5.1 for the
Bosch injector setup and figure 5.3 for the Stanadyne injector semp. The fuel delivery
system components are described in the following sections. The procedures used for
experimentation and fuel injector calibration are described in the next chapter.
The electric fuel pump was a 1/20 hp, 120 VAC, 60 Hz pump with a maximum
speed of 3000 rpm (Universal Electnc Company, senal # 4RA1105R, model #
ABlS076N). The pump was a thermally protected model for use with combustible
materials. The pump is actuated with an off/on toggle switch. Two fuel supply tanks or
reservoirs were used in this system as shown in figure 5.1. The stainIess steel supply
tanks each have a capacity of approximately 10 L. Each of the tanks had manual valves
on the supply end and threaded caps on the top for filling purposes. The recirculation line
from the fuel rail couId be connected to either of the tanks depending on the experiment
being conducted. The recirculation cap was equipped with a 3 psig relief valve to avoid
any reservoir pressurization. Two tanks were used in this system for versatility reasons.
Under standard opersiting conditions, both tanks contained a research grade fuel. When
two fuels were used, supply tank #1 contained pump grade fuel and supply tank #2
contained research grade fuel. This allowed for the use of a variety of research fuels
some of which could be corrosive to the fuel injector. After the system was run with the
corrosive fuel the pump grade fuel could be used to rinse the injector and thus prevent any
injector damage. A second reason for having two fuel reservoirs was to allow a
separation of the mass measuring side of the system from the bulk fuel supply side. This
spread the components out and provided roorn for the mass scale enclosure.
Most of the fuel lines shown in figure 5.1 were 6.4 mm stainless steel lines joined
with Swagelok fittings. Rubber fuel Iine, 7.9 mm in diameter, was used for the line from
the pump to the fuel rail and the recirculation line from the fuel rail pressure replator to
the reservoir to alIow far easy mobility.
A number of valves were used in the system. All of the valves that are not shaded
are manually controlled open/close valves that were positioned in various locations to
provide a range of system configurations and to allow for simple disassembly. The
mechanical valves are labeled 1, 2 ,3 and 4. The three shaded valves numbered 1, 2 and 3
are electronicall y controlled, 120 VAC, 60 Hz solenoid valves (Asco solenoids)
controlled with solid state relays (Crydom SSR, 120 V, 10 A, 3-32 VAC control). Valves
1 and 2 are two way valves, meaning that there are two States of operation. The fueI flow
input side is always the same but the fuel flow output can be changed between two
possible paths depending on the solenoid state. The non-energized state for these two
valves is depicted schematically as straight through in figure 5.1. The energized state is a
90 degree angle in schematic form. Valves 1 and 2 are controlled by a relay, which is in
tum computer controlled. Valve 3 is a one way solenoid valve, meaning that it is either
open or closed. The non-energized state is closed. This valve is controlled with a simple
hand operated toggle switch. The purpose of these valves will become clear when the
overall system operation is explained in the next chapter.
Two fuel filters were added to the fuel line. One of the filters uses a second fluid
to filter the fuel. The second filter is a meshed barrier to remove any particulate matter in
the fuel flow. The fuel measuring side of the fuel delivery system was mainly used for
injector calibration. The mass measurïng part of the fuel delivery system was made up of
a digital scale, two enclosures and a fuel reservoir. The small reservoir was composed of
stainless steel and had a fuel level indicator made of clear tubing fitted on the side. A
Sartorius (model# 1404MP8) digital scale was used to make mass measurements. The
scale limit was 2.0 kg and it was accurate down to hundredths of a gram. The scale was
also equipped with a leveling bubble to ensure that the mass measurements would be
accurate and consistent. The small reservoir and the digital scale were completely
enclosed in Plexiglas. The purpose of this enclosure was to obtain mass measurements
that were not affected by any air currents in the laboratory. The digital scale used was
very sensitive to any disturbances and for that reason was completely isolated. A rubber
boot was used to seai tne top of the small reservoir with the roof of the Plexiglas box in
order to capture any fuel vapor and improve systern accuracy.
fuel reservoirs pressure relief valve
fuel rail pressure
m füel rail temperature
pressure 1 I regulator
1
i ipj 1
fiel i level fiiel return Iine u-
i .w , isolated tùel injectors
Figure 5.1 Ford Injector fuel supply system.
5.5. Ford Injector Fuel Supply System
The fuel rail was mounted to the Iower intake manifold (not shown) as per the
stock Ford layout for the experiments and for fuel injector calibration. The fuel delivery
system utilized the standard Ford fuel rail and Ford injector. The fuel rail is designed to
accommodate four fuel injectors, one for each engine cylinder, however only one injector
is shown in figure 5.2. The other three injectors were present to seal the fuel rail properly
but they were not pulsed and were therefore inactive. Leaving the three inactive injectors
in place was the easiest way to seal the fuel system without having to make modifications.
The fuel rail came equipped with a fuel feed line, a fuel recirculation line, a threaded fuel
pressure relief fitting and a pressure regulator. As shown in figure 5.1, the fuel feed line
was lengthened and connected to the pump and the recirculation line was connected to 2-
way solenoid valve #2. Since the fuel rail pressure could be released by disconnecting the
fuel rail feed line, the fuel rai1 pressure relief fitting was used to acquire a fuel rail
pressure and temperature reading. A 3.2 mm Swagelok T fitting was adapted to the
pressure relief fitting. On either side of the T fitting an analogue pressure gauge and a K-
type ungrounded thermocouple were mounted using Swaplok. AS shown i n the figure,
the pressure regulator rnaintained a fuel rail pressure relative to atmospheric. One side of
the repulaior, usually connected to the intake manifold which is at a vacuum under
normal engine operating conditions, was left open to atmospheric pressure and the other
side monitored fuel rail pressure. When the pressure in the rail exceeded 39 psig the
pressure regulator opened a fuel recirculation valve and allowed fuel to flow back
towards Zway solenoid valve #2. In this way, the fuel rail pressure was maintained at 39
psig.
high flow rate pressure reguIator
plate
hot water feed
water r e m
'/ I upper manifold , lower manifold
cylinder 4 1 1 fi~el feed
condenser J7
injected fuel collection
Figure 5.2 Ford fuel injector setup.
5.6. Stanadyne Injector Fuel Supply System
The Stanadyne injector was chosen because it is a mechanically actuated injector
and was deemed suitable for modifications and for high temperature fuel flow. The fuel
supply system for the Stanadyne injector is shown in figure 5.3 in schematic form. This
injector required the use of a single cylinder Bosch rotary pump (senal #
PFRIKSOA427/1 l) , often referred to as a jerk pump, in order to develop the necessary
injector opening pressures. The maximum pressure the pump was capable of developing
was approximately 5000 psia, well within experimental requirements. The purnp has a
barre1 diarneter of 7.50 mm with a range of delivenng quantities from O to 120
mm3/stroke. Under normal operation, a mechanical injection pump would be coupled to
an engine camshaft, which turns at half the crankshaft rpm. In this modified, research
application, the pump speed was set and maintained with the aid of a 1 hp Woods SCR
motor and controller (serial # 1382). The motor used 208 VAC, 3 phase supply voltage
and provided a maximum speed rating of 1750 rpm but was only used up to 600 rpm.
Initially, the pump and rnotor were rigidly mounted and the shafts were directly linked
through a steel coupling. A number of configurations were tested before it was
determined that a gearing system was necessary. A 2.9 to 1.0 gear ratio was chosen to
allow the rnotor to rotate closer to its normal operating speed limit. This lowers the
torque requirernents and provides as constant a rotational speed as possible. This specific
ratio was chosen due to limitations in space around the pump and motor. Toothed gears
and a toothed belt were chosen to avoid slippage. The motor controller allows
independent rnotor torque and speed settings, however, maximum torque was the only
setting used during expenmentation because the torque requirement for the pump varied.
In an attempt to rnaintain a constant pump rotational speed it was detemined that the
maximum torque setting would minirnize speed variations particularly at low rpm. The
electric fuel purnp, that was part of the main fuel delivery and measuring system, was
used to supply the inlet to the mechanical fuel pump with fuel at 40 psig. This pressure
was set with a Swagelok, variable opening pressure, relief valve (mode1 #B-KA-50).
The supply pressure to the pump was relatively low so 7.9 mm diameter rubber fuel line
was used to allow for simple system rearrangements. The fuel line from the pump to the
Stanadyne injector was a 3.0 m length of stainless steel chromatographie tubing with an
44
intemal diameter of 1 mm. This small diameter tubing was chosen to minimize the
internai volume from the pump to the injector in order to minimize fuel compressibility.
The fuel line pressure rating was well above experimental levels whiie the tubing wall
thickness was thin enough to allow for small radius bends. A Iength of 3.0 m allowed
enough fuel line to tightly wrap around the heater bar and maximize the heat transfer to
the fuel.
fuel reservoirs - - - -?, pressure relief
valve
electric fiel pump
l torque 0 l
Stanadyne
isolated rneasurement
Figure 5.3 Stanadyne Injector fuel suppl y system.
5.7. Fuel Heating System
Two heaters were used to achieve the desired liquid fuel temperatures just
upstream of the injector. The complexity of the heat transfer problem made it difficult to
calculate the system requirements necessary to heat the liquid fuel to the desired
temperatures. Some of the issues involved included heat transfer to the liquid fuel
through a complex geomtry, intermittent liquid flow and liquid compressibility. It was
not realistic to attempt an accurate calculation including al1 of the variables involved. A
high wattag heater was chosen to ensure that the desired temperatures were attainable
and a secondary heater system was included as a factor of safety. The primary heater was
a Caloritech 3500 W. stainless steel cartridge heater (CIR 4360). The heater was 15.9
mm in diameter and 9 14.4 mm in length. It was capable of temperatures up to 650°C but
the unit was chosen for its high heat flux capability. A number of accessories were
needed in order to accurately set and control the heater temperature and a wiring diagram
is shown in figure 5.4. An Omega CN77332-A2 digital feedback control unit was used in
conjunction with an Omega solid state relay (Omega SSR, 220 VAC, 25 A, 3-32 VDC
control) for this purpose. The digital control was equipped with a PID option with
temperature feedback. This option was chosen in order to maintain the heater
temperature as close as possible to the desired set point temperature. The PID settings
used were proportional band of 300°C, reset of 300°C and rate of 0.0 s (i.e. not in use).
As figure 5.4 shows, it was necessary to use three different power supplies for the heater
control system. 120 VAC to power the digital controller, 12 VDC to actuate the SSR and
a single phase of a 208 VAC line to supply current to the heater through the high voltage
side of the SSR. An ungrounded thermocouple (GKQSS-18U-12) was used as the
feedback source to the controller.
t feedback thermocouple
-
t emperature controller
i i
I I l
i l
Figure 5.4 Heater control system.
The secondary heater was an Omega 120 VAC, 720 W heater and controller
(HTWC 10 1-010). The heater strap was 25.4 mm in width and 254.0 mm in length. This
heater was wrapped around one of the fuel supply reservoirs in order to give the bulk fuel
mass any desired amount of preheat up to approximately 50°C. The heated fuel supply
reservoir was Iocated before the electric fuel pump so to avoid fuel pump damage it was
decided not to exceed approximately 50°C. The heater was tightly wrapped around the
metallic reservoir and three layers of fiberglass insulation with a maximum temperature
rating of 550°C (Intertex Textiles) were wrapped around the heater. A simple analogue
control unit was used to set the heater temperature. No attempt was made to implement a
feedback control system for this heater because accurate temperature was not crucial this
far upstrearn of the injector. The heater
checked during each expenment and was
ternperature was set to the desired value and
found to maintain the reservoir at a constant
value. The important temperature value was the fuel temperature at the entrance to the
injector and the primary heater was used to obtain an accurate temperature at this point.
With both heaters working it was found that after a sufficient soak time of approximately
10 or 15 minutes, the primary heater temperature would not vary from the set point
ternperature by more than 0S0C. It was found that the fuel preheating system was
capable of supplying fuel up to a temperature of 220°C with a 95.0% confidence interval
of less than 0.7"C on the mean fuel temperature in an experirnental set.
5.8. Exhaust Management
A custom designed system was assembled to collect fuel in liquid and vapour
form. Any fuel injected onto the valve of the experirnental apparatus would flow down
the cylinder head wall surfaces and into the cylinder. A valve was placed at the bottom of
the simulated cylinder for liquid fuel collection. Any entrained or vaporized fuel that
found its way beyond this point was condensed in a cold trap. The trap was made
primarily of ABS plastic and a schematic is shown in figure 5.5. When the heated fuel
injection experiments were carried out, ice water and liquid nitrogen were used to cool
the condenser walls. The fuel vapour and nitrogen mixture would flow through the
condenser core with ice water in the outside 50.8 mm enclosure and liquid nitrogen in the
inner 6.4 mm enclosure. The fuel vapour would condense on the outer surface of the 6.4
mm Swagelok tubing and on the inner surface of the 50.8 mm A13S enclosure.
Figure 5.5 Condenser system.
5.9. Data Acquisition Hardware
In order to cany out the fuel injector calibrations and to acquire data at moderate
acquisition rates for al1 the experiments a relatively versatile data acquisition (DAQ)
board was needed. For that reason, a National Instruments ATMIO16E-IO board was
purchased dong with a SC-2070 termination board.
The National Instruments ATMIOl6E-IO board is a 100000 Hz board, equipped
with 16 single ended or 8 differential analogue inputs, digital input and outputs. The
board was configured in the differential mode of operation for the purpose of data
acquisition. Seven of the eight analogue inputs were used to acquire differential voltage
signals. Five digital lines were also used as counters, triggers and timing signais
acquisition, event coordination and injector pulse control. The following is a s
table of the channel configurations and channel types used.
Table 5.2 Data acquisition channel information.
for data
~umrnary
- I - -
Channel Label Channel Function
/ differential analogue O** 1 cold junction
differential analogue
L
differentia1 analogue
thermocouple
1,9 thermocouple
differential analogue
1 differential analogue
' differential analogue
MAP pressure sensor
1
differential analogue
3,11
4,12
hotwire fiow meter
thermocouple
thermocouple
counter
differential analogue
injector puIse
counter gate
7,15 Schaevitz pressure transducer
Ctrgate
I trigger 1 PFIO
putse gate
external trigger
camera trigger and injector lift counter I
counter
digital output
Ctr 1
counter
relay control
A shielded cable (National Instruments SH6850) connected the data acquisition board to
the SC-2070 termination board. The SC-2070 board was used for signal termination,
signal filtering and thermocouple cold junction compensation. The SC-2070 board was
PFI2 extemai timing
incorporated into a surge protection box in order to protect the data acquisition board
from signai line spikes.
5.10. Sensors
A range of sensors were impiernented to fully characterize the fuel injection event.
In fact, a number of sensors were caiibrated and later determined to be unsuitable for use
before a functional data acquisition system was in place. A surnmary of both sensor
location and sensor noise level are listed in table 5.3. The calibration equations that were
developed for each sensor are listed in the sections to follow. The developed equations
were incorporated into the LabView data acquisition software. The calibration
procedures are listed in Appendix E.
Table 5.3 Sensor locations and noise levels.
Sensor
chip
themocouple
t hermocouple
therrnocouple
thermocouple
MAP
hotwire
Schaevi tz
Sensor Location
on board cold junction compensation
upper intake manifold temperature
injected fuel temperature
injector body ternperature
local cylinder head temperature
intake manifold
upstream of throttle
high pressure feed line
Signal Noise LeveIs [mV]
Al1 the thermocouples were K-type, low noise and ungrounded sensors with
ground straps (GKQSS- 18U- 12). LabView prograrns were developed to carry out cold
junction compensation and voltage-to-temperature conversion. The thermocouples were
304.8 mm in length with a diameter of 3.2 mm to allow for mounting with 3.2 mm
Swagelok fittings.
The manifold absolute pressure ( M M ) sensor was used to measure upper
manifold pressures in order to characterîze the downstream injection environment. The
device was a 0.0 to 2.0 bar General Motors MAP sensor. A pressure tap was made in the
manifold and connected to the sensor input via 6.4 mm diameter tubing. The linear
relation developed for this sensor, relating absolute pressure to voltage, is listed in
Appendix E.
To measure nitrogen flows through the experimental apparatus a Nissan hotwire
anernometer was used (Nissan, Hitachi, 22680 53J00, AFH50-06, 0x23). The meter was
used to measure flowrates up to approximately 1000 slpm, which was well within the 0.0
to 2000.0 slpm range. The flow meter was positioned just upstream of the engine throttle
body. The calibration curve for the sensor and the charactenstic equation are listed in
Appendix E.
After testing was carried out, the best available method of acquiring a fuel line
pressure was a strain gauge pressure transducer. The sensor calibrations and the steps
taken in developing a pressure measurement system are discussed in Appendix E. A 0.0
to 1000.0 psig Durham Instruments Schaevitz transducer (P 102 1-0005, senal # 1006 15)
and a bridge amplifier were used to acquire the fuel line pressure. The transducer had a
frequency response of 3 kHz. This sensor was located just upstream of the Stanadyne
injector mounted on the end of 3.2 mm diameter, 254.0 mm length of Swagelok tubing.
A Swagelok, 0.0 to 1000.0 psig pressure relief valve (SS-R3A-KI-C) was placed in the
fuel supply line near the pressure sensor to protect it from over-pressure. The calibration
and the equation converting voltage to pressure are listed in Appendix E.
To calibrate the modified Stanadyne injector a method was needed to coont the
number of injection events during a given time period. For this purpose a lift sensor
system was developed. A Wolf Controls Corporation Hail effect micosensor was used in
conjunction with two custom designed circuits to count injector pulses. When a current is
passed through a thin metal foi1 in the presence of a magnet a current a voltage is
produced. The Hall effect is utilized in the lift sensor to produce an analogue voltage
signal that is proportional to the injector needle movement. The injector was fitted with a
custom made magnet and a sensor holder assembly. The primary circuitry used linear
differential amplifiers, a differential emitter follower output and a voltage regulator.
Since an actual lift quantity or distance could not be detemined from the analogue output
signal it was converted to a TTL pulse with the aid of secondary thresholding circuitry.
The TTL pulses were read into the National Instruments board and were counted using
the LabView software. The method for counting injections was later modified due to
poor operation of the lift sensor at elevated temperatures. The fuel line pressure sensor
signal was used as a threshold signal input to the thresholding circuitry instead of the lift
sensor signal. In that way TTL pulses were produced when the pressure signal rose above
3 set value.
Two methods were used to monitor Bosch fuel pump rotational speed. Initially a
hand held digital tachometer (Veeder Root Mode1 #66 I 1) was used to obtain a rotational
speed. After preliminary tests with the DC motor drive and fuel purnp it was determined
that a more accurate method of monitoring pump speed was necessary. A sixty tooth gear
was adapted to the coupling shaft between the DC motor and the fuel pump. A magnetic
pickup (Airpax 1-0002) was then mounted perpendicular io the sixty toothed gear at a
distance of approximately 2 mm. The magnetic pickup signal was amplified and
displayed on a Daytronic frequency indicator/controller (mode1 #3 MO). During testing
the pump speed was monitored for each set of experiments.
To trigger the camera for the Stanadyne fuel injector experiments an optical
switch was used. Since the fuel injector opened once every fuel pump revolution, a signal
produced each revolution was chosen as an external timing event. The sensor was a
reflective type optical switch (senal # OPB 701), with a custom made circuit to convert
the output to a TTL signal. The circuit was developed to convert the sensor signal to a
TTL signai only when a threshold level was exceeded. In order to minimize room
lighting effects a relatively high threshold value was chosen. In addition, the sensor was
shielded from external light. A reflective surface, approximately 30 mm in diameter, was
mounted to the gear on the Bosch fuel supply pump. The sensor was rigidly mounted to a
stand to allow positioning perpendicular to the reflective surface. In summary, figure 5.6
iIlustrates the signal connections for al1 calibrations and experiments.
Generator [ ~ ~ ~ h i l s e ; - ~ . 7 r ~ i i m a 7
From MAP sensor
From Nissan Flowmeter
From Schaevib Tranducer Bridge Amplifier
From Lift Sensor Circuit
Data Acquisition and Termination Boards (ATM10 16E-10 and SC2070)
Tirnebase Signai (PFI.2)
CJC Temperature (ACHO)
Plenum Temperature (ACH 1)
Injector Fuel Temperature (ACH 2)
hjector Body Temperatlue (ACH 3)
Local Cylinder Head Temperature (ACH 4)
Plenum Pressure (ACH 5) Solenoid Actuation @IO O)
htake Manifold (ACH 6) ihjector Pulse (Ctr O) N2 Flowrate
Fuel Line Pressure (ACH 7) Camera (Ctr 1)
Injection Count (CTRl)
- (~uel System ~elaysl
4 Injector circuit 1
4 Camera Circuit]
Figure 5.6 Data acquisition signal connections.
5.11. Data Acquisition Software
The software used to coordinate events and acquire data was National Instruments
(NI) LabView Software version 4.1. LabView is a visual programming Ianguage, which
was used to calibrate the injectors and acquire data during injection events. Using the
software terminology, the programs are referred to as virtual instruments (VI) and sub-
VIs. Each program consists of a front panel and a back panel. The front panel displays
control switches, filename inputs and numerical outputs and the back panel displays the
program structure. A brief description of the LabView programs developed for this
project are listed in Appendix B.
5.12. Data Acquisition Triggers
In order to capture an image of the fuel spray it was necessary to develop a
repeatable method of camera control for both experimental setups. Camera triggering
was accomplished with a unique method for each injector. The camera, motor driver and
flash unit were tested in order to quantify the time delay between the carnera receiving a
trigger and the flash finng. This value was found to be 92.0 ms +/- 0.3 ms rneasured with
an oscilloscope and a photoresistor circuit. For the Ford injector, correcting for this delay
was accomplished by incorporating a variable time delay into the software. For the
Stanadyne injector, the flash timing was coordinated with a software delay and proper
trigger sensor positioning. The sensor used for triggering the expenment was discussed
in section 5.10. The reflective surface was mounted such that the trigger signal would be
sent approximately 210 degrees before the cam in the pump started to lift the pump
pIunger. The start of the plunger lift is approximately the start of injection. With the
reflective surface appropriately located, the flash timing could be accurately controlled
using LabView.
5.13. Optical Access
Optical access was obtained through two view ports, one through the cylinder
head and upper manifold and the second through the lower intake manifold. The top
view-port was design to observe the fuel spray developrnent downstream frorn the
injector whiIe the bottom view-port was designed to make observations at the injector
exit. The view ports were designed to accept an 8 mm diameter Olympus Industrial fiber
optic borescope. The view port locations were shown in figure 5.2. Both ports were
designed to align the fiber optic borescope axis with the center axis of the hiel spray in
the intake port. The upper view port required significant modification of the plenum and
the cylinder head in order to position the borescope at the desired viewing angle. A
channel was machined through the plenum to accept a sleeve, which was slightly larger
than the borescope diameter. The sleeve would act to support the borescope and to seal
the plenum against nitrogen leaks. A hole was bored and an 8 mm diameter Swagelok
adapter was mounted into the cylinder head to accept the borescope. When the borescope
was inserted, it would first be push completely through the plenum and out the other side.
It would then be inserted into the cylinder head section of the view-port and Iocked down.
The second view port was located perpendicular to the tip of the injecter. A block of
aIuminum was welded to the Iower manifold and again a hole was bored and an 8mm
Swagelok adapter was mounted. Teflon ferniles were used to lightly clamp the borescope
into place in each of the view port locations.
5.14. Photographic Equipment
Obtaining photographic images of the injection event at different fuel preheat
temperatures was the primary objective of this research. Much like the sensor
instrumentation, the photographic system involved a trial and error process to acquire
quality images.
As discussed in the previous section, optical access was developrd to
accommodate an Olympus series 5 Industrial fiber optic borescope (R080-024-000-
50ILG) and OIympus light source (KLS-13 1). The borescope wcrs used for a11
expetirnentai image acquisition and provided a direct view dong the axis of the scope
body with a focusing range of 5 mm to infinity. Adapters were purchased in order to
adapt the borescope to a 35 mm camera (Nikon T-Mount and T-2 Mount adapter) and a
high speed ICCD camera (Nikon T-Mount and T-MD Mount adapter). The borescope
was equipped with an integrated light p i d e to supply illumination to the tip. Numerous
atternpts were made to increase the light intensity produced by the light source by adding
higher wattage bulbs and a custom made cooIing system but it was later determined that
only flash photogaphy could produce the necessary light intensity.
A 35 mm camera with flash photography was determined to be the best method of
acquiring images. The unit included a Nikon FM2 camera, MD12 rnotor driver and a
Vivitar 185HV flash unit. Fuji 1600 speed black and white film was used to acquire al1
fuel spray images. After a great deai of trial and error testing, the camera was set to 1/250
s exposure time (the maximum sink rate for use with a flash) and a film speed of 1600.
The flash unit was capable of producing a fiash duration between 111000 and 1130000 s
when set in automatic light detection mode. For this experimental setup, the flash
duration was effectively the exposure time. The flash unit was set to maximum intensity
and the automatic light detection mode was chosen to minirnize exposure times. To
further minimize exposure times, different light intensities, targeted at the flash unit light
sensor, were tested until. A signal from LabView was used to tngger the camera through
custom made control circuitry. A l'TL pulse entered the camera control circuit, resulting
in a shorted output terminal to the motor driver. The motor driver then actuated the
camera shutter and the camera actuated the flash unit.
6. Experimental Procedures
6.1. Calibration Procedures
The calibration procedure for each of the tv JO fuel injectors utilized the m a s
measunng and fuel supply apparatus described in sections 5.4,5.5 and 5.6 of the previous
chapter. Iso-octane was used for al1 experiments and a detailed list of the fuel properties
has been included in Appendix A. A standard calibration procedure was used to calibrate
the Ford fuel injector and is described in Appendix D. The raw data and a summary plot
characterizing the Ford injector are also included in Appendix D. A custom procedure
was utilized when calibrating the Stanadyne injector. An explanation for al1 calibration
and experimental conditions chosen has been covered in the next chapter.
6.1.1. Stanadyne Fuel Injector Calibration
A unique method was developed to calibrate the Stanadyne injector. The purpose
of the calibration procedure was to quantify the mass of fuel delivered per injection at
different Fuel temperatures. The fuel temperature was measured just upstream of the
injector. In order to reduce the experimental test rnatrix to a manageable size, the injector
pulse width, opening pressure and fuel supply purnp rotationaI speed were set to constant
values. The pulse width was set with the Bosch fuel pump rack setting. The calibration
procedure was as follows:
1. Fuel was added to each of the IO L fuel reservoirs. They were not fiIled to capacity.
2. R e f e ~ n g to figure 5.3, mechanical valves #1,2 ,3 and 4 were opened.
Using toggle switch controlled solenoid valve #3, the small fuel reservoir was filled
(gravity fed), whiie carefully observing the fuel level through the fbel level window.
Mechanical valve #3 was then closed.
The digital scale was leveled to horizontal in order to ensure consistent readings. The
scale was leveted using a leveling bubble.
The pressure sensor bridge amplifier and the injector needle lift circuitry were tumed
on and allowed 20 minutes to warrn up.
The pump was then actuated with a toggle switch mounted on the front panel of the
fuel system. As shown schematically in figure 5.3, the eiectric pump drew the fuel
from reservoir # 1 , through the fuel filters and delivered fuel to the Bosch fuel pump
inlet. The 40 psig pressure relief valve allowed the fuel to divert to solenoid valve #2
and back to reservoir #1.
The Bosch fuel pump speed was set to 400 rpm.
The LabView calibration proprams were loaded. Explanations of the programs are
covered in Appendix B.
10. The desired calibration temperature was set on the temperature control unit. The fuel
injector continued to deliver fuel, while the heater was allowed I O minutes to bring
the fuel to a steady state set point temperature. The injection fuel temperature was
monitored with a separate LabView propram.
11. When the fuel temperature reached a constant value the pressure data acquisition
program was used to acquire one fuel line pressure trace at the start of each
calibration. The pressure was monitored for repeatability over the entire calibration
procedure but on1 y one trace was acquired for each temperature.
12. The initial mass reading on the digital scale was recorded.
13. The fuel temperature Nas recorded.
14. The lift sensor program was run with the number of injections set to 500. Relay
controlled solenoid valves # 1 and #2, actuated by the software, diverting fuel flow to
the mass measuring side of the fuel system. SoIenoid valve switching was
coordinated with the start of injection counts through the software. When the number
of injections reached 500 the software switched the valves back.
15. The final mass reading on the digital scale was recorded.
16. After approximately two or three sets of injections, the fuel collection flask
downstream of the injector was emptied.
Steps 12 to 16 were repeated 10 times at each temperature in order to ensure statistical
significance. At each temperature the fuel supply system was flushed and filled with
fresh fuel. The resultant data from these calibrations are listed in appendix 1. A figure
showin; the quantity of fuel delivered per injection as a function of temperature is listed
in the followinp chapter.
6.2. Experimental Procedure
Separate procedures and experimental setups were used to acquire photographs
and data during experimentation with the two fuel injectors. Similar data acquisition
schemes were used with the most significant difference being the triggering and timing
procedures discussed in the previous chapter.
6.2.1. Ford Fuel Injector Experimentation
The following procedure was carried out to acquire an image of an injection event
and to acquire data during that event.
1. The MAP sensor and the Nissan flowmeter power supplies were tumed on and given
tirne to warm up.
2. Power was supplied to the fuel injector control circuitry and the nitrogen flow control
relays.
3. The fuel level was checked in the fuel supply reservoir.
4. The fiber optic borescope was mounted in either the top or bottom view port.
5. The camera was loaded with film and mounted on to the motor driver.
6. The motor driver base was then mounted to the tripod.
7. The camera was connected to the borescope with the alignment adapter. Careful
alignment was necessary to ensure that stress was no? applied to the borescope body.
8. The flash un i t was connected to the carnera body.
9. The electric fuel pump was turned on and using the Ford injector calibration program.
the injector was pulsed 500 times to prime the system. While the injector pulsed, the
borescope was focused on the fuel spray. A small, high wattage light source was used
to illuminate the spray through the borescope light guide.
10. After the borescope was focused the light guide tip was repositioned directly in front
of the flash unit.
1 1. Motor driver power and the flash power were tumed on.
12. The Ford injector data acquisition program was loaded.
13. The start of injection was set to delay 83.0 ms from the camera irigger signal.
14. The injector pulse width was set to 18.0 ms.
15. A data filename was entered for data collection.
16. The nitrogen control switch was turned to the on position, setting up the desired
nitrogen flow through the experimental apparatus. A shon period of time was
a1Iowed for the flow to reach a steady velocity.
17. The electric fuel pump was tumed on to supply the injector with fuel.
18. The high wattage Iipht source was placed in front of the Rash unit Light detector and
the lights in the test ce11 were tumed off. The lipht source forced the flash unit to
produce the shortest flash duration possible.
19. The data acquisition program was run, capturing an image and acquinng data for a
single injection even t.
Step 19 was repeated 36 times utilizing an entire role of film for a given test condition.
6.2.2. Stanadyne Fuel Injector Experimentation
Steps 1 through 8 used to acquire data for the Ford injector experiment were the same
for the S tanadyne inj ector experiment.
The Schaevitz pressure transducer bridge amplifier was tumed on twenty minutes in
advance of use.
The electric fuel pump and the Bosch fuel pump were turned on to inject fuel and
prime the system.
The desired calibration temperature was set on the temperature control unit. The fuel
injector continued to deliver fuel, while the heater was allowed 10 minutes to bring
63
the fuel to a steady state set point temperature. The injection fuel temperature was
monitored wi th a separate LabView prograrn.
While the injector pulsed, the borescope was focused on the fuel spray. A small, high
wattage light source was used to illuminate the spray through the borescope light
guide.
After the borescope was focused the iight guide tip was repositioned directly in front
of the flash unit.
Motor driver power and the flash power were turned on.
The Stanadyne injector data acquisition prograrn was loaded.
A data filename was entered for data collection.
10. The nitropen control switch was turned to the on position, setting up the desired
nitrogen flow through the experimental apparatus. A short period of time was
allowed for the flow to reach a steady velocity.
1 1. The high wattage light source was placed in front of the flash unit light detector and
the lights in the test ce11 were turned off. The light source forced the flash unit to
produce the shortest flash duration possible.
12. The data acquisition program was mn, capturing an image and acquiring data for a
single injection event.
Step 12 was repeated a maximum of 36 times utilizing an entire role of film for a given
set of test conditions.
7. Results and Discussion
7.1, Overview
Expetiments have been conducted with fuel upstrearn of the injector nozzles
between roorn temperature and 220°C. Iso-octane was the fuel used for al1 experiments
in this study. A successful experiment resulted in: a photograph of the fuel spray as well
as rneasurernents of the fuel injection temperature, fuel injection pressure, fuel injector
body temperature, local cylinder head temperature, nitrogen flowrate and manifold
pressure.
Baseline testing was accomplished using a Ford production injector with fuel
upstream of the injector at room temperature. The fuel supply pressure for the Ford
injector was maintained at a constant 3.7 bar (39 psig). Testing with superheated fuel
was camed out using a modified Stanadyne diesel injector. Fuel injection temperatures
in a range from room temperature to 220°C were achieved with the Stanadyne injector
setup. Fuel supply pressure to the Stanadyne injector was acquired during
experimentation because it varied continuously throughout a given injection event.
The data acquisition process was triggered using different methods for each
injector but the data acquisition timing, number of data points acquired and the data
processing remained essentialiy the same. For each experirnental test point (fuel
injection photograph), 720 data points were acquired and processed for each signal. The
significance of acquiring 720 data points was that the DAQ program was deveioped to
function with an engine in the future and 720 data points would represent one data point
per CAD (crank angle degree) for one complete cycle. With a sampling rate of 1000
samples per second the entire acquisition would occur over 0.72 S. The Ford injector was
software controlled and only one injection occurred during each experimental cycle. The
S tanady ne injections were camshaft actuated and four injections would occur during the
0.72 s with image acquisition taking place during the first injection. The multiple
injections did not pose a problem because a11 acquired values were found to be constant
at each test condition (i.e. injection temperature) and did not Vary if acquired over a
separate set of injections. AH acquired values were averaged except for the Stanadyne
injector upstream pressure because this was the only value that was found to Vary with
tirne. Raw data for both sets of experiments can be found in appendix J. The average
data are organized in columns composed of thirty-six rows, one for each photograph.
Mean, standard deviation and 95.0% confidence intervals on these acquired averages
have been determined and are included at the end of each data set. The raw pressure data
for the Stanadyne injector have also been included in appendix J.
A total of approximately 360 experiments were camed out with the Ford injector
using both the bottom and the top view ports, where an experiment is considered to be the
acquisition of a single image and the corresponding data. Approximately 360
experiments were carried out with the Stanadyne injector over a temperature range from
room temperature to 230°C. Eight temperatures were chosen within this range and a
minimum of ten images and the correspondinp data were acquired at each temperature.
Images of the baseline Ford injector tests are presented in section 7.5. A sequence
of fuel spray photographs, produced with the Stanadyne injector at increasing
temperature, are also presented in section 7.5. A large number of fueI spray pictures were
acquired and from these the clearest typical images are presented. It should be noted that
the fuel sprays appeared to be very consistent at a given test condition and only the
quality of the photographs varied.
7.2. Ford Injector Experimental Data
Raw data for the baseline experiments are listed in Appendix J, tables J. I for the
data corresponding to the top view port image and J.2 for the data corresponding to the
bottom view port image. Plenum, upstream fuel, injector body and cylinder head
temperatures were found to remain constant at approximately 22, 22, 22 and 2I0C
respectively for the top view pon set of experiments. The manifold pressure remained at
a consistent 1 1 I kPa and the nitrogen flowrate was 9 13 sIpm. The temperatures acquired
durhg the bottom view port set of experirnents Iisted in the same order as above were 22,
22, 22 and 21°C respectively. The manifoId pressure was 11 1 kPa and the nitrogen
flowrüte was 966 slpm. An inconsistency in flowrate developed between the two sets of
experiments but was not considered to be a problem because different nitrogen flowrates
did not appear to strongly affect the injection process. The mass flowrate of fuel through
the Ford injector was deterrnined as described in Appendix D. The fuel injector delivered
0.038 g of fuel over an IS ms injection period.
7.3. Stanadyne Injector Experimental Data
Data for the high temperature fuel injection experiments has been listed in
Appendix J, tables 5.3 to J. 1 1 . The data has been orpanized in the same way as the low
temperature data acquired during the Ford injector experiments with measured spray cone
angles included in one additional column. The fuel spray cone angles were measured
from photographic prints. Fuel pressure upstream of the injector was also acquired
during each experiment and the data is included in table 1.12 of Appendix J. In some
cases a different number of experiments were carried out at each of the chosen upstream
fuel temperatures. A range from 7 to 38 experiments were run but this variation was not
considered to pose a problem because of the repeatability witnessed with the fuel spray at
a given temperature. In fact, repeatability testing was carried out when the system was
being debugpd and both photographic and visuai inspection showed consistency at each
temperature.
Figure 7.1 shows a typical injector pressure trace over the course of a single
injection event. The large peak indicates the lift pressure necessary to lift the pintle from
its seat. For the Stanadyne injections, image acquisition occurred at approximately 0.135
S. At 0.135 s the injection event was approximately 75 5% complete. The oscillations that
follow the large peak are thought to be reflected pressure waves rebounding between the
fuel pump plunger and the injector pintle. The peak pressure remained at a constant
value of 38 bar (540 psi@ for al1 experiments. The minimum fuel Iine pressure seerned
to be a function of temperature and varied from 12 bar (160 psig) to 14 bar (1 90 psig)
over the temperature range investigated.
- r
! - ! r
? t
- r - I
l , , , , , , , , , ! , , , , , , , I
, . I , . . , J . , . , .
O. 10 0.12 0.14 0.76 0.18 0.20 0.22 0.24
Time [s]
Figure 7.1 Fuel line pressure as a function of time.
7.4. Examining Experimental Test Conditions
The test conditions used dunng experimentation were chosen in an attempt to
reproduce a pon fuel injection event. The experirnents were designed to simplify the
environment into which the fuel is sprayed to a steady state system. A large number of
test variables were available and i t was necessary to fix as many of these as possible in
order to reduce the complexity of the experiment. Preheated fuel temperature just
upstream of the fuel injector nozzle was the test variable. In an attempt to achieve a
repeatable and meaningful experiment, al1 other test conditions that couid be controlled
were set to an appropriate value and held constant. Justification for the chosen test
conditions wilI become clear in the following sections.
7.4.1. Fuei-to-Air Equivalence Ratios
When the goals for the research were laid out, it was decided that cold engine start
conditions wouId be the focus. In order to start an engine under cold conditions the
combustion mixture m u t be enriched to compensate for fuel condensation losses and less
than optimum mixture preparation. This is accomplished by either extending the
injection times 1281 or under extreme conditions by double pulsing the injector 1291. For
this investigation, the Ford injector experiments were conducted at stoichiometric
equivalence ratios ($=1.0) and simulated wide-open throttle conditions where
equivalence ratio is calculated by dividing the measured fuel-to-air ratio by the
stoichiometric fuel-to-air ratio. This would be representative of a fuel delivery quantity
during cold starting if the injector was double pulsed. The Stanadyne injector system was
set up to deliver twice as much fuel as the Ford injector would for a single pulse since
double pulsing was nor possible. For both injectors, these fuel delivery strategies
represent an extreme condition that has been shown to exist in engines dunng cold start
W O I -
The amount of fuel delivered was of course controlled with a different method for
each of the two injectors. The fuel quantity deIivered for the Ford fuel injection
experiments was calculated based on a stoichiometric fuel-to-air ratio. The calculation to
determine fuel delivery quantity per injection for the Ford injector is included in section
G.2. of Appendix G. For the arnount of air delivered, an ideal gas assumption was used
to convert the volume per induction to a m a s of air per cycle. The stoichiometric ratio
was then used to determine the quantity of fuel required per cycle. With a required fuel
quantity of 0.037 ghjection, the injector cali bration equation developed earlier was used
to calculate an injector open duration or puise width of 18.0 ms. Typical pulse width
values Vary from approximately 2 to 20 ms over the engine load and speed range [3 11.
The 18.0 ms pulse width is representative of a wide-open throttle pulse width because
atmospheric pressure was chosen to calculate the inducted air volume. The injection
environment would be near atmospheric pressure only if the throttle was set to a wide-
open position. This was, in fact, the case during experimentation. The calculated pulse
width was implemented through software for the Ford injector.
The Stanadyne injector fuel deIivery quantity was controlled with the fuel pump
control rod setting. At room temperature the Stanadyne injector was found to deiiver
0.082 grarns of fuel per injection. Using 0.082 ginjection in conjunction with the fuel
density, the volume of fuel delivered per fuel pump stroke was approximately 120
cm3/stroke. Characteristic pump curves given in reference [32] provide a means of
detennining injection duration. With a volumetric delivery of 120 cm3/stroke and a fuel
pump speed of 400 rpm the injection duration was approxirnately 4.6 ms. This value was
also verified with the aid of the lift sensor and an oscilloscope. Therefore, the Stanadyne
injector was delivering twice as much fuel per injection in Iess than 113 of the time. In
fact 0.08 ghnjection corresponds to a fuel-to-air ratio of 0.14 gF/gA or an equivalence
ratio of 2.0 which is well above stoichiometric proportions but representative of a cold
start condition.
The important quantity for comparison is the fuel quantity delivered by the
injectors. It has already been shown that the Ford injector expenments were run with
approximately stoichiometric equivalence ratios. Higher equivalence ratios, achieved
with longer injection pulse widths, were tested and did not appear to change the nature of
the fuel spray. The high temperature expenments were run at an equivaience ratio of
approximately 2.0 because this value represents a bound on the equivalence ratio used for
enrichment purposes during engine cold starting conditions.
7.4.2. Nitrogen Volumetric Flowrate
Since the experimental apparatus was a steady flow system, calculations were
made to approximate the voiumetric flow past the injector at a simulated engine speed of
1000 rpm. The calculation for voiumetric flowrate is provided in section G.I. of
Appendix G. A volurnetric efficiency value of 0.85 was chosen based on typical values
listed in reference [3 I l . The single cylinder volume for the test engine was 0.475 L and
is inducted once every 2 crankshaft revolutions for a time duration equal to the intake
valve open duration. This calculation results in an average voiumetric flowrate during
the intake valve actuation period (opening and closing) in an actual engine.
Instantaneous values would be Iarper corresponding to the maximum piston velocity in a
fully functional engine [3 11. The actual value achieved with the nitrogen supply system
during experirnentation was approximately 940 slpm, which corresponds to an engine
speed of 970 rpm. The flowrate values measured during each set of experirnents (i.e. at a
given fuel preheat condition) appeared to be quite steady. The average flowrate values
were found to be within +/- 4 slpm of the mean flowrate value (with 95.0% confidence)
for al1 but two sets of experiments. The confidence intervals were larger for the
experiments carried out at fuel injection temperatures of 80°C and 125°C because there
was one high flowrate measured dunng each of these experimental sets. These variations
can be attributed to the finite time taken by the nitrogen fiow system to achieve a steady
flow condition. When the nitrogen system was turned on, initial flowrate values were
high and then the system would drop down to a steady value. The large fiowrate readings
probably occurred when the system was still corning to a steady state condition. Care
was taken to choose a picture where the flowrate did not Vary substantially from the mean
value.
Once a flowrate was established the values were quite constant, however, some
fluctuations in flowrate were observed to occur between sets of experirnents. The
measured flowrates were observed to be between 893 sIpm and 967 slpm for al1 the
experimental data sets however these values represent two extremes with most of the
measured values between 940 slpm and 960 slpm. The one extremely low value may be
due to a low supply Iine pressure. At the desired flowrates the nitrogen cylinders were
emptied quickly and this may explain the one relatively low value. This is not interpreted
to present a problem because the nitrogen flow did seem to strongly affect any of the fuel
sprays captured in the photographs.
7.4.3. Examining Fuel Injection Pressures
Fuel supply pressure just upstream of the injector is an important quantity to
charactenze the injection process. As discussed in chapter 5, the Ford injection pressure
was maintained using a stock Ford fuel rail arrangement. The pressure regulator
maintained the supply of fuel to the injector at 3.7 bar absolute pressure (39 psig)
resulting in a pressure differential across the injector nozzle of 2.6 bar just pior to
injection.
As discussed in chapter 5, a Bosch fuel pump was used to provide fuel to the
Stanadyne injector at a pressure high enough to invoke the needle lift. The fuel pressure
developed upstream of the Stanadyne nozzle is depicted in figure 7.1. The pressure
required to lift the injector needle from its seat wzs 38 bar (540 psig). This pressure
remained constant within +/- 5 psig for each set of experiments. Taking the measured
manifold pressure into account, the pressure differential across the nozzIe just prior to the
injection was 37 bar. The change in fuel pressure upstream of the nozzle during a single
injection event was measured to be a maximum of approximately 26 bar. This value was
lower at higher temperatures due to increasing fuel line minimum pressures with
temperature. The minimum line pressure was thought to increase because of the imposed
increase in fuel temperature. Increasing the fuel temperature descreases the fuel density
leading to an increase in line pressure. The fuel temperature increase was, of course,
primarily due to the imposed heat from the heater systern but secondary heating was aIso
witnessed to occur when the heater was tumed off. This secondary heating (24°C) was
most likely due to frictional heat dissipation in the fuel supply pump and was not found to
change the fuel line pressure characteristics. The maximum fuel line pressure (the
injector lift pressure) remained the sarne with increasing fuel temperature because this
value is not a function of themodynamic properties but is simply based on the chosen
fuel injector mechanical settings.
Having discussed the pressures measured upstream of the nozzle for each injector,
it is clear that the injectors operate under different pressure conditions. The Ford injector
was the baseline experiment to illustrate the inadequacies of the injector spray. The
Stanadyne injector experiments were then carried out from room temperature up to 220°C
to illustrate fuel spray improvements beyond the Ford injector spray.
7.4.4. Stanadyne Injector Fuel Delivery at Elevated Temperatures
It was necessary to quantify the injector fuel delivery at elevated temperatures
because it could be expected to change relative to the low ternperamre calibration. A
method to characterize the Stanadyne injector m a s flowrate was developed and carrïed
out as described in the Experimental Procedure chapter. Fuel delivery measurements
were made at the corresponding test temperatures to determine if the quantity of fuel
delivered was dependent on temperature. Ten sets of 500 injections were canied out at
each test temperature to accurately quantify fuel delivery. Figure 7.2 shows a summary
of the results obtained from the injector calibration experiments with mass flow quantity
plottea versus reduced ternperature, where reduced ternperature is defined as the ratio of
the upstream injection temperature to the critical temperature of the fuet. Raw data from
the calibrations has been included in Appendix I with a calculation of 95.0% confidence
intervals on the mass of fuel delivered per injection. The quantity of fuel delivered per
injection for this set of experiments did not exhibit a strong dependency on temperature
as shown in the figure. The fuel quantity was approximately 0.083 ghjection, however,
a statistically significant but small increase in mass flow quantity was witnessed over the
experimental temperature range. Statistical significance was determined based on the
overall increase in mass delivered (0.002 ginjection) compared to the 95.0% confidence
intervals (+/- 0.0006 ghnjection on the mean).
It was anticipated that the mass of fuel delivered would remain approximately
constant with increasing fuel temperature because the pressure required to lift the injector
needle remained constant. A slight increase in delivered mass per injection was
measured for the temperature range investigated. With a temperature change from 0.55
Tc to 0.87 Tc an increase from 0.082 to 0.083 gram per injection was measured which
corresponds to an increase of approximately 1.0%. Statistically this quantity was
determined to be significant and there are a number of factors that could explain this
increase. The injection pressure traces were individually checked and although the peak
pressures remained constant the average pressure during the injection duration increased
slightly with temperature. The increase may be due to fuel property changes at elevated
temperature. As the fuel temperature was increased the minimum fuel supply pressure
increased therefore requirïng the pump to produce less of a pressure increase for an
injection to occur. One possible explanation can be drawn from the way in which Bosch
injection pump operates. If the required developing pressure decreases, more cam travel
is available to produce fuel flow and the flow will occur at a higher average delivery
pressure. A second factor that rnay be involved is fuel viscosity decreases with
temperature. As the viscosity decreases, the fuel flow rate through the nozzle will
increase although the injection duration may shorten and counter balance this flow
increase. More expenmentation specifically designed to investigate the fuel deiivery
system would be necessary to conclusively determine the fuel delivery dependence on
upstream temperature. The measured increase is quite small and is presurnably
insignificant with respect to the focus of this study.
Figure 7.2 Mass flowrate as a function of temperature.
7.4.5. Examining Manifold Pressure and Secondary Temperatures
Manifold absolute pressure (MAP) rneasurements were made for al1 of the
experimental tests. The manifold pressure values were found to remain quite constant
during each test and between each set of experiments. Over a11 the experiments the
minimum mean pressure measured was 110 kPa and the maximum was 1 1 1 kPa. The
maximum 95.0% confidence interval on a mean rneasurernent was found to be 0.2 kPa.
The measured pressures were found to be slightly higher than the atmospheric value used
to calculate injector pulse widths. This was probably due to minor flow restrictions
downstream from the pressure measuring point in the steady flow system. Modifying the
calculation for an average manifold pressure of 110 kE% increases the pulse width by less
than 1 ms and pulse width was already conchded to have very little effect on the
acquired images.
The remaining measured temperatures include plenum nitrogen temperature,
injector body temperature and local cylinder head temperature. Al1 measured
temperatures appeared to stay consistent throughout each set of experimen ts. Variation
in the measured nitrogen temperature that occurred between sets of experiments can be
attributed to changes in ambient conditions. The minimum mean measured nitrogen
temperature was 22°C and the maximum was 24°C for al1 sets expenments. The injector
body temperature appeared to increase with increasinp preheated injection temperatures.
The injector body was not insulated and a temperature differential between the fuel
temperature and injector body temperature developed during each experiment. With fuel
temperature of 80°C the injector body temperature was measured to be 49°C and at the
highest levels of preheat the injector body reached a temperature of 105°C. Local
cyIinder head temperatures also followed the injected fuel temperature increases as was
expected. The local cylinder head temperature measurement was made where the fuel
impinges on the port wall. The temperature reached a maximum of 36°C which
represents a temperature increase of approximately 1 6°C.
This acquired data was of secondary importance compared to the fuel injection
upstream temperature and pressure measurements. The secondary data, overall, appears
to be representative of steady state conditions which was the objective.
7.5. Examining the Fuel Spray Images
The test conditions summarized above were average values over the entire set of
experiments. The data corresponding to each photograph has been included in Appendix
J. Figure 7.3 shows the results of baseline testing with the Ford fuel injector. Figure
7.3(a) shows a fuel injection from the top view port. The highly reflective surface at the
edge of the photograph is the machined entry into the intake port. In the background of
the photograph the intake valve stem and the seat are visible. It should be noted that the
top of the valve stem is tilted slightly towards the view port. The fuel spray can be seen
in the center of the picture with liquid droplets moving from right to left across the
borescope field of view. Figure 7.4 is a schematic diagram of the image, which has been
included to further describe the fuel spray. In figure 7.3(a) the liquid droplets appear
mainly as streaks across the field of view because the exposure time (flash duration) was
not short enough to completely stop the liquid droplet motion. Large variations in droplet
size can be observed from the image with liquid fuel concentration near the center-line of
the spray. The spray appears to be a relatively thin stream compared to the size of the
intake port. To pive the fuel spray scale, the intake valve stem diameter is 8 mm and
looks to have a diameter similar to the fuel spray. The valve stem could not be used to
accurately measure the fuel spray geometry because it in not in the sarne pIane as the fuel
spray.
Figure 7.3(b) shows the fuel injection event from the bottom view-port. Figure
7.5 is a schematic diagram that has been included to aid in the explanation of figure
7.3(b). From the bottom view port, the fuel injector is perpendicular to the field of view
and fuel motion is from left to right as shown in figure 7.5. The liquid fuel stream
appears to be a thin jet with a very smdl cone angle. In fact, the Iiquid fuel Stream does
not appear to expand very much in diameter above the exit diameter of the nozzle.
Noticeable expansion of the spray can be seen to occur between the two view-ports. The
top view port was located approximately 50 mm downstream from the bottom view pon.
Figure 7.3 Ford injector fuel injections at rocjrn temperature shown from: a) the top view port and b) the bottom view port.
intake valve stem
approximate fuel spray b oundar y
valve seat
borescope field of view
Figure 7.4 Schematic diagram illustrating a fuel spray captured in the top view port.
machined surface
approximate / I fuel spray i
1 I
boundary
1 Ford injector exit flush with surface
borescope field of view
Figure 7.5 Schematic diagram illustrating a fuel spray captured in the bottom view port,
The transition from a cold liquid fuel spray to flashing flows is illustrated in
Figure 7.6(a) to (0 with sprays produced by the Stanadyne injector. Plenum temperature,
injected fuel temperature, injector body temperature, cylinder head temperature, manifold
pressure and nitrogen flowrate values have been averaged over the entire set of
experiments at each temperature and are summarized in table 7.1.
Table 7.1 Mean data corresponding to figure 7.6.
Figure Label
1 . , I I 1 - -
I
Note: AI1 temperatures are listed in Celsius.
7.6(a) 7.6(b) 7.6(c)
The precise values corresponding to the chosen photographs are included in Appendix J
Plenum Temp.
and are closely represented by the values listed above. Figure 7.7 is a schematic diagram
23 22 23
illustrating some of the major points that are visible in the photographs. In al1 the
Injected Fuel
photographs included in figure 7.6, the injector body sits in the center of the picture
Temp. 25 80 125
surrounded by the lower intake runner surface, which is slightly out of focus. The
Injector Body
surface appears dark with reflective spots, which is simply the roughness due to casting
Temp. 24 49 68
of the part. The target for focusing the images during experimentation was rnidway
Cylinder Head
between the base of the spray at the injector exit and the end of the visible spray. In
Temp. 19 23 28
general, this area looks clear in each of the photographs. The injector body appears to be
Manifold Pressure
reflecting some light back to the Dorescope tip in all of the photographs. The injector
Nitrogen FIowrate
[ k W 110 I l 0 110
body was a mildly polished surface and seerned to collect a liquid film near the tip,
b lpm] 92 1 950 893
producing a reflection. The fuel jet issuing from the injector tip appears as a dense white
spray with fluid movement from left to right in each of the pictures. Fuel droplets are not
distinguishable in any of the pictures due to the limitations of the photographie imaging
system, however, useful information about the jet shape and cone angIe can still be
determined. In al1 the acquired images the fuel spray appears to be centered slightly off
the axis of the injector due to a small machining flaw in the injector tip modification.
Figure 7.6 Fuel injection through the Sianadyne injector shown from the bottom view port location at increasing upstream temperature: a ) 35°C (0.55 Tc), b) 80°C (0.65 Tc) ..
Figure 7.6 continued. Fuel injection through the Stanadyne injector s h o w from the bottom view port location at increasing upstream temperature: c) 125°C (0.73 Tc), d) 142°C (0.76 Tc).
Figure 7.6 continued. Fuel injection through the Stanadyne injector shown frorn the bottom view port location at
increasing upstream temperature: e) 174OC (0.82 Tc), f) 207°C (0.88 Tc).
approximate fuel spray boundary
Stanadyne inj ector exit
Figure 7.7 Schematic diagram illustrating a fuel spray captured in the bottom view port.
Since this appears to be present in a11 of the photographs it is not deemed to introduce
significant problems to the resuIt however a small error may result in measurements
taken from the images. It should also be noted that the orientations of the pictures are not
precisely the same in each case due to the need for occasional borescope tip cleaning and
realignment.
The fïrst two photographs in the series (figure 7.6) show fuel being injected at
35°C and 80°C. Figures 7.6(a) can be used as the cornparison case for the rest of the
photographs in the series. There does not appear to be significant change in the spray
appearance between figures 7.6(a) to (c). When the temperature was increase beyond
1 Q°C the fuel spray cone angle appeared to increase with increasing temperature.
7.6. Liquid to Liquid Injections
Both the Ford fuel injector and the Stanadyne fuel injector were used to inject
1 iquid fuel at arnbient temperatures. Two injectors were required because heating the
Ford injector to the desired temperatures was not a feasible option as discussed earlier.
Stanadyne injector experiments were carried out at room temperature in order to illustrate
how closely the fuel spray it produces resembles the Ford injector spray. Experiments
using the stock Ford injector were camed out to show the inadequacy of the fuel spray
that it produces.
Figure 7.3 shows fuel injections through the Ford injector from the top and
bottom view ports. Figure 7.3(b) illustrates the nature of a fuel injection event in a
typical port injection application. The liquid fuel exits from the nozzle in a very thin
cylindrical stream with no measurable cone angle. Figure 7.3(a) shows the spray under
the same conditions. Although the fuel droplets are rnoving too quickly to be captured by
the photographie system, large droplet streaks can be seen in the picture. The injected
fueI travels 50 mm between the two view ports, but this distance does not appear to be
long enough for the fuel spray to develop. The increase in the fuel spray cone angle
between the two view ports can be attnbuted to mechanical break up of the liquid stream
due to injector geometry and to aerodynamic effects produced by the high speed nitrogen
flow in the port.
Figure 7.6(a) shows a fuel spray produced by the Stanadyne injector with a
measured fuel temperature upstream of the injector of 25°C. Comparing this fuel
injection image to the fuel spray produced by the Ford injector depicted in figure 7.3(a),
it is clear that the Stanadyne injector induces a slightly larger amount of liquid fuel
atomization than the Ford injector. Exactly reproducing the ambient temperature Ford
injector fuel spray with the Stanadyne injector was not realistic. However, the
photographs show that the baseline tests carried out with the Ford injector are quite
comparable to the baseline tests carried out with the Stanadyne injector.
The Ford injector does not appear to create a finely atornized spray but instead
produces a spray with large variations in droplet size. This type of spray is not ideal for
fuel preparation because it Ieads to significant and localized wall wetting.
7.7. Preheated Fuel Flow through the Stanadyne Injector
The series of injections in figure 7.6 shows the transition from hydrodynamic and
instability controlled flow to a regime where thermal effects dominate. The performance
of any given type of atomizer depends on its size and geometry and on the physical
properties of the liquid being atomized [33]. Secondary atomization that occurs after the
liquid exits the nozzle is a function of the gaseous medium into which the liquid is
discharged. The modified Stanadyne diesel injector is a pressure atomizing injector. The
fuel spray break up and development is due prirnarily to the geometry of the injector at
low temperatures. The liquid fuel is discharged through a srnaIl aperture under relatively
high pressure and the pressure energy is converted to kinetic energy.
The first two photographs in the series (figure 7.6) show fuel being injected at
25°C and 80°C. This is often referred to as a liquid-to-liquid injection because no
flashing can occur at these temperatures. Only mechanical fuel break up induced by the
injector geometry occurs at the nozzle exit. The normal boiling point for iso-octane is
9g°C so as the fuel undergoes a pressure drop from the fuel line pressure to the manifold
pressure, injections at temperatures of less than approximately 9g°C do not cross the
liquid saturation boundary. There doesn't appear to be significant change in the spray
appearance between figures 7.6(a) to (c) aithough the fuel temperature increases by
100°C. A further fuel temperature increase of 17OC appeared to change the physical
appearance of the fuel spray quite significantly. The spray seemed to spread out with a
greatly increased cone angle at 142°C compared to the first three experirnental
temperanires. Further increases in cone angle can be seen to occur as the temperature
was increased to a maximum of 207OC. In addition to cone angle increases, the outer
edges of the spray seem to be more strongly affected by the nitropen flow at higher
temperatures. The fuel spray nearer to the right side of the borescope field of view looks
to be approaching a more cylindrical arrangement rather than an expanding conical
arrangement as it does at lower temperatures.
Injections at preheat values of less than 0.73 Tc are though to be prima-ily
controlled by hydrodynamic forces and instabilities produced by the injector geometry.
Above this superheat level, the thermodynamic mechanisms begin to take over. The
transition is quite clearly indicated in figure 7.8 where a sharp transition in spray cone
angle occurs at 0.73 Tc for the iso-octane data acquired during experimentation with the
Stanadyne injector. Spray cone angle was referred to in a qualitative sense in the above
descriptions of figure 7.6. An atternpt was made to measure the spray cone angle at each
of the test temperatures to obtain a more meaningfül quantitative value. For each set of
experiments, two photographs were enlarged to make accurate cone angle measurements.
The best photographs, with respect to image quality, were chosen from the contact sheets
for each data set and cone angle measurernents were taken. Further, although less
accurate, measurernents were made from the negatives in order to increase the sample
size for each cone angle value. Cone angle data has been listed with the corresponding
data set in Appendix J with an asterisk beside the measurements taken from enIarged
photographs. AI1 other cone angle values are measurernents made from the negatives.
No detectable discrepancies were found between the cone angles rneasured from the
enlarged photographs and those measured from the negatives. It should be noted that
cone angle measurements required a subjective choice of the outer fuel spray boundary.
Figure 7.8 is a plot of cone angle in degrees versus reduced temperature. Additional data
has been included on in figure 7.8 to aid in the comparison of the results to the
preliminary experiments and to work by other authors. The maximum reduced
temperature shown on the plot is 0.9 1. The value 0.9 1 Tc represents a physical limitation
in the apparatus, above which, liquid fuel wiIl begin to boil in the line. The figure
indicates a slight increase in cone angle up to a reduced temperature of 0.73 for iso-
octane injections using the Stanadyne injecter. From 0.73 Tc to 0.76 Tc there appears to
be a rapid increase in cone angle from approximately 3 4 O to 8O0, although further testing
would be necessary to conclusively comment on this trend. From a reduced temperature
of 0.76 to 0.91 the cone angle increase appears to be approximately linear from 80° to
115". The fuel spray cone angles increase and from the photograph in figure 7.6 the
penetration distance seems to shorten as upstream temperature increases.
Figure 7.8 Cone angIe as a function of reduced temperature. + Iso-octane fuel injection data through the Stanadyne injecotor. o Iso-octane fuel injection data from the preliminary experiments. Sloss dodecane fuel injection data.
A similar transition location of approximately 0.75 Tc was observed in an
expenment with a converging nozzle by Sloss [23] and Athans [34] and was further
substantiated dunng the preliminary experirnental work carried out in this study. As
shown in figure 7.8, data corresponding to the injection of dodecane through a
converging nozzle carried out by SIoss has a similar upper cone angle limit of 120° and a
similar abrupt increase in cone angle at a comparable reduced temperature. In fact,
similar experiments carried out by Sloss using kerosene and diesel fuel exhibited a
similar cone angle transition point of 0.75 Tc. Although only two cone angle
rneasurements can be obtained from the preliminary iso-octane experiments carried out
during this study, they more closeIy represent the test conditions used by Sloss and
therefore have been included in figure 7.8 to aid in the cornparison of the data. It is
interesting that the cone angIe rneasuremen ts obtained from the S tanadyne injector
experiments exhibit similar trends as the dodecane experiments camed out by Sloss even
though there were so many differences in experimental conditions. The reduced pressure,
measured upstream of the nozzle, corresponding to the Stanadyne injector experiments
was 1.5, while Sloss used 0.5. The fuel type was different, the nozzle geometnes were
different and the Stanadyne injector experiments produced intermittent sprays while the
apparatus developed by S loss produced a continuous spray.
As discussed in the Theory chapter, Jakob number is a measure of superheat.
Instead of using reduced temperature, Figure 7.6 could also be descnbed in terms of
Jakob number. The corresponding Jakob numbers for figures 7.6(a) to (0 are 0.00, 0.00,
0.23, 0.40, 0.74 and 1.1 1. A table of Jakob numbers and the corresponding fuel
temperatures are listed in Appendix H. The Jakob numbers are calculated using upstream
temperature and a downstream pressure of I atm to characterize a given fuel spray. The
images indicate that a Jakob nurnber significantly greater than zero must be reached
before flashing occurs. To more accurately comment on the transition, finer increases in
experimental temperatures wouId be required.
Bubble nucleation and growth are responsible for the transition to a flashing type
jet. Heterogeneous nucleation requires less energy than homogeneous nucleation and is
most likely the mechanism responsible for bubble formation. Heterogeneous nucleation
sites usuaIly exist at the interface between the metastable phase and another phase, either
liquid or solid and it is unclear whether nucleation is beginning inside the injector or just
downstream from the nozzle. Further expansion of the jet with increasing temperature
was presumably due to the increased number of critical nuclei at increasing Ievels of
superheat.
Figures 4.2 and 4.3 show the progression of a liquid jet frorn a thin stream
breaking up due to aerodynamic forces to fuel jets that are breaking up more due to
thermodynamic mechanisms. This is an interesting observation because the Stanadyne
injector appears to impose substantially more rnechanical fuel break up than the nozzle
used in the preliminary experimentation. This implies that the critical superheat value
may be independent of the mechanical fuel break up imposed by the injector geometry.
Clearly, further research is necessary to substantiate this observation but the fact remains
that increased atomization was obtained with increasing levels of preheat.
Before implementing a fuel preheating system in a practical application such as a
port injected engine, an understanding of the energy requirements is a necessary first
step. The Jakob number is essentially the ratio of the superheat energy divided by the
heat of vaporization of the fuel. The highest level of superheat achieved in the present
study was a Jakob number of 1.1 1. Multiplying the Jakob number by the heat of
vaporization of the fuel ana dividing by the lower heating value of the fuel, a crude
estimate of the preheating system enegy requirements can be obtained. The heat of
vaporization for iso-octane at 1 bar is approximately 308 KT/kg. The lower heating value
for iso-octane, which is essentialiy the chemical input energy to an engine, is
approxirnately 44 MJ/kg. This implies that the preheating process requires less than 1 %
of the chemical energy that the fuel is capable of delivering. Thus, the proposed
preheating techniques may be feasible in a functional port injected engine.
8. Conciusions and Recommendations
In this research, the effects of preheating liquid fuel prior to injection has been
studied as a means of improving fuel spray charactenstics in a multi port fuel injected
engine configuration. Useful conclusions can be drawn from the results obtained during
experimentation and from the expenence gained during instrumentation. Single shot 35
mm photography in conjunction with a fiber optic borescope was used to capture the fuel
injection events at two different view port locations. Research grade iso-octane, a pure
hydrocarbon, was injected through a Ford fuel injector at ambient temperatures and
throuph a Stanadyne injector over a range of temperatures from arnbient to 220°C.
The Ford injector appeared to produce a spray that is considered inadequate for
cold engine stan conditions. Poor fuel atomization was observed from the injector, which
illustrates a need for improvement over the present port injection technology.
The possibility for irnprovement was shown to exist with the implementation of
preheating techniques and the modified injector. As the fuel was preheated above
approximately 0.73 Tc, there appeared to be a sharp increase in spray cone angle and
shortened penetration distance indicating increased fuel atomization. Fuel spray break up
at temperatures less than 0.73 Tc is due to a combination of injector geornetry effects and
aerodynamic effects produced by the high speed nitrogen flow. Further fuel spray break
up and development at temperatures above 0.73 Tc is due primanly to thermal effects
superimposed on the physical break up mechanisms. This improvement in fuel spray
characteristics during cold engine start up conditions could prove to be extrernely
beneficial in improving fuei-to-air ratio control and in reducing HC emissions.
To continue this project the next logical step would be to convert the steady flow
system to a fully functional single cylinder engine. A number of me necessary steps for
the conversion have been completed in the development of the present study. A similar
test matrix could be designed and both motored and eventuaily fired engine testing could
be camed out. Improvement of the image acquisition system would allow droplet size
measurements and therefore a more quantitative discussion of fuel atomization
improvements. Under fired engine conditions, engine power testing and HC emissions
testing in addition to fuel spray image acquisition would prove to be a valuable tool in
further verifying the hypotheses laid out in the present work.
References
1. Fox, J.W., Min, K.D., Cheng, W.K. and Heywood, J.B. "Mixture Preparation in a SI Engine with Port FueI Injection During Starting and Warm-Up." SAE Paper No. 922 170, 1992.
2. Carey, V.P. Liquid-Vapor Phase Change Phenomena. Hernisphere Publishing Corporation, U.S.A., 1992.
3. Oza, R.D. and Sinnamon, J.F. "An Experimental and AnaiyticaI Study of Flash Boiling Fuel Injection." SAE Paper No. 830590, 1983.
4. Brown, Ralph and York, Louis J. "Sprays Formed by Flashing Liquid Jets." A.1.Ch.E. Joumal, 1962, pg. 149- 153.
5. Oza, R.D. "On the Mechanism of Fiashing Injection of Initially Sub-cooled Fuels." Vol. 106/105, March 1984.
6. Plesset, M.S., and Zwick, S.A. "The Growth of Vapour BubbIes in Superheated Liquids." Joumal of Applied Physics, Vol. 25, No.4, 1954, pg.492-500.
7. Cheng, Chun-On, Cheng, Wai K. and Heywood, John B. "Intake Port Phenomena in a Spark-Ignition Enpine at Part Load." SAE Paper No. 9 1240 1, 199 1.
8. Shin, Younggy, Cheng, Wai K. and Heywood. John B. "Liquid Gasoline Behavior on the Engine Cylinder of a SI Engine." SAE Paper No. 941872, 1994.
9. Meyer, R. and Heywood, J.B. "Liquid Fuel Transport Mechanisms into the Cylinder of a Firing Port-Injected SI Engine During Start Up." SAE Paper No. 970865, 1997.
lO.Shin, Younggy, Min, Kyoungdoug and Cheng,Wai K. "Visualization of Mixture Preparation in a Port Fuel Injection Engine During Engine Wann-up." SAE Paper No. 95248 1, 1995.
1 l.Cheng, Wai K., Hamrin, Douglas, Heywood, John B., Hochgreb, Simone, Min, Kyoungdoug and Norris, Michael. "An Overview of Hydrocarbon Ernissions Mechanisms in Spark-Ignition Engines." SAE Paper No. 932708, 1993.
12.Glockler, Otto, Knapp, Heinrich and Manger, Hansjorg. "Present S tatus and Future Development of Gasoline Fuel Injection Systems for Passenger Cars." SAE No. 800467, 1980.
13.Galliot, F, Cheng, W.K., Cheng, C., Szetenderowicz, M. and Heywood, J.B. "In Cylinder Measurements of Residual Gas Concentration in a Spark Ignition Engine." SAE Paper No. 900485, 1990.
14.Aquin0, Charles and Plensdorf, William D. "An Evaluation of Local Heating as a Means of FueI Evaporation for Gasoline Engines." SAE Paper No. 860246, 1986.
lS.Boyle, R.J., Boam, D.J. and Finlay LC. "Cold Start Performance of an Automotive Engine Using Prevaponzed Gasoline." SAE Paper No. 9307 10, 1993.
16.Berg, Peter G. "Cold Weather Diesel Fuel Preparation with PTC Heaters." SAE Paper No. 840539, 1984.
17.Chen, f .L. and Chen, Grant "Slow Heating Process of a Heated Pintle-Type GasoIine FueI Injector." SAE Paper No. 950068, 1995.
18.Williams, Paul and Beckwith, Paul. ''The Effect of Fuel Composition and Manifold Conditions Upon Spray Formation from an SI Engine Pintle Injector." SAE Paper No. 94 f 865, 1994.
19.Sait0, Kirnitaka, Sekiguchi, Kiyonori, Imatake, Nobuo, Takeda, Keiso and Yaegashi, Takeda. "A New Method to Analyze Fuel Behavior in a Spark Ignition Engine." SAE Paper No. 950044, 1995.
20.Yang, Jilian, Kaiser Edward W., Siegel, Walter 0. and Anderson, Richard W. "Effects of Port-Injection Timing and Fuel Droplet Size on Total and Speciated Exhaust Hydrocarbon Emissions." SAE Paper No. 9307 1 1, 1993.
21.Shayler, P.J., Davies, M.T., Coiechin, M.J.F. and Scarisbrick, A. "Intake Port Fuel Transport and Emissions: The Influence of Injector Type and Fuel Consumption." SAE Paper No. 961996, 1996.
22.Che1-1, Gang, Vincent, Michael T. and Gutermuth, Terry R. "The Behaviour of MuItiphase Fuel-Fiow in the Intake Port." SAE Paper No. 940445, 1994.
23.Sloss7 Clayton. "Experimental Smdy of Preheated Fuel Injection through a Nozzle." Masters Thesis, University of Toronto, Toronto, Canada, 1996.
24.Vesik, W.H. "A Thermodynamic Analysis of Evaporation Waves in an Expanding Jet." Masters Thesis, University of Toronto, Toronto, Canada, 1997.
25.Kessler, C . Personal Communications, unpublished, 1998.
26.Beha.r, E., Simonet, R. and Rauzy, E. "A New Non-cubic Equation of State." Fluid Phase Equilibria, Vol. 2 1,237-255, 1985.
27.Julian, S., Barreau, A., Behar, E. and Vidal, J. "Application of the SBR Equation of State to High Molecular Weight Hydrocarbons." Chernical Engineering Science, Vol. 44, NO. 4, 1004-1006, 1989.
28.Lenz, P. Mixture Formation in Spark-Ignition Engines. SAE Inc., 1992.
29.Probst, C.O. How to Understand, Service and Modifv Ford Fuel Iniection and EIectronic Engine Control. Robert Bentley hc., 1993.
30.Quader, A.A. "Single-Cylinder Engine FaciIity to Study Cold Starting-Results with Propane and Gasoline." SAE Paper No. 92000 1, 1992.
3 1 .Heywood, I.B. Intemal Combustion Engine Fundamentals, McGraw-Hill, 1 988.
32.Robert Bosch. PF Fuel Injection Purnps. GMBH Sttuttgart.
33.LefebvreT A.H. Atomization and Sprays. Hemisphere Pub
34.Athans, R.E. "The Rapid Expansion of a Near-Critica Thesis, Rensselaer Polytechnic Institute, Troy, NY, 1992.
lishing Corporation, 1989.
.1 Retrograde FIuid." PhD
35.Reid, R.C., Prausnitz, J.M. and Poling, B.E. The Properties of Gases and Liquids. 4'h ed. McGraw-Hill Book Company, Toronto, 1987.
36.1995 SAE Handbook. Gasoline Fuel Injector SAE J 1832 Nov89, vol.2, pg.26.265.
A. Fuel Data
Table A. 1 Listing of fuel properties [35].
Fuel Parameter iso-Octane (CsH 18)
(2,2,4 Trimethylpentane, (CH3)3CCHgH(CH3)~)
Omega
p [gml @ 25"C]
0.303
0.668
B. LabView Virtual Instruments
B.1. Ford Fuel Injector Calibration Program
The program used to calibrate the Ford injector controlled pulses to the injector
and the fuel measurement system. The front panel for this program is shown in figure
B.1 and the back panel is shown in figure B.2. The number of pulses, pulse frequency,
duty cycle and fuel system relay control (off/on switch) were used as inputs to the
Relay Actuation OFF - - ON 1
. . . . . .................
< F I > to stop -2 1
'OFFI S T O P 1
d ~ t y cycle (0.5) i fjo.so!
- - - - - - -
numb;r-of pulses (cont:O)
:I5 O---
lnjector Operation Time ( s ) ]
2 .50 -1
lnjector Open Time (s) .-
1.25 l
pulse polarity (high:O)
$ high pulse I[c gate mode ( u r q a t e d : ~ ) - _"_1_1___ --- --P.".".- - , $ ungatedlsoftware start ][O
. - -- - - -
(tasklD of counter] 1 &-000001
1 l
ac tua l ara met ers
1
pulse widthl
10.00003 . - - A - - . - - - -- 1 12.50
Figure B. 1 Ford fuel injector calibration program front panel.
. . - .
1- [ninjeîtor o p e n Tirne ( r ) ]
l n h c t o r Operalion Time (s)/ :=
Figure B.2 Ford fuel injector calibration program back panel.
B.2. Stanadyne Fuel Injector Calibration Programs
Three different VIS were devetoped to calibrate the Stanadyne injector. The main
VI was used to count injections frorn a signal produced by the lift sensor and control the
fuel measurement system. Figure B.3 shows the front panel and figure B.4 shows the
back panel of the VI. To acquire fuel line supply pressure data just upstream of the
injector, a separate VI was developed. The pressure acquisition VI saved data to a file
and allowed sample rate and sarnple number inputs. The pressure trace was also
displayed on a plot on the front panel. Figures B.5 and B.6 show the front and back
panel respectively. The third program was used to rnonitor injection temperature just
upstream of the injector.
- - - . .. - Relay Actuation off on I over f low?
Figure B.3 Stanadyne fuel injector calibration program front panel.
, .. .
Figure B.4 Stanadyne fuel injector caiibration program back panel.
- - - number of s a m ~ l e s l
Wrile t o - ~ G e file path (dialog i f empty)]
3 / c : \~ i ke \Da ta \~a i i b ra t i on \~ ressu re \ 5 9 8 ~ 8 ~ 1 apressure -- ---
-- -- - -- -. - -- -- -.-
new file path (Not A Path i f cancelled)
! c : \ ~ i k e \ ~ a t a \ ~ a l i b r a t i o n \ ~ r e s s u r e \ E980727dpressure - I
. . . . . . . . . . . . . . - .. . . . . . . . . . . - sample rate (1000 1 Pressure (psig)]
II
1 ' 400.0 - I i
high limit (0.0) low limit (0.0)/
r$z-r :lo.oo- waveform
sample # J-1 - -. . O 10000 20000
-- .-
Pressure actual sample period (sec) 1 -
0.00
Figure B.5 Fuel line pressure front panel.
$ample rate (1000 sampleslsec) ]
Figure B.6 Fuel line pressure back panel.
B.3. Experimental Data Acquisition Prograrns
Figure B.7 shows the front panel of the experimental DAQ program developed for
the Ford injector. This VI used numerous sub-VIS to accomplish the desired set of tasks.
The program was designed to activate the fuel injector and the camera and to acquire data
durinp the injection event. A scan rate of 1000 Hz was used to acquire data from
differential analogue channels as discussed in chapter 5. The data was processes by the
software after the acquisition was complete. The temperature, pressure and flowrate
signals were converted from voltages (using the calibration equations), averaged over the
acquisition penod and stored to a data file. A 1000 Hz function generator signal was
used as an input to the DAQ board to control the injector pulse characteristics. Since the
injector was computer controtled, an extemal trigger was not necessary for this VI.
Starting the VI was al1 that was necessary for DAQ. The camera was also controlled by
software. The camera had a slow response, which made it necessary to incorporate a
variable time delay for the start of injection. In this was, the VI coordinated image
acquisition with fuel injection and DAQ.
The program used to acquire data for the high ternperature Stanadyne injection
experiments was based on the Ford DAQ program. Two changes were incorporated into
the Stanadyne injector DAQ program. A fuel pressure sensor was used in the DAQ setup
and was therefore added to the software. The injection pressure trace was recorded to a
sepante data file and was unprocessed by the program. The second change made to the
VI was do to the change in injector control strategy. The S tanadyne injector could not be
controlled through software so an extemal trigger was incorporated into the VI in order to
initiate DAQ.
- - - -- - -- - - 7 1
Pulse lnjector !Actual lnjection ICDM p u l s e s per CADI Off On :parameters Used E / i I r
10 F F] ~ S O S O ( C A D iftu non- f i r ing
j 10.50 -pi TDC o r s tartscan) A-
Sta tus I /Y +Il O 0
Number of cycles1 to acquire
I
I A- .VI 1
- - - - Number o f c y c l e s /
i lnaci ive 1 / S T O P 1 - - - - - - - - - . - .
In ject ion Durat ion (CAD) Wr i te Data to Spreadshee t F i l e
1.û F F] - - S imu la ted Engine R P M
Ave. Data F i le Narne & 9 3 0 00A
[ c : \ M i k e \ ~ a t a \ ~ x ~ e r i m e n t \ ] vL
- acqui red 1 [i--
: Fordlnjector\Avgdata\ 1980808 - Pulse Wid lh [1ns]1
Wr i te Pressure Data to 17 .92 A
Spreadshee t F i le
O F F )
~ c h a e v i t z Volt. Data F i l e Name -
1 Addit ional Tr igger
b S tanadynelnjector\ window s i z e coupling
i mode (O: no change) ;no -
d e l a l skip count ]
t r igger type
1 Plenum Temperature ( K ) 1 ,-- - 127.49
ln jector Fuel Ternpirature 1
ln jector Body Temperature
F3r-T Local Cy l inder Head Temperature
Hotwi re Flowrate (slpm) T Schaevitz Pressure (psig) 1 115.18
Figure B.7 Experimental data acquisition front panel.
C. Stanadyne Injector Modifications
The injector initially had four injection holes located radially around the injector
nozzle that injected fuel perpendicular to the injector body. Ln order to use the injector
under port injection conditions it had to be rnodified to deIiver fuel through a singte hole
dong the axis of the injector. To maintain injector fuel delivery characteristics the
surface area of the original four holes were equated to a single hole surface area.
Measurements were made using srnall dimeter wires with accurately known diameters.
The original holes were 0.23 mm in diameter and the final hole diameter was calculated
to be 0.46 mm. The tip of the injector was composed of hardened steel and it was
necessary to machine the hole using a irecision EDM (electrode discharge machining)
process to a through depth of 0.5 1 mm. The EDM process was chosen to avoid material
burring and to allow for an accurate hole size. The second step taken to convert the
injector to a single orifice design was to plug the original holes. A number of methods
were attempted before a final working injector was developed. The injector was
completely disassernbled to allow optical access to the tip from the large end with a light
source and a magnifying glass. Epoxy was used to hold 0.23 mm diameter stainless steel
plugs in place and the depth of insertion of these plugs was monitored so that the plugs
would not interfere with the needle and seat surfaces. It was found that under heated
injection conditions the epoxy would fail and the holes would open. Another method
used to plug the original holes was to use oversized plugs and shrink fit thern into place
with liquid nitrogen. This method also failed because it was difficult to get the plugs to
contract the necessary amount to produce a tight interference fit. The final method
attempted was to silver solder the plugs in place. A custom designed plug was made for
insertion into the large end of the injector body. The tip of the injector was then packed
with graphite powder through the existing large diameter orifice in order to prevent the
flow of solder into the injector and ont0 the needle seat surface. The plugs were low
temperature silver solder into place and the injector was flushed free of any graphite
powder. This modification method proved to be successful after testing and this injector
was used for al1 high temperature experimentation.
The injector had a high-pressure fuel fitting for fuel delivery and a modification
was made to the injector for fuel overflow. The manufacturer claimed that fuel overflow
could leak past the spring housing in the injector so a 50.00 mm length of 6.35 mm
diameter tubing was adapted to the injector body above the fuel input connection in order
to collect the overflow. In actual fact, fuel did not ovefflow under any of the
experimental conditions used.
The Stanadyne injector was a rnechanically actuated device and it was necessary
to monitor the injector pulse frequency with a lift sensor. The details of the sensor itself
are discussed in the Experimental Apparatus chapter of the document. A modification
was made to the injector lift pressure control end in order to accommodate the lift sensor.
The sensor diameter was slightly smaller than the control spring inner diameter, which
allowed a secondary threaded adapter of smaller diameter than the lift pressure set screw
to be rised. The adapter was cylindtical in shape with the end exposed to fuel closed and
was designed to thread into the lift pressure set screw used for cornpressing the control
spring. It was threaded such that the depth into the housing could be adjusted and a lock
not was used to maintain the desire depth.
injector adjustment
fbeI feed
Figure C. 1 S tanadyne injector modification.
D. Ford Fuel Injector Calibration
D.1. Ford Injector Calibration Procedure
SAE 11832 standard calibration procedure for gasoline fuel injectors [36] was
followed when calibrating the injector. The purpose of calibrating the injector was to
quantify the mass of fuel delivered per injection at a range of injector pulse widths. This
calibration was performed with room temperature fuel. Al1 equiprnent mentioned in the
procedure refers to figure 5.1. The procedure carried out was as follows:
1. Fuel was added to each of the 10 L fuel reservoirs. They were not filled to capacity.
2. Mechanical valves #1,2, 3 and 4 were opened.
3. Using toggle switch controlled solenoid valve #3, the small fuel reservoir was fiiled
(gravity fed), while carefully observing the fuel level through the fuel level window.
4. MechanicaI valve #3 was then closed.
5. The digital scale was leveled to horizontal in order to ensure consistent readings. The
scale was leveled using a leveiing bubble.
6. The pump was actuated with a toggle switch mounted on the front panel of the fuel
system. As shown schematically in figure 5.1, the fuel was drawn from reservoir #1,
through the fuel filters and the pump to the fuel rail. The pressure regulator allowed
the fuel pressure in the fuel rail to build to 39 psig. The fuel was then diverted to
solenoid valve #2 and back to reservoir #1.
7. The LabView calibration program was loaded. An explanation of the LabView
cal i bration program was covered in section 5.1 1.
8. The injector pulse frequency had a software setting of 20 Hz for al1 the calibration
experiments.
9. With the pump running as described in step 5, the relay actuation switch on the front
panel of the LabView calibration VI was set to off.
10. The injector was pulsed 10000 times as laid out in the SAE standard. This primed the
system and 'broke-in' the injector to ensure consistent operation.
1 1. The total number of injection was then set to 1000.
12. The relay actuation switch on the front panel of the LabView VI was set to on.
13. The desired injector pulse width was set.
14. The initial mass reading on the digital scale was recorded.
15. With the fuel pump still running the LabView program was activated. With the reIay
actuation switch set to on, the computer actuated relay controlled solenoid valves # 1
and #2 and simultaneously began pulsing the injector. In this configuration, the fuel
was drawn from the small reservoir to the fuel rail, through mechanical valve #4,
solenoid vaIve #1, the filters and the pump. From the fuel rail, the fuel would flow
back to the srnall reservoir through solenoid valve #2. When the 1000 injections were
completed the computer program stopped the pulses to the injector and
sirnultaneously de-energized the relay retuming solenoid valves #I and #2 to their
default positions.
16. The final mass reading on the digital scale was recorded.
17. After approximately two or three sets of injections, the fuel collection flask
downstream of the injector was emptied. The frequency with which this flask was
emptied depended on the duty cycle. At higher duty cycles, the injector delivered a
larger arnount of fuel.
Duty cycle (D) is defined as,
Phase1 is the 0.0 VDC portion of the TTL pulse to the injector control box and phase2 is
the 5.0 VDC portion. Changing the duty cycle effectively changes the injector open time.
Duty cycles from 0.2 to 0.8 (20 to 80 9%) in increments of O. 1 were mn through in random
order for statistical purposes. With a pulse frequency of 20.00 Hz, a duty cycle range of
0.20 to 0.80 was equivalent to a pulse width range of 10.00 to 40.00 ms. At each duty
cycle, thirty mass measurements were taken to improve the overall calibration. The
calibration curve that was developed to characterize the injector mass flowrate is shown
in figure D. 1. On the vertical axis of the graph is a dynamic flowrate in units of mg/pulse
and on the horizontal axis is pulse widrh in units of ms. The data fiom the calibration
experiments are listed in table D. 1 with a data summary listed in table D.2.
0.00 10.00 20.00 30.00 40.00 50.00 Pulse Width [ms]
Figure D. 1 Characteristic ifijector flow curve.
D.2, Ford Injector Calibration Data
Table D. 1 Calibration data.
Exp. Rep. #
Mean Std. Dev.
95.0% Con.
Note: A11 measurements are listed in units of grams.
Table D.2 Calibration summary data.
8 9 10 I 1 12 13 14 15 I6 17 18 19 20
Mean S td. Dev.
95 .O% Con.
-28.83 -93.23 38.63 -28.20 33.84 -32. I6 -96.69 43.79 -23.47 34.69 -31.08 -95.78 -92.40
64.48 65.96 66.93 65.67 66.12 64.45 65. I7 67.13 63.99 65.89 64.70
-93.3 1 - 159.19 -28.30 -93.87 -32.28 -96.6 1 - 16 1.86 -23.34 -87.46 -3 1.20 -95.78
-161.35 - 158.48
-65.84 16.49
-62.39 23.10
18.3 1 -59.08 19.58
-59.07 27.82
~ u t y cycle
0.2
- 143.35 -62.38 -139.58 -55.80
-55.75-131.7475.99 -59.1 1 - 136.37 -59.1 1
-135.64 -49.99
-49.97-127.52 -5 1.68 -46.26
Period [s/pulse]
0.05
Pulse Width
0.0 1
77.5 1 78-57 77.29 78.90
77.42 77.29 78.69 76.57 77.8 1
77.55 78.56 77.86 77.7 1 0.97
0.42 1
65.57 66.08 65.47 1.16
0.5 1
42-10 -48.7 1 29.60 -59.52 37.87 -50.20 42.70 -46.08 42.48 -47.32 74.40 -14.73 -54.56
' 26.88 3 1-60
-48.73 - 137.62 -59.70 - 147.48 -50.25 - 138.00 -46.19 - 134.14 -47.33 - 136.18 -14.75 -102.20 - 144.20
Qd [mg/pulse]
19.09
Pulse Width [msl 10
90.83 88.9 1 89.30 87.96 88.12 87.80 88.89 88-06 89.8 1 88.86 89.15 87.47 89.64 89.15 1.08
0.47
FIowrate [g,/ 1 OOOpulses]
19.09
86.42 8 1.76 -29.56 83.79 83.00 -30.29 28.60 87.86 -25.95 57.22 101.95 - 12.49 0.95
-27.2 1 -29.42
-143. I8 -30.7 1 -30.17 -140.79 -86.14 -25.94
-134.09 -6 1 .O3 -12.49 - 125.46 -1 14.20
1 13-63 1 1 1.18 1 13.62 I 14.50 113.17 1 10.50 1 14-74 1 13-80 108.14 1 18-25 114.44 1 12.97 1 15-15 1 13.00 3.3 I
1 -45
E. Transducer Caiibration Procedures and Curves
The manifold absolute pressure (MAP) sensor was used to measure upper
rnanifoId pressures in order to characterize the downstream injection environment. The
device was a 0.00 to 2.00 bar General Motors MAP sensor with a custom made 5.0 VDC
power supply. The linear relation used for this device relating absolute pressure to
voltage was:
P = 39.625 *V + 10.649 E. 1
In equation 5.1, P is absolute pressure in kPa and V is voltage measured in volts.
To measure nitrogen flows through the experimental apparatus a Nissan hotwire
anemometer was used (Nissan, Hitachi, 22680 53J00, AFH50-06, 0x23). A custom 12
VDC power supply was made to provide power the sensor. The sensor was cylindrical in
shape with a diameter of 88.9 mm. This diameter matched the throttle body diameter,
allowing the sensor to be positioned just upstream of the throttle plate. Since this
instrument was calibrated to rneasure air flowrates, a srnaIl correction factor was
necessary to measure nitrogen flowrates. The original regression equation for the air
mass flowrate was multiplied by the ratio of specific heats of air to nitrogen at 298K to
yieid the equation
Q = 128.46v3 - 3 17.42~' + 5 14.70~ - 283.75 E.2
In equation 5.2, Q is volumetric flowrate in slpm and v is voltage in volts. The correction
amounted to a change of 3.27% from the original regression equation produced with the
air calibration. The calibration curve for the sensor is shown in figure E. 1.
O .O 0.5 1 .O 1.5 2 .O 2.5 3 .O 3 -5 4.0 Voltage [VI
Figure E. 1 Nitrogen flowrate vs. voltage.
After testing was camed out, the best available method of acquiring a fuel line
pressure was a strain gauge pressure transducer. A 0.0 to 1000.0 psig Durham
Instruments Schaevitz transducer (P 102 1-0005, serial # 1 O06 15) and a bridge amplifier
were used to acquire the fuel line pressure. The transducer had a frequency response of 3
kHz at 4 dB cutoff. The sensor was not mounted closer to the injector because the fuel
supply line was heated. The sensor had a maximum operating temperature of 80°C so
minimizing heat transfer to the sensor was a priority. The tubing the sensor was mounted
to was essentially a stagnation tube so this aiso limited the transfer of heat to the sensor.
The linear relation produced from the calibration was found to be
P = 29 1 . 6 2 ~ + 14.62
In equation 5.3, P is pressure in psig and v is voltage in volts.
To calibrate the modified Stanadyne injector a method was needed to count the
number of injection events during a given time period. For this purpose a lift sensor
system was developed. A Wolf Controls Corporation Hall effect micosensor was used in
conjunction with two custom designed circuits to count injector pulses. When a current
is passed through a thin metal foi1 in the presence of a magnet a current a voltage is
produced. The Hall effect is utilized in the tift sensor to produce an analogue voltage
signal that is proportional to the injector needle movement. The injector was fitted with a
custom made magnet and a sensor holder assembly. The primary circuitry used linear
differential amplifiers, a differential emitter follower output and a voltage reguiator.
Since an actual lift quantity or distance could not be determined from the analogue output
signal it was converted to a TTL pulse with the aid of secondary thresholding circuitry.
The TTL pulses were read into the National Instruments board and were counted using
the LabView software. The method for counting injections was later modified due to
poor operation of the lift sensor at elevated temperatures. The fuel line pressure sensor
signa1 was used as a threshold signal input to the thresholding circuitry instead of the lift
sensor signal. In that way TTL pulses were produced when the pressure signal rose
above a set value.
Two methods were used to rnonitor Bosch fuel pump rotational speed. Initially a
hand held digital tachometer (Veeder Root Mode1 #661 1) was used to obtain a rotational
speed. An extemal shaft rotational speed rneasurement was made and then converted to
the actual pump speed. After preliminary tests with the DC motor drive and fuel pump it
was determined that a more accurate method of monitoring pump speed was necessary.
A sixty toothed gear was adapted to the coupling shaft between the DC motor and the
fuel pump. A magnetic pickup (Airpax 1-0002) was then mounted perpendicular to the
sixty toothed gear at a distance of approximately 2mm. The magnetic pickup signal was
amplified and displayed on a Daytronic frequency indicator/controller (mode1 #3340).
During testing the pump speed was monitored for each set of experiments.
Fuel pressure upstream of the Stanadyne injector was a crucial experimental
quantity and proved to be the most difficult quantity to obtain. The factors considered
when sizing a pressure sensor were frequency response, maximum working temperature
and maximum working pressure. Initial pressure testing was attempted with high-speed
piezoelectric pressure transducers, which are normal1 y used for in c y1 inder pressure
measurements. A 0.0 to 150.0 bar AVL transducer (1 2QP505C 1) and a 0.0 to 150.0 bar
Kistler transducer were calibrated and tested. A Kistler 5004 charge amplifier was used
for both of the piezoelectric transducers. Both had an adequate frequency response but
measure the rate of change in pressure rather than an actual pressure value. In order to
use the rate of change of pressure, an actual pressure value at some point during the
injection process would have to be known and al1 other values could then be referenced
to this known quantity. There were no accurately known pressure Ievels in the Stanadyne
injector fuel supply line so the piezoelectric transducers were ruled out. After further
testing it was determined that a strain gauge pressure transducer would be suitable for
pressure acquisition. The Schaevitz transducer calibration curve is shown in figure E.2
and was incorporated into the LabView software.
0.4 O .6 0.8 Voltage fV]
Figure E.2 Schaevitz tranducer pressure vs. voltage.
F. Data Sheets
F.1. Ford Injector Calibration Sheet
Date:
Mass Measurement FiIe Name:
I I . 12.
Repetition Nurnber 1.
Start M a s [grams] End Mass
F.2. Stanadyne Injector Calibration Sheet
Date:
Mass Measurement File Name:
Fuel Line Pressure Measurement File Name:
Repetition Number
1. 2.
Start Mass [grams]
End Mass
Fuel Temperature ["cl
Pump Speed frpml
Notes
F.3. Experimental Data Sheet
Date:
G. Calculations
G.I. Volumetric Flowrate
rev linduction Q z 0.85(970-)( ) G 9401pm
min 2rev
G.Z. Ford Injector Pulse Width Calculation [31]
For iso-octane
- PV m~ - = cycle R T
From equation G.3
\ cycle J
in F = (0.066 1 F)(0.562g,) g = 0.037 1 cycle !?A cycle
g, cycle
The characteristic fuel injector equation developed during calibration was
y = 2 . 3 3 ~ - 4.23 G.7
In equation G.7, y represents the dynamic flowrate calculated in equation G.6 and x
represents the pulse width.
mg F 37.1 - = 2 . 3 3 ~ - 4.23 pulse
From G.8, the pulse width used for experimentation was calculated to be 18.0 ms.
H. Jakob Number Data
Table H. 1 Temperatures and corresponding Jakob numbers for iso-octane.
1 Ternperature[K] 1 Jakob Number 1
1. Stanadyne Injector Calibration Data
Table 1.1 Stanadyne injector calibration data.
Injection Temperature
[Celsius] 23.62
24.64
Table 1.2 Stanadyne injector calibration data.
Std. Dev. 95.0% Con.
1 Injection 1 Pump 1 Injection 1 Start 1 End 1 Delta 1 FueUInj. 1
Pump Speed [rpm]
400.00 400.00 400.00 400.00 400.00 400.00
0.00067 0.00042
Injection Count
500 500 500 500 500 500
Temperature [Celsius] 121.53
Con. 95-0% l Mean
Std. Dev.
S tart Mass
90.20 49.17 8.27
-32.60 -72.91 -114.37
Speed [rpm]
400.00
120.62 120.27 119.27 117.51 1 17.30 1 17.24
1 18.13 1
End M a s
49.76 8.34
-32.60 -72.90 -114.37 -155.48
Count
500
400.00 400.00
Delta Mass
40.44 40.83 40.87 40.30 41.46 41.11
Mass
55.26
1
Fuelnnj. Wi nj . 1
0.0809 0.08 17 0.08 17 0.0806 0.0829 0.0822
500 500
0.00068
Mass
13.71
155.56 114.26
400.00 400.00 400.00 400.00
Mass
4 1.55
0.082
73.02 32.04 -9.24
500 500 500 500
[ d i nj -1
0.083 1
1 14.26 73.03 32.05 -9.23
-50.15
4 1.30 4 1.23
0.0826 0.0825
40.97
-50. T 5
0.08 19
4 1 .90 -92.05 0.0838
4 1.27 40.9 1
0.0825 0.08 18
Table 1.3 Stanadyne injector calibration data.
Injection Pump Injection S tart End Delta FueIAnj. Temperature Speed Count Mass Mass Mass Winj -1
[Celsius] [rpm] 146.15 400.00 500 153.91 112.59 41 -32 0.0826
1
141.12 400.00 500 7 2.25 30.14 41.1 1 0.0822 138.38 400.00 500 30.14 -11.36 4 1.50 0.0830 137.13 400.00 500 - 1 1.37 -52.55 41-18 0.0824 137.42 400.00 500 -52.55 -94.27 4 1.72 0.0834 144.3 1 400.00 500 155.50 1 13.76 41 -74 0.0835 143.57 400.00 500 113.75 71.79 4 1.96 0.0839 142.19 400.00 500 7 1.78 30.2 1 4 1.57 0.083 1
140.56 400.00 500 30.21 -1 1.48 41.69 0.0834
Mean 14 1 -508 0.083 Std. Dev. 0.00055
TabIe 1.4 Stanadyne injector calibration data.
Injection Temperature
[Celsius] 179.90
Mean Std. Dev.
95.0%
Pump Speed [rpm]
400.00
Con. 1 I
175.58 173.05 176.737
I
Injection Count
500
400.00 400.00
Start Mass
155.46
500 500
End Mass
1 13.6 1
74.56 32.84
Delta Mass
4 1-85
Fuelhj . W ~ J - 1
0.0837
32.87 -7.87
41 -69 40.7 1
0.0834 0.08 14 0.083
0.00080 0.00049
Table 1.5 Stanadyne injector calibration data.
Injection Temperature
[Celsius] 206.30 204.79
1 con. 1 I I
S td. Dev. 95.0%
Note: Al1 mass measurements are Iisted in units of grams.
Pump Speed [rpm]
400.00 400.00
0.00 1 04 0.00065
Injection Count
500 500
Start Mass
156.10 113.88
End Mass
113.90 71.67
Delta Mass
42.20 43.2 1
Fuelhj. [ gh j .]
0.0844 0.0844
J. Experimental Data
J.1. Ford Injector Experimental Data
Table J. 1
Photograph Number
1 2 3 4 5 6 7 8 9 10 1 1 12 13 14 15 16 17
18 19 20 2 1 22 23 24 25 26 27 28 29
Ford injector
Plenum Temp.
21.520 2 1.476 21.502 2 1.385 2 I .400 21.415 2 1.376 21.420 2 1.38 1 2 1.28 t 2 1-35 1 21.339 2 1.707 2 1.685 2 1.675 2 1.704 2 1 -688 2 1.660 2 1.689 2 1 -704 2 1.708 2 1.648 2 1.636 2 1.677 2 1.674 2 1 -682 2 1.687 21.681 21 -664
bottom
Knjected Fuel
Temp.
21.296 2 1 -244 21.262 2 1.280 2 1 -26 1 21.259 2 1.292 21.315 2 1.35 1 2 1.277 2 1.3 13 21.373 2 1 .548 2 1 .572 2 1 .590 2 1.582 2 1.540 2 1.606 2 1.542 2 1.565 2 1.539 2 1.555 2 1 .574
view-port
Injector Body
Temp.
21.195 2 1.1 13 21.178 2 1 .O90 2 1 .O7 1 21.142 2 1.154 21.168 2 1 .O85 2 1.070 2 1.204 21.162 22.742 22.628 22.563 22.432 22.483 22.24 1 22.2 1 1 22.150 22.28 1 22.253
experimental
Cylinder Head
Temp.
20.913 20.9 1 1 20.917 20.909 20.869 20.972 20.879 20.852 20.967 20.897 20.934 20.897 20.974 20.948 2 1 .O64 2 1 .O 13 20.896 20.855 20.965 20.936 20.89 1 20.8 18
data.
2 1.622 2 1.632 2 1.568 2 1.620 21.512 2 1.652
22.2 16
Manifold Pressure
[kPa]
110.818 1 10.807 110.822 1 10.835 1 10.839
22.179 22.124 22.088 22.109 21.965 21 -999
Nitrogen Flowrate
[slpm]
965.845 965.072 964.425 975.794 964.594
966.638 957.658 964.434 962.843 964.482 972.002
20.872 20.924 20.890 20.899 20.792 20.885
1 1 1.559 1 1 1 .552 1 1 1.546 1 1 1.540 111.528 1 1 1 SOI
968.000
110.844 1 10.852 120.844 1 10.854 1 10.554 1 10.860 110.856 1 12.146 1 1 1.837 1 1 1.65 1 1 1 1.573 1 1 1.568 1 1 1 -565 1 1 1.575 1 1 1 .566 1 1 1.569 1 1 1.563
20.8 t 9
963.005 972283 965.684 964.685 965.086 978.229 971.942 998.386 979.3 80 966.708 956.250 954.009 97 1.304 965.538 977.097 957.962 960.442
1 1 1 .560
30 3 1 32 33
Average Std-Dev.
95 .O% Con.
Table 5.2
Photograph Number
1 2 3 4 5 6 7 8 9
1 I o 11 12 13 14 15 16 17 18 19 20 2 1
22 23 24 25 26
2 1 .705 2 1 -663 2 1 -59 1
2 1.664 2 1 -577 0.141 0.048
Ford injector
Plenum Temp.
22.058 22.034 22.038 22.02 1 22.025 22.000 22.0 13 2 1 -988 22.0 17 21.875 21.912 21.811 21.845 2 1.909 22.018 2 1.976 21.894 21.902 22.153 22.073 22.073 22.092 22.009 21.992 2 1.988 2 1.958
2 1 .592 2 1 .596 2 1.603 2 1.6 17 2 1.477 0.146 0.050
top view-port
Injected Fuel
Temp.
2 1.795 2 1.828 21.803 2 1.8 1 1 2 1.845 2 1.790 21.794 2 1.76 1
2 1.842 21.513 21.521 21.521 21.520 2 1.672 21.587 2 1.737 21.605 21.665 2 1 .767 2 1.643 2 1.680 2 1.735 2 1.790 21.800 2 1.795 2 1.829
22.002 2 1.956 2 1.939 2 1.86 1 2 1.820 0.559 0.191
Injector Body Temp.
22.304 22.449 22.34 1 22.337 22.2 13 22.246 22.229 22.205 22.16 1 22.186 22.051 32.106 22.034 22.206 22.105 22.055 21.904 22.110 22.880 22.82 1 22.795 22.687 22.598 22.442 22.320 22.274
20.947 20.943 20.942 20.9 14 20.9 12 0.055 0.019
experimental data.
1 1 1 -490 1 1 1 -494 1 1 1.474 1 1 1.462 1 1 1.3 15 0.383 0.131
952.684 957.9 19 962.525 958.205 966.397
8.815 3 .O07
Cylinder Head
Temp.
2 1.466 2 1.38 1 21.425 2 1.390 2 1.449 2 1.49 1
2 1.525 2 1.464 2 1.398 21.083 21.074 21.091 21.019 2 1.242 21.179 2 1.255 21.141 21.247 2 1.226
Manifold Pressure
[kPa]
1 10.570 1 10.373 1 10.404 1 10.420 1 10.424 1 10.450 1 10.458 1 10.476 1 10.495 110.522 110.536 110.540 110.560 1 10.570 110.586 1 10.607 110.613
2 1 .O95
Nitrogen Fïowrate [slpm]
90 1.470 900.069 909.965 898.344 90 1 .O44 902.323 903.822 90 1.722 906.085 898.320 895.710 910.518 916.758 906.08 1 914.762 9 10.2 18 915.144
' 920.329 9 10.343 9 12.445 919.891 9 12.163 922.8 1 1
2 1 .O40 2 1.2 13 2 1.22 1 21 -209 2 1.22 1 2 1.238
110.617 1 1 1.43 1 1 10.841 1 10.626 1 10.649 1 10.667 1 10.690 1 10.739 1 10.768
919.924 952.254 924.940
Average 1 2 1.979 1 2 1.744 1 22.298 1 2 1.262 ( 1 10.645 1 9 12.674
Std. Dev. 1 0.071 1 0.1 10 1 0.225 1 0.138 1 0.188 1 10.934 1 95.0% 1 0.023 1 0.036 1 0.074 1 0.045 1 0.061 1 3.5721 Con.
5.2. Stanadyne Injector Experimental Data
Table 5.3 Stanadyne injector experimental data.
: Photograph Plenum
Number Temp. Tnjected Injector Cylinder Manifold
Fuel Body Head Pressure Temp. Temp. Temp. [kPa]
Ni trogen Spray Flowrate 1
c;; 1 [slpm] Angle
934.522
TabIe 5.4 Stanadyne injector experimental data.
19 20 21 22 23 24 25 26 27 28 29 30 3 1 32 33 34 35 36 37 38
Average Std.Dev.
95.0%
23 .582 23.578 23.591 23.490 23.561 23.446 23.271 23.305 23.27 1 23.196 23.275 23.200 23.149 23.263 23.162 23.166 23.162 23.166 23.1 16 23.086 23.549 0.299 0.095
Photograph Number
24.82 1 24.809 24.805 24.805 24.822 24.835 24.839 24.885 24.889 24.893 24.872 24.898 24.830 24.93 1 24.906 24.885 24.940 24.9 19 24.977 24.935 24.782 0.130 0.041
Plenum Temp.
23.692 23.767 23.675 23.801 23.784 23.793 23.797 23.755 23.822 23.839 23.767 23.839 23.877 23.826 23.839 23.885 23.864 23.793 23.978
Injected Fuel
Temp.
Injector Body Temp.
1 8.903 18.898 18.805 18.869 18.861 18.835 18.717 18.653 18.7 17 18.591 18.541
Local Cylinder
Head
1 10.076 1 10.093 110.089 1 10.104 1 10.103 1 1 O. 1 09 110.126 110.120 1 10.124 110.131 110.138
Manifold Pressure
[kPa]
Nitrogen Flowrate
[slpm]
922.769 92 1.333 6.236 1.983
1 10.158 1 10-070 0.091 0.029
23.864 23.6 13 0.252 0.080
Spray Cone Angle
30
922.32 1 928.444 930.414 92 1.275 927.126 927.062 926.912 923.028 922.785 929.568 921.756
18.602 18.435 18.437 18.442 18.455 18.39 1 18.298 18.37 1 18.323 18.930 0.443 O. 141
30 30 30 30 30 30 30 30* 30 30 30-
926.865 924.317 924.7 19 9 16.9 1 1 926.555 926.930 924.9 12 925.907
1 10.149 1 10.134 1 10.156 1 1 O. 154 1 10- 155 1 IO. 154 1 IO. 145 1 10- 153
30 30 30 30 30 30 30 30
Table 5.5 Stanadyne injector experirnental data.
10 1 1 12
Average Std.Dev. 95.0% Con.
22.499 22.312 22.514 22.4 13 0.102 0.057
Photograph Number
1 2 3 4 5 6 7 8 9 10 1 1
Average Std. Dev.
-
Table 5.6 Stanadyne injector experimental data.
78.798 78.981 78.61 1 79.878 0.893
95.0% Con.
Photograph Number
Plenum Temp.
23.191 23.229 23.073 23.069 23.015 22.989 22.851 22.804 22.632 22.598 22.93 1 22.944 0.207
48.706 48.636 48.439 49.054 0.729
Locai Cylinder
Head Temp. 28.867 28.704 28.498 28.352 28.176 28.051 27.925 27.900
O. 122
Lnjector Body Temp.
Injected Fuel
Temp.
125.468 125.614 125.60 1 125.485 125.572 125.572 125.531 125.472 125.2 15 125.227 125.0 1 1 125.433 0.196
Plenum Temp.
22.246 22.181 22.034 22.56 1 0.684
0 . 5 0 ~ ~ 0 . 3 8 7 ~ 1 6 8 ~
Injector Body Temp.
70.883 70.072 69.583 69.323 68.793 68. 104 66.910 66.620
Manifold Pressure
[kPa]
109.165 109.199 109.2 24 109.228 109.250 109.275 109.300 109.3 15
O. 1 16
Injected Fuel
Ternp.
66.1 14 65.792 69.57 1 68.342 1.738
Local Cylinder
Head
1 10.261 110.244 110.250 1 10.394 0.298
Nitrogen Flowrate
[slpm]
867.477 872.649 865.17 1 881.637 876.569 880.736 884.575 878.885
1 .O27
Manifold Pressure
[kPa]
Nitrogen FIowrate
[slpm]
Spray Cone Angle
34 34* 34 34 34 34 34 34-
27.339 27.188 28.227 28.1 12 0.518
Tern~.
Spray Cone Angle
944.250 952.904 947.1 18 949.552 17.217
30 30 30*
109.422 109.420 1 12.7 1 1 lO9.Sg 1 1.038
32.247 I
0.306
879.3 19 879.578 1056.555 893.0 14 54.569
0.614
34 34 34
P
06 06
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Table 5.8 Stanadyne injector expenmental data.
Photograph Number
1 2 3
7 Average
Table J.9 Stanadyne injector experirnental data.
Plenum Temp.
22.812 22.766 22.708
Std.Dev. 95.0% Con.
22.649 22.74 1
Injected Fuel
Temp.
173.880 174.0 1 1 173.803
0.070 0.05 1
173.964 173.875
Photograph Number
1 2
1 1 Average Std. Dev.
95.0% Con.
Injector Body
Temp.
89.575 88.595 87.546
0.128 0.095
Manifold Pressure
[kPa]
1 10.705 1 10.574
85.980 87.450
Plenum Ternp.
23.364 23.259
22.74 1 23.060 0.197 0.1 16
Locai Cylinder
Head Ternp. 31.120 3 1.1 1 1 3 1 .O57
1.247 0.924
Nitrogen Flowrate [slpm]
952.485 939.954
30.848 30.997
Spray Cone Angle
102 102'
192.382 192.704 0.306 0.181
Manifold Pressure
[kPa]
110.447 1 10.420 t 10.4 16
0.106 0.079
Local Cylinder
Head Ternp. 36.691 36.41 7
Injected Fuel
Temp.
193.052 192.848
1 10.43 1 1 10.428
Injector Body Temp.
99.043 98.26 1
9 1.776 95.102 2.370 1.401
Nitrogen Flowrate
[slpm]
931.917 94 1.426 938.521
0.011 0.008
Spray Cone Angle
90 90 90.
945.235 940.43 1
8.493 6.292
34.084 35-25 1
0.938 0.554
90
1 10.72 1 1 10.604 0.073 0.043
948.929 940.6 14 7.073 4.180
102
Table J. 10 Stanadyne injector experimental data.
Photograph Plenum Injected Injector Locai Number Temp. FueI Body Cylinder
Temp. Temp. Head Temp.
1 23.339 208.170 105.70 1 36.899 2 23.036 208.297 104.148 36.7 12
Manifold Nitrogen Spray Pressure Flowrate Cone
[kPa] [slpm] Angle
1 Average 1 22.909 1 206.865 1 100.273 1 35.553 S td. Dev. 0.153 1.235 2.622 0.816 --
95.0% 0.083 0.672 1.425 0.444 Con.
- - -- -. . --
Table J. I 1 Stanadyne injector experirnental data.
Photograph Plenum Injected Injector Local Number Temp. Fuel Body CyIinder
Ternp. Temp. Head Temp.
1 23.175 2 18.549 107.659 36.687
Manifold Pressure
W a I
Nitrogen Spray Flowrate Cone
[slpm] Angle
Table 5.12 S tanadyne injector experimental pressure data. Matching pressure data for the data listed in tables 5.3 to J. 1 1.
12 13 14
Average Std. Dev.
95.0% Con.
Time 1 Table 1 Table 1 Table 1 Table 1 Table 1 Table 1 Table 1 Table 1 Table
22.800 22.809 22.807 22.907 0.122 0.064
217.414 2 16.945 217.026 2 17.739 0.593 0.31 1
102.965 102.936 102.846 104.465 1.348 0.706
34.762 34.72 1 34.737 35.5 1 1 0.641 0.336
110.722 1 10.734 110.741 1 10.722 0.037 0.019
953.226 949.069
961,594 952.7 1 1 4.260 2.232
115 '
1 15 1 15
Note: Al1 temperature measurements are listed in units of Celsius. Al1 cone angle measurements are listed in units of degrees. Al1 pressures listed in table J. 12 are in units OS psig.