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1999-01-1766
Gear Noise Reduction through Transmission
Error Control and Gear Blank Dynamic Tuning
Chih-Hung (Jerry) Chung, Glen SteyerMTS Systems Corp., Noise and Vibration Division
Takeshi Abe, Mark Clapper, Chandra ShahFord Motor Co
Copyright 1998 Society of Automotive Engineers, Inc.
ABSTRACT
Gear whine can be reduced through a combination of
gear parameter selection and manufacturing process
design directed at reducing the effective transmission
error. The process of gear selection and profile
modification design is greatly facilitated through the use
of simulation tools to evaluate the details of the tooth
contact analysis through the roll angle, including the
effect of gear tooth, gear blank and shaft deflections
under load. The simulation of transmission error for a
range of gear designs under consideration was shown to
provide a 3-5 dB range in transmission error. Use of
these tools enables the designer to achieve these lowernoise limits.
An equally important concern is the dynamic mesh
stiffness and transmissibility of force from the mesh to
the bearings. Design parameters which affect these
issues will determine the sensitivity of a transmission to
a given level of transmission error. These dynamics are
studied through the use of detailed finite element models
of the transmission internals.
A systematic approach to gear element design will be
presented to optimize the gear blank design from the
perspective of the influence both the transmission error
and system dynamics on operating noise. The
correlation of model predictions with measured operating
data on prototype transmissions will be presented. The
model results will be used to illustrate how the use of
proper tuning of gear blank resonances can be used to
further reduce noise levels by 5 10 dB.
INTRODUCTION
Gear noise control measures can be categorized into the
classical areas of source path receiver measures.
Source treatments include all design and manufacturingmeasures to minimize the transmission error
Transmission error is the fundamental source of gea
whine and any reduction will result in lower perceived
levels. Tooth contact analysis incorporating mesh
kinematics, assembly tolerance analysis and load
deflections of the teeth, gear blank, and shafting enables
the engineer to minimize gear noise at the source.
The path of the gear noise in this instance is understood
to be the physical processes and system dynamics
translating the input transmission error into radiated
noise. Experience has shown that certain transmissions
are highly sensitive to transmission error, and thatproper control of the gear and shafting dynamics, as wel
as case radiation characteristics can have a dramatic
effect on reducing the transmitted noise. The system
dynamics can be properly tuned through an engineering
understanding of the underlying physical concerns and
proper design direction. This is facilitated through the
use of a detailed finite element model simulation.
Finally the receiver aspect is understood in the contex
of how the free-field radiated noise from the transmission
translates into noise inside the vehicle passenge
compartment. This includes the aspects of sound field
directivity, engine compartment reverberation, and body
panel transmission loss. The vehicle sound package is
designed to control this aspect of gear noise. The use o
engine compartment acoustic absorption and dash pane
mass damping layers is the primary design methods at
our disposal.
This paper will demonstrate how all three of the aspects
of gear whine were engineered to meet targets for a new
automatic transaxle.
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MAIN SECTION
The results presented in this paper were generated from
a combined experimental and analytical study of gear
noise in a newly developed transaxle. Overall NVH
performance was given high priority for the target
vehicle. One of the NVH goals was to minimize or
completely eliminate transmission gear whine tonaldetectability under normal driving conditions. This goal
was achieved with no slippage in program timing through
the use of vehicle level targets driven down to operating
measurements on a transmission dynamometer. Thus,
allowing for early detection of target exceedance and
resolution prior to production release.
The use of simulation technology for system dynamic
response and gear transmission error estimation
analysis was essential to clearly define the controlling
design parameters and provide direction for design
solutions. The effectiveness of design recommendations
from these simulations were confirmed throughtransmission dynamometer testing. Final testing in a
pre-production release vehicle confirmed that the target
was in fact achieved after resolving minor vehicle noise
path issues.
GEAR TRANSMISSION ERROR STUDY
One of the most significant contributors to gear whine is
gear transmission error. Transmission error is defined
as any deviation in output gear speed when the input
gear is rolled through the tooth mesh engagement with
constant angular velocity. This error can be expressed
in terms of an angular motion, or in terms of a relative
dynamic displacement along the gears line of action.
This displacement error causes radiated noise as a
result from dynamic forces at the gear tooth mesh which
are transmitted through the shafts to the transmission
housing.
Perfectly rigid gears with a perfect involute tooth profile
will theoretically have zero transmission error. In
practice, a finite level of transmission error is introduced
from a combination of gear tooth manufacturing errors,
assembly misalignments, load deflections and tooth
deformations. Some of the critical design measures forquiet gearing is the proper selection of the gear form,
refinement of the manufacturing process, and design of
the shafting and supports to minimize the resulting
transmission error.
Figure 1 shows the relative importance of gear
transmission error versus generated sound levels of fully
assembled transmissions for multiple gear sets. The
plot shows a 92% R2correlation coefficient of measured
gear transmission error versus measured transmission
operating sound levels.
-20.00
-10.00
0.00
10.00
20.00
-20 -10 0 10
Transmission Norm alized SPL (dB)
Measure
dTE
(20*LOG10(TE/Ref))
R2= 92%
Figure 1: Measured gear transmission error versus measured
transmission hemi-anechoic normalized sound pressure
levels
The transmission error was experimentally measured
with a single flank gear test rig capable of evaluating the
gear pairs under various operating loads and speeds
The sound levels shown were experimental results from
a hemi-anechoic dynamometer test system capable o
testing transmissions under load and through an
operating speed range. The normalized sound levels
shown in the plot are the de-trended average difference
over the operating frequency range relative to an
average transmission response. The two experimenta
tools presented here were important in the produc
development phase and were used to prove-ou
analytical tools and manufacturing development. Thus
they greatly improved the efficiency and timing for theNVH development of the transmission program.
Two key areas of the gear design were considered
during the development stage of the transmission. The
first consideration was the tooth macrogeometry. This
included decisions of the fundamental gear design
parameters such as module, number of teeth, pressure
angle, helix angle, etc. where careful consideration o
manufacturing, durability, and noise need to be
considered. The second phase of development was to
optimize the gear tooth microgeometry which includes
involute, lead, and bias modifications to the tooth surface
for low transmission error, optimal load distribution andoptimal contact patterns for the gear pair unde
operating loads and speed.
Transmission error minimization was one of the highest
weighted factors in the gear design process for the gea
set under study. Analytical modeling techniques and
design optimization were utilized to achieve the targe
design criteria. Gear tooth contact analysis techniques
were some of the fundamental tools which allowed the
gear engineer to optimize gear design and study gear
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stress, mesh stiffness, transmission error, load
distribution and contact patterns for differing conditions.
In order to determine the optimum tooth design a gear
design optimization software package GODA [1] (Gear
Optimization Design Analysis) establishes the basic gear
design parameters with considerations of design and
manufacturing limits. Further detail analysis is then
performed using LDP [2] (Load Distribution Program)
and CAPP [3] (Contact Analysis Program Package).CAPP is a general gear analysis tool which is capable of
solving gear tooth contact problems by combining the
strength of finite element techniques with boundary
elements and surface integral techniques. LDP is also a
contact analysis prediction tool, but uses simplified
classical representations of the tooth and gear bodies,
allowing faster detailed studies of tooth design
specifications and tooth surface topographies. Both
software techniques can determine relative transmission
error performance, mesh stiffness, stress, and tooth and
gear body load deflection. If the detailed analysis is
unsatisfactory, the design process begins again with
GODA.
-20
-10
0
10
3.5 4.5 5.5
Total Gear Contact Ratio
NormalizedSPL
(dB)
Drive Flank
Coast Flank
Trend Line
[A]
[B]
[C]
[D]
[E]
Figure 2: Normalized transmission sound pressure level (hemi-
anechoic chamber) for gear designs A-E of differing
contact ratios
Figure 2 shows five different candidate gear designs that
were considered for the transmission design.
Analytically, each of the designs had differing appeals
and compromises. With the aid of a gear tooth form
grinder all of the candidates could be prototyped at arelatively low cost and quick timing. Each design could
be easily tested in the hemi-anechoic chamber or
transmission error test stand. This allowed
determination of their relative NVH performance with
nominal tooth surface modifications, and also allowed
comparison against their analytical predictions (Figure
3).
Figure 2 clearly shows the classical trend of
transmission error decreasing with increased gear tooth
contact ratio. Gear tooth contact ratio is the theoretical
average number of gear teeth in contact during tooth
meshing. It is generally considered that smoother tooth
meshing action will occur for higher gear contact ratios
In this design range, transmission sound levels and
transmission error decrease at approximately 10 dB pe
1.0 increase in contact ratio. In this case, gear design
[C] was eventually chosen for production because it was
deemed adequate for noise performance and was
acceptable for manufacturing.
Drive Gear
Tip
Drive GearSAP
Drive GearTip
Drive Gear
SAP
Observed ContactPattern
Predicted Contact Pattern
Figure 3: LDP predicted versus observed gear tooth contact
pattern
Figure 4: CAPP FEM model of studied gear pair
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Figure 5: CAPP predicted load distribution along the gear tooth
lines of contact
Final verification of the tooth macrogeometry was
performed using CAPP. This analysis verified tooth
strength and rim deflections under load so that gear and
assembly deflections could be considered in the final
design stages. Figures 4 and 5 show examples of
CAPP simulations. Experimental verification of the
analytical tools used allow the design robustness to be
further evaluated for noise performance without
producing prototype hardware.
After the primary gear design parameters were
established, tooth microgeometry was then optimized for
the operating speeds and load deflections induced by
the transmission. Microgeometry is the refined tooth
surface topography of the gear tooth flank. Typically,
topography definition includes modifications of lead,
involute profile, and tooth bias modifications. To
determine the most robust tooth surface specifications,
optimization techniques incorporating LDP [4] were used
where manufacturing tolerances, assembly andoperating variances were considered. Table 1 shows
Taguchi allocation for five critical gear parameters: lead,
profile and bias specifications a-e, alignment and torque.
This statistical technique attempts to minimize the
transmission error over the design space considered
using historical manufacturing capability to define the
tolerance range for each parameter. This attempts to
insure that the tooth surface specification is robust
enough for transmission error over the design space.
Figure 6 shows sample order tracks of transmission
noise performance through a speed range under load
both before and after optimizing the tooth surfaces.
Table 1: Allocation to Taguchi study
a b c d e Align. Torq TE
1 + + + + + + + f1
2 + + + - - - - f2
3 + - - + + - - f3
4 + - - - - + + f4
5 - + - + - + - f5
6 - + - - + - + f6
7 - - + + - - + f7
8 - - + - + + - f8
9 0 0 0 0 0 0 0 fc
TEnominalforforceexcitingM esh-
factorweighting:5.0
)8(
indexysensitivit:2Eqn.1
minimizofunction t:1Eqn.)1(
1
2
fc
n
fin
SI
SIfcF
n
i
=
=
=
?+?=
=
This section clearly demonstrates that gear mesh
performance and transmission error are critical factors
for gear whine. Additionally, it shows how proper
analytical analysis supported by experimenta
techniques can find optimum noise performance while
considering design and manufacturing criteria. Although
gear design and manufacturing alterations can
significantly improve gear whine performance, factors
such as gear blank and transmission dynamics mus
also be considered in order to achieve total system
robustness.
Order Function
40.00
100.00
50.00
60.00
70.00
80.00
90.00
0 8002000 4000 6000Frequency (Hz)
Figure 6: Overlay of transmission sound level performance before
and after tooth profile microgeometry optimization (Solid
Optimized Profile, Dashed Initial Profile)
GEAR BLANK DYNAMICS STUDY
Unfortunately there are limits to the degree to which
transmission error can be reduced. It has been found
that certain transmission designs have a relatively high
sensitivity to transmission error. In this instance even
the best gear profile design and manufacturing controls
result in unacceptable levels of gear whine. Minimizing
the noise sensitivity to transmission error is an importan
aspect of transmission design
The design sensitivity of a transmission can be
understood in terms of the system dynamics. The
excitation is the transmission error at the gear mesh
This acts as a specified dynamic displacement forcing
the mating gear teeth apart. The gearing design mus
accommodate this transmission error, absorbing the
input motion while minimizing the vibrations transmittedto the outer casing.
Experience with previous transmission design had
shown that proper tuning of the gear and shafting
dynamics may provide on up to a 10 dB effect on
radiated noise levels. However proper tuning of the
rotating elements requires an understanding of the
component dynamics and interactions. This reqires the
use of a detailed finite element model to perform the
design studies.
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The mesh frequency for the transfer gear set in this
transmission covered the frequency range of 1500
5000 Hz under normal operating conditions. It was
necessary to use a solid element based finite element
model since the mesh frequency extended to such high
frequencies and it was anticipated that the results could
be sensitive to the fine details of the gear blank design.
Figure 7 shows the gearing finite element model. During
the course of the study a number of design iterations
were performed on the gears in order to optimize thenoise performance while not sacrificing manufacturability
nor durability. The finite element model was created
using an automatically generated mesh based off the I-
DEAS solid model. Figure 8 shows the dimensioned
wireframe used as a basis for the secondary gear model.
This modeling approach allowed for the various
wireframe dimensions to be modified, the model quickly
updated and the noise performance predicted.
Figure 7: Geometry plot of gearing finite element model.
CS1_{Global}"Revolve3"
Figure 8: Wireframe geometry basis for secondary gear blank
cross section.
Model Correlation
Model correlation tests were performed to ensure
accuracy of the predictions. Correlation was performed
using component artificial excitation data as well as ful
system operating measurements. Experimental impac
frequency response functions of acceleration over force
were compared to the model for unrestained
components such as the individual gears and shafts
Figure 9 shows a typical result from a gear blank test.
The system models were also used to predict theoperating vibration during controlled speed sweeps
This was accomplished by predicting the response pe
unit transmission error over the frequency range o
interest, then multiplying the result by the predicted leve
of transmission error from the tooth contact analysis
Figures 10 and 11 show overlays of analysis results with
experimental order track plots for the gear blank
vibration as measured through slip rings as well as
transmission housing bearing vibration. These figures
show excellent correlation at the problem frequency
range of 4200 Hz. Elsewhere the correlation was o
acceptable level for the purpose of this study.
The comparison of model predictions and test results
shown in Figures 10 and 11 provided a high level o
confidence that the model was accurately accounting fo
the relevant physical phenomena. The model was then
used to perform numerical design studies to identify an
optimal design.
0.1000
10000.0
1.000
10.00
100.00
1000.00
500 150001000 10000Frequency (Hz)
Figure 9: Overlay of an acceleration over force frequency
response function for a axial driving point on the rim of
the secondary gear. (solid test data, dashed model)
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1.000
1000.00
10.00
100.00
0 60002000 4000Frequency (Hz)
Figure 10: Overlay of model prediction with experimental data for
the order track function of secondary gear axial vibration
at the gear rim. The primary frequency of concern was
4200 Hz.
0.00
40.00
10.00
20.00
30.00
0 60002000 4000Frequency (Hz)
Figure 11: Overlay of model prediction with experimental data for
the order track function transmission housing bearing
vibration.
Design Optimization
In order to identify an optimal design it is necessary to
develop detailed insight into the physical processes and
understand the design issues. In the case of gear noise,
the optimal design is arrived at through a relatively fine
balance of the dynamic characteristics of a number of
components. An approach of blindly changing
numerous design parameters and evaluating the effect
until the magical combination of design changes is
arrived at results in a very inefficient process. However,if the baseline model is used to perform a detailed
investigation of the controlling dynamics then it becomes
possible to home in on a near optimal design in relatively
short order. The following discussion presents a quick
summary of the theory of quiet gearing design.
The dynamics of the gearing can be best understood as
a two part process of the development of dynamic force
at the mesh for a unit transmission error, followed by the
transmissibility of this mesh force to the casing. This
principle has been presented and demonstrated in
previous papers [1,2].
The fundamental design parameters which control the
dynamic mesh stiffness are gear inertias, bearing
stiffnesses and shaft bending and torsional stiffnesses
In the higher frequency ranges we find that the gear
blank out-of-plane bending modes as well as the gear
mesh compliances have a significant influence.
The transmissibility of the mesh forces to the bearings
are controlled by such parameters as the mass of the
gears, the bearing stiffnesses and the shaft bending
stiffness. Past experience of applying this simulation
technology and design optimization approach to
automotive transmissions has shown that the primary
impact of design modifications is in the control of the
dynamic mesh force. It is a common misconception in
gearing design that a low noise gear design would be
comprised of very massive and rigid gears and shafts
In fact the opposite is often true. Quiet gearing is bes
embodied in light weight gears with sufficient compliance
to absorb the transmission error without generatingundue dynamic force.
The parameters which control the dynamic mesh force
can best be understood with the aid of Figure 12. The
transmission error will be absorbed through the sum o
motion of the primary and secondary gear along the line
of action. The developed mesh force is an equal and
opposite force reaction on both gears at the pitch contac
point and oriented along the mesh line of action. Thus
the mesh compliance (or motion per unit dynamic mesh
force) is the sum of the compliance of the primary gear
and the secondary gear. The reciprocal of this mesh
compliance is then the dynamic mesh stiffness, or the
force developed at the mesh per unit transmission error.
The presence of resonances in the individual gears is
beneficial in that they reduce the mesh force
Unfortunately these resonances may also cause peaks
in the transmissibility of forces to the bearings. The
secret to the design of quiet gearing is to design in
compliances (often through modal resonances) tha
reduce the mesh dynamic stiffness but do not adversly
affect the force transmissibility from mesh zone to
bearings.
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1.00E-09
1.00E-06
1.00E-08
1.00E-07
200 80001000Frequency (Hz)
Primary N=1
N=2
SecondaryN=2
Primary N=3
SecondaryN=0
Shaft Rigid Bodyon Brgs
Mesh dynamics controlled bygear blank modes (n nodaldiameters)
F
mesh compliance
ondary primary
xf
xf
=
+ +
1
sec
_ primary
xf
secondary
xf
Figure 12: Illustration of how the mesh dynamic stiffness is the
result of the individual gear line of action (LOA) dynamiccompliances. The upper part of the figure shows the
dynamic LOA compliances for the primary and
secondary gears for the baseline design.
A bounce mode of the gear on the bearing compliances
would result in such a transmissibility peak. However a
purely torsional mode of a shaft will result in a reduction
in the mesh force with no effect on the transmissibility of
the force from the mesh to the bearings. Similarly a two
nodal diameter mode of an axi-symmetric gear blank
(the potato chipping mode) will reduce the mesh force
but will result in no net shaking force transmitted to the
bearings.
The system finite element models can be used to
accurately predict the system dynamic compliances
taking into account the gear rigid body motions and
bending compliances as well as shaft rigid body and
bending motions. These functions can be used to
understand the dynamic mesh stiffness as well as the
transmissibility of forces from the mesh to the bearings.
This process was used to study the baseline
transmission design. Figure 13 shows the dynamic
compliances and the resulting mesh dynamic stiffness.
Notice the prominent peak in the predicted mesh force atthe 4200 Hz problem frequency. This peak in the mesh
force was understood to be the result of a lack of
appropriate component modes in the neighboring
frequency range. It was determined that if certain of the
component modes could be retuned into this frequency
range then the mesh force could be smoothed out.
X/F
1.00E-09
1.00E-06
1.00E-08
1.00E-07
0 80002000 4000 6000Frequency(Hz)
A B C D
Figure 13: Gear LOA compliances and dynamic mesh force for thebaseline gear sets. Notice the irregular spacing of themodes and the wide frequency range about 4200 Hz witha total lack of component modes. This corresponds to ahigh level peak in the mesh force.
Figure 14 shows one of the gear blank modes which was
a controlling factor in the mesh compliance. This mode
is a two nodal diameter mode which occurred at 3200
Hz. A design objective was set to modify the secondary
gear web in such a manner as to force this mode into the
3800 Hz range and to drop the primary gear n=3 mode
from 5300 Hz down to 4400 Hz. This would result in a
more uniform spacing of the modes and help to reduce
the mesh force peaks in the 3000 to 5000 Hz range.
Figure 15 shows the predicted effect on the mesh
compliance and the resulting mesh force.
The actual change to the gear web wireframe was easily
developed through the use of geometric optimization
algorithm applied separately to the primary and
secondary gears. The underlying dimensions on the
wireframe were used as the design variables and the
objective functions were defined as the new targe
frequencies.
Figure 14: Deformed geometry plot of the 2ndnodal diameter mode
of the secondary gear which was tuned to the 4000 Hz
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frequency range and smooth the mesh dynamic stiffness
as a function of frequency.
X/F
1.00E-09
1.00E-06
1.00E-08
1.00E-07
0 80002000 4000 6000Frequency (Hz)
A B CD
Figure 15: Gear LOA compliances and dynamic mesh force for themodified gear sets. Notice the uniform spacing of the
modes and the alternate spacing of primary gear
resonances with secondary gear resonances. The mesh
force is seen to uniformly increase with frequency.
Prototype gears were fabricated and installed in the
transmission and operating noise measurements made
on a tranmission dynamometer. The sound pressure
order track functions were measured for four
microphones located at the front of dash locations. A
composite function was computed as the power average
of these four functions.
Figure 16 shows the predicted effect of the modifieddesign on the mesh dynamic force per unit micrometer.
Figure 17 shows the corresponding measured averaged
front of dash noise levels for the baseline and modified
designs. This figure shows data for the fundamental
gear mesh frequency as well as the second harmonic
(scaled up by a factor of 2 in order to overlay on the
fundamental).
10
70
20
30
40
50
60
700 80002000 4000 6000Frequency
(Hz)
Figure 16: Analytical results: Overlay of predicted dynamic mesh
force per unit transmission error for the baseline design
(dark dash) and the modified design with tuned gear
blanks (light dotted).
40
100
50
60
70
80
90
700 80002000 4000 6000Frequency (Hz)
Figure 17: Experimental results: Overlay of mesh order track plots
of operating noise for the baseline design (dark dash)
and the modified design with tuned gear blanks (light
dotted).
The results of Figures 16 and 17 show a remarkable
degree of aggreement in the differences between thebaseline and modified design. These both show the
modified design to be over 10 dB quieter at the previous
problem frequency of 4200 Hz, with a corresponding
increase in levels at the new resonance frequency o
3500 Hz. Also, both figures show the 3500 Hz peak to
be on the order of 8 dB lower than the original peak a
4200 Hz. This reduction corresponded to a ful
subjective rating point increase when installed in the
vehicle.
Further design modifications were studied and
implemented which affected the transmissibility of the
mesh force to the bearings. The model was additionallyused to study detail design modifications to the
transmission housing and identify stiffening structure
which resulted in 1 2 dB of additional noise reduction.
VEHICLE PATH CONSIDERATIONS
One of the difficult aspects of automotive NVH
development is the fact that numerous engineering
activities are simultaneously occuring. The subjective
NVH performance of the transmission is determined not
only by the acoustic strength of the transmission, but is
equally influenced by the acoustic integrity of the body
the presence of mechanical short circuits, and by the
ambient masking from wind and road noise. All of these
features are ever changing during the vehicle
development and do not allow for a valid subjective
evaluation of the transmission in the vehicle until the
final production release vehicle is available
Unfortunately at this stage it is too late to affect any
major reduction in the gear noise.
It is essential that a vehicle system NVH targe
development and allocation process be used. This
enables the transmission development to proceed and
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allows for rational decisions about the various design
and cost trade-offs required to have confidence in the
final product.
The dominant noise path for this transmission was
anticipated to be airborne due to the high frequencies
associated with the transfer gear. Transmission tonal
target levels were determined through a process of
applying tonal masking theory. The vehicle office had
determined targets for wind and road noise on acompetitive basis. This allows the generation of a
frequency and road speed dependent target surface for
the gear tonal noise levels at the drivers ear. The gear
whine will be undetectable for all levels below this
surface.
The drivers ear target surface is driven down to a front
of dash target surface with the use of an acoustic
transmission loss model for the dash panel. The vehicle
office again had target information for this based on
competitive analysis. The acoustic package was being
driven to meet this target.
This engine compartment front of dash noise level was
then driven down to a target level for an equivalent front
of dash plane measured on a transmission
dynamometer in a hemi-anechoic chamber. The gear
development activities identified the gear blank tuning
which enabled the design to meet this noise target. All
of the transmission noise development work was
accomplished without the benefit of full vehicle testing.
Operating road tests were performed as soon as a
production release vehicle was available. These tests
had identified a gear whine problem in the 45 mph speed
range. Subsequent testing on a chassis dynamometer
quickly determined that the noise was a result of a
mechanical path through the transmission shift cable.
Figure 18 shows an order track plot for three baseline
configuration runs and three runs with the shift cable
disconnected. The addition of mechanical isolation in
the shift cable resolved this noise problem. The gear
whine passed the subjective targets in the final vehicle
tests,
0
60
10
20
30
40
50
1000 70002000 3000 4000 5000 6000Frequency
Cable
Disconnnect
Figure 18: Passengers ear Sound Pressure order track data from
vehicle tests with and without the shift cable
disconnected.
Based on the data in Figure 18 a design modification to
the shift cable was implemented. Subsequent vehicle
drives showed the transmission noise to meet or exceed
the subjective evaluation targets.
In each vehicle development program it is essential to
perform an engineering process assessment in order tovalidate and refine the methods. Further vehicle testing
was conducted to evaluate the assumptions in the
system NVH model. The vehicle was instrumented with
four microphones in the engine compartment on the fron
of the dash. The average of the order track data from
these microphones were compared to the fou
dashplane microphone data from the transmission
dynamometer. This data confirmed the model used to
project the free-field sound pressure data to the engine
compartment data.
The apparent transmission loss was evaluated by
dividing the average front of dash microphone data by
the interior microphone data. Only the order track data
at the transfer and final drive gear mesh orders were
used. This data was compared to the anticipated body
transmission loss. These results were very close and
validated the system noise model.
CONCLUSION
The results reported in this paper demonstrate very
clearly the potential impact that simulation technology
can have on reducing transmission gear noise through
gear profile modifications for transmission erroreduction as well as gear blank tuning for reducing the
tranmission sensitivity to transmission error. The use o
tooth load deflection analysis had identified gearing
changes which resulted in a 5 dBA reduction, while
proper gear blank tuning reduced the peak noise levels
by approximately 10 dBA.
The success on this transmission has demonstrated the
value of incorporating these technologies into the early
design process. These tools will aid in optimal selection
of transmission skeletal designs and provide the ability
to develop even quieter designs before the problem has
been overly constrained.
Incorporation of these simulation technologies early in
the design process require that appropriate design
targets are developed. This begins with determination o
the target levels for vehicle interior noise based on tona
detectability theory. These targets are then rolled down
to transmission nearfield noise levels as well as moun
vibrations. Finally, these targets can be translated into
simulation targets such as bearing reaction forces and
dynamic mesh force.
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A fully integrated approach of target roll downs coupled
with simulation technologies enables the transmission
design team to select more optimal design from an NVH
perpestive at a point in the process where there exists
greater design freedom.
ACKNOWLEDGMENTS
The authors would like to acknowledge the support and
contributions of numerous colleagues at both Ford MotorCo. and MTS Systems Corp. without whom this effort
would not have been possible. Among these are Mr.
Jeff Nolff Mr. John Hiatt and Mr. Brian Wilson. The
authors are also very grateful for the solid support of
management throughout the effort and their commitment
of the necessary resources to successfully apply these
technologies.
REFERENCES
1. D. Hughson (1990), GODA5 Gear Optimization anAnalysis 5), SAE Gear Design, Manufacturing, andInspection Manual, Chap. 12, pp 175-186.
2. Houser, D.R. (1990), Gear Noise Sources and theiPrediction Using Mathematical Models, SAE GeaDesign, Manufacturing, and Inspection Manual, Chap. 16pp 213-223.
3. S. Vijayakar, A Combined Surface Integral and FiniteElement Solution for a Three Dimensional ContactProblem, International Journal for Numerical Methods inEngineering, 31, 525-546 (1991).
4. S. Sundaresan, K. Ishii, D. Houser, Design of HelicaGears with Minimum Transmission Error UndeManufacturing and Operating Variances, JSMEinternat iona l Conference on Mot ion andPowertransmissions, Nov. 1991.
5. G.C. Steyer, Influence of Gear Train Dynamics on GeaNoise, Proceedings of the National Conference on NoiseControl Engineering, pp 53-58, 1987
6. G.C.Steyer and T.C.Lim, System Dynamics in Quiet GeaDesign, Proceedings of the 9th International ModaAnalsysis Conference, pp 999-1005, 1991