High Voltage Switched-Mode Power Supply for Three-Phase AC ...
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AC AC AC AC AircraftAircraftAircraftAircraft SystemsSystemsSystemsSystems
A Senior Project
Presented to
The Faculty of the Electrical Engineering Department
California Polytechnic State University, San Luis Obispo
In Partial Fulfillment
Of the Requirements for the Degree
Bachelor of Science
By
John Brewer, Jr.
And
Kamaljit Bagha
June, 2010
© 2010 John Brewer, Jr. and Kamaljit Bagha
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Table of Contents
Section Page
Title Page i
Table of Contents ii
List of Table and Figures iv
Acknowledgements vi
I. INTRODUCTION 1
II. BACKGROUND 3
2.1 Predator® - Too Versatile For Its Own Good 3
III. REQUIREMENTS 5
IV. DESIGN 7
4.1 Inverter Project Design Overview 7
4.2 The Power Stage 10
4.3 The PWM Control Circuit and Signal Flow 17
4.4 The LC Output Filters 28
V. CONSTRUCTION 32
5.1 PWM Control Circuit Assembly 32
5.2 Inductor Construction 33
5.3 Wire Harnesses, Connectors, and Cable Fabrication 35
5.4 Power Plane Construction 36
5.5 Enclosure Fabrication 36
iii
5.6 System Assembly 37
VI. TESTING 38
VII. CONCLUSION AND RECOMMENDATIONS 45
VIII. BIBLIOGRAPHY 48
Appendices
A. Schematic 50
B. Bill of Materials 66
C. Circuit Board Layout 69
D. Circuit Board IC and Component Locations 70
E. Hardware Configuration and Layout 71
iv
List of Tables and Figures
Table Page
3.1 MIL-STD-704F AC System Requirements [3] 5
3.2 Summary of Inverter Project Requirements 6
B.1 Bill of Materials and Donated Items 66
Figures
2.1 MQ-1 Predator Drone 3
2.2 MQ-9 Reaper Drone, originally named “Predator B” 4
4.1 IGBT Half-Bridge Configuration 7
4.2 Block Diagram of Inverter Project 9
4.3 Bootstrap Supply Topology with Protection 11
4.4 Nomenclature Used for IGBT Switching Transition 15
4.5 PWM Control Signal Flowchart 18
4.6 dsPIC-based Function Generator 19
4.7 Passive Component Nomenclature for UC3637… 21
4.8 Generating a Trigger Pulse 25
4.9 Bode Plot of Second Order LC Filter 28
5.1 Portion of Circuit Board Layout Graphic 32
5.2 Wire Wrapping 33
5.3 Inductor Bobbin 33
5.4 Tightly Wound Inductor 34
v
5.5 Wood Handle to Support Bobbin 34
5.6 Finished Inductor with Connectors and Mylar Tape 34
5.7 Fabricated Wire Harnesses 35
5.8 Top and Bottom Sides of Copper-Clad Board 36
5.9 Inverter System Assembly 37
6.1 Ideal Inverter Pspice Simulation 38
6.2 Output Voltage Waveform of Ideal Inverter Simulation 39
6.3 IGBT Gate Driver and Half-Bridge Pspice Simulation 39
6.4 High-side (green) and low-side (blue) IGBT… 40
6.5 Adjustable Three-Phase Sinusoidal Reference… 42
6.6 Trigger Pulse successfully generated by AD823AN… 42
6.7 Square wave with 97% duty cycle successfully generated… 43
6.8 Three-phase and Neutral-phase Duty Cycle limited… 43
6.9 Three-phase Inverter Output Voltage referenced… 44
6.10 Three-phase Inverter Output Voltage referenced… 44
C.1 Microsoft PowerPoint Circuit Board Layout 69
D.1 IC and Component Circuit Board Location 70
E.1 Hardware Configuration and Layout 71
E.2 Test Bench Setup 72
AcknowledgementAcknowledgementAcknowledgementAcknowledgementssss
We would like to thank –
Mr. John (Jeff) Brewer, Director of Electrical Engineering for the Aircraft
Systems Group at General Atomics Aeronautical Systems, Inc. for providing and
funding a challenging project for us to work on and offering the technical support
needed to complete this project. We appreciate him sharing his knowledge and
insight of the broad range of topics that this project covers and have been inspired
to work hard and never stop learning as electrical engineers.
Dr. Taufik, Professor of Electrical Engineering at California Polytechnic State
University, San Luis Obispo, as our faculty advisor for this project. His dedication
and excellence as a teacher both in the classroom and lab have equipped us with a
solid foundation of knowledge and understanding in the field of power electronics.
His teaching curriculum and techniques significantly contributed to our ability to
“Learn by Doing” here at Cal Poly.
Mr. Jaime Carmo, Cal Poly EE Department Electronics Technician, for his
support and generous donation of time, equipment, and parts throughout the
construction, testing, and fabrication stages of our project.
Mr. Cole Brooks, Cal Poly mechanical engineer and friend, for his assistance
in metal parts fabrication
Our families for supporting our educational endeavors.
Sincerely,
John Brewer, Jr. and Kamaljit Bagha
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I.I.I.I. INTRODUCTIONINTRODUCTIONINTRODUCTIONINTRODUCTION
With the advent of the first power rectifier by an American engineer and
applied physicist, Robert Hall, in 1952, a new form of power control and conversion
was born – Power Electronics. The successive arrival of thyristors in 1957, bipolar
transistors in the 1960s, power MOSFETs in the late 1970s, and IGBTs in the 1980s
led to the rapid advancement of power electronics in all fields of electrical
engineering [1]. These fields include utility power distribution, industrial electronics,
and especially aircraft electronics because of the small size of power electronic
components. A few applications of power electronics in these fields include power
quality controllers, variable speed drives, and power supplies.
Power electronics is unique in its method of power control and conversion in
that it is based on the switching fully-on and fully-off of semiconductor devices to
regulate power flow. More efficient than linear power regulation which uses
variable resistance to regulate power flow, switching semiconductor devices by
using a technique called “Pulse Width Modulation (PWM)” is the method used in a
modern “switching” or “switched-mode” power supply (SMPS). PWM is a technique
where the duty cycle of the semiconductor switch is manipulated to control power
flow through the switch. As a result, the output voltage delivered to the load can be
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well regulated to produce a fixed Direct Current (DC) voltage or a desired Alternating
Current (AC) voltage.
There are two types of converter topologies used in SMPS design – isolated
and non-isolated. Transformers are used in the design of isolated converters to
provide flexibility in circuit design by allowing for separate (isolated) input and
output current return paths to “ground.” Non-isolated converters, however, do not
use transformers and the input current ground is used as the ground for the output
load current.
For our application, we have designed a non-isolated SMPS that produces AC
output voltage from DC input voltage – this is known as a DC/AC converter or,
simply, an inverter. It uses the common method of Pulse Width Modulation to
switch Insulated Gate Bipolar Transistors (IGBTs) to control the flow of power from
±DC input voltage “rails” to three-phase, sinusoidal AC output voltage. In the next
section of this report, we will present the background and application of our inverter
design.
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II.II.II.II. BACKGROUNDBACKGROUNDBACKGROUNDBACKGROUND
Our three-phase, sinusoidal inverter project was sponsored by Jeff Brewer,
the Director of Electrical Engineering at General Atomics Aeronautical Systems, Inc.
(GA-ASI). The purpose of this project was to design and build a proof-of-concept
high-power switched-mode inverter. This project began the development process
for a high-voltage three-phase AC power supply for use on any of the Predator®
Unmanned Aircraft Systems (UAS) that GA-ASI manufactures.
2.1 Predator® – Too Versatile For Its Own Good
Predator® aircraft like the ones shown in Figure 2.1 and Figure 2.2 are used
by multiple branches of the United States’ military and homeland security including
the Air Force, Army, U.S. Customs and Border Protection, Central Intelligence
Agency, and NASA. They are popular for their wide range of applications including
remote sensing, reconnaissance, weapons delivery, search and rescue, and
surveillance. Predator® systems are versatile
aircraft platforms upon which an increasingly
large array of electronic device payloads like
sensors, weapons, and communications
equipment can be mounted. Fig. 2.1 – MQ-1 Predator Drone
Source: Public Domain
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Currently, these devices are powered by 28 VDC power on the aircraft – one of three
standard aircraft power systems prescribed by MIL-STD-704F [3]. Because these
aircraft are required to support an increasing number of electronic payloads, the
weight of the cables in the aircraft needed to deliver 28 VDC power to these
payloads exceeds practicality. So, to counteract this problem, plans to provide high-
voltage power systems in accordance with MIL-STD-704F on Predator® aircraft are in
effect. It is estimated that the cable weight required to distribute power on the
aircraft will be reduced by a factor of ten when high-voltage power is provided [2].
These plans include the provision of a 270VDC system and a three-phase AC system
as outlined in the next section of this report.
Fig. 2.2 – MQ-9 Reaper Drone, originally named “Predator B”
Source: Public Domain
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III.III.III.III. REQUIRREQUIRREQUIRREQUIREEEEMENTS MENTS MENTS MENTS
The purpose of our project was to design and build a non-isolated DC/AC
SMPS capable of supplying 10 kW for a standard three-phase AC aircraft power
system. According to MIL-STD-704F,
“AC systems shall provide electrical power using single-phase or three-phase
wire-connected grounded neutral systems. The voltage waveform shall be a
sine wave with a nominal voltage of 115/200 volts [115 VRMS] and a nominal
frequency of 400 Hz” [3].
Because MIL-STD-704F also prescribes AC system requirements like the
sample shown in Table 3.1, the production level version of our inverter will require
the use of closed-loop feedback to provide adequate line and load regulation.
However, designing a closed-loop system was beyond the scope of this project, so
an open-loop system was required.
Table 3.1 – MIL-STD-704F AC System Requirements [3]
Characteristics Limits
Steady State Voltage: 108.0 VRMS to 118.0 VRMS
Voltage Unbalance: 3.0 VRMS (maximum)
Voltage Modulation: 2.5 VRMS (maximum)
DC Component: +0.1 to -0.1 Volts
Voltage Phase Difference: 116° to 124°
Steady State Frequency: 393 Hz to 407 Hz
Frequency Modulation: 4 Hz
Peak Voltage: ±271.8 Volts
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Lastly, the production level version of our inverter will be powered by the
engine alternator on the aircraft. The three-phase, variable voltage, variable
frequency engine alternator power will be rectified and regulated to produce
±190 VDC rails from which the inverter will draw its power [2]. Since this
rectification and regulation of engine alternator power is beyond the scope of this
project, it was required that our proof-of-concept inverter work from ±125 VDC rails
for three-phase operation given 10Ω resistive loads. This requirement was limited
by the available test equipment in Cal Poly’s EE Department Power Electronics Lab.
The nominal requirements of our inverter project are summarized below in
Table 3.2. In the following section of this report, we will present a system overview
of our inverter project followed by a more detailed discussion of the circuit design
process.
Table 3.2 – Summary of Inverter Project Requirements
Nominal System Requirements
Converter Topology: Non-Isolated SMPS
Input Voltage: ±125 VDC
Output Voltage: 85 VRMS AC
Output Voltage Waveform: Three-Phase, Sinusoidal
Steady State Frequency: 400 Hz
Maximum Output Power: 10 kW
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IV.IV.IV.IV. DESIGNDESIGNDESIGNDESIGN
This section of our report represents a majority of the work that went into
this project – circuit design. In this section, we will present an overview of our
inverter project followed by a series of discussions covering the details of the circuit
design, signal flow, and discrete components used.
4.1 Inverter Project Design Overview
The design of our three-phase sinusoidal inverter is based on the PWM
switching of N-Channel IGBTs connected in a half-bridge configuration as shown in
Figure 4.1. As the high-side and low-side IGBTs are complementarily switched fully-
on and fully-off, they connect the load to the
+DC and -DC Rails, respectively. Since the
output is connected to one of two voltage
polarities during this method of switching, it is
known as Bipolar Switching. Because the
output voltage is effectively an amplified
version of the PWM Control Input, this stage of
the inverter system can be considered the
Power Amplification stage and is shown in the System Block Diagram in Figure 4.2.
Fig. 4.1 – IGBT Half-Bridge Configuration
Source: John Brewer, Jr.
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The IGBT Gate Drivers and Floating Bootstrap Supply topology required to drive
N-Channel IGBTs in this configuration are also indicated in Figure 4.2 and will be
discussed in Section 4.2.1.
The PWM Control Input is generated by the PWM Control Circuit block. The
PWM Control Circuitry is responsible for generating the sinusoidal reference
waveforms, establishing the switching frequency, creating PWM signals, limiting the
duty cycle of the PWM signals, and interfacing logic-levels. A thorough discussion of
the PWM Control Circuitry will be presented in Section 4.2.2 of this report.
The final piece of our inverter design is the inductor/capacitor (LC) output
filters on each phase. The LC output filters were designed to smooth the PWM
output of the Power stage and filter out high-frequency harmonics introduced by
IGBT switching. These will be discussed in Section 4.2.3.
An important characteristic to note about our inverter design is the fourth
IGBT Half-Bridge “leg” which is used to create a virtual ground (neutral) through
which phase currents from an unbalanced three-phase load can return to the DC
input supply. The PWM Control Input to this neutral leg will have a nominal 50%
duty cycle, creating a voltage that is one-half the DC supply voltage upon which the
three-phase sinusoidal output voltages will be centered. The creation of this neutral
return is necessary in the case that a bipolar DC supply with ground connection is
unavailable and a unipolar DC supply must be used.
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4.2 The Power Stage
As mentioned in Section 4.1, the Power Stage consists of two IGBTs
connected in a Half-Bridge configuration. Four identical half-bridge legs form the
foundation of our three-phase inverter and are responsible for controlling power
flow from the DC Input Supply to each phase output voltage – Phase A, Phase B,
Phase C, and Neutral.
Jeff Brewer donated the IGBTs that were to be used for this project –
IRGP50B60PD1, WARP2 Series IGBT with Ultrafast Soft Recovery Diode from
International Rectifier (IR). These IGBTs are high-speed, high-power, SMPS,
N-Channel IGBTs capable of withstanding a collector-to-emitter voltage of 600V.
Driven with a gate-to-emitter voltage of 15V, these IGBTs can source 33A with
maximum turn-on and turn-off delay times of 40ns and 150ns, respectively [4]. With
an operational output voltage of 115VRMS, the resulting power output capability of
all three inverter phases combined can then be calculated to be:
= 3 ∗ ∗ (Eq. 4-1)
∴ = 3 ∗ 33 ∗ 115 = 11.385
In conclusion, using these IGBTs will fulfill our requirement to design a three-
phase inverter capable of supplying 10kW with an output voltage of 115VRMS. In the
next section, we will discuss the floating bootstrap supply topology required for
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switching N-Channel devices, the IGBT Gate Driver design process, and design
measures taken to protect the IGBTs.
4.2.1 Bootstrapping, IGBT Gate Drivers, and Transient Voltage Protection
N-Channel semiconductor devices are commonly used in half-bridge
configurations as our IGBTs are used in the power stage of our inverter. However,
these N-channel devices require a charge applied to the gate that is positive with
respect to the emitter such that (VGE > VTH). While this does not present a problem
for turning on low-side devices with a power supply referenced to the –DC rail, the
same supply would be unable to turn on the corresponding high-side device as the
high-side emitter follows the output voltage of the half-bridge – a much larger
voltage than the supply voltage. Therefore, a bootstrap supply topology is required.
As illustrated by the schematic of a typical bootstrap supply topology in
Figure 4.3, a bootstrap capacitor is connected from the power supply, VCC, to the
high-side emitter. Due to
the charge storage
characteristics of a
capacitor, the bootstrap
capacitor voltage will rise
+VCC above the high-side
emitter, providing the Fig. 4.3 – Bootstrap Supply Topology with Protection
Source: John Brewer, Jr.
12
necessary gate drive voltage to turn on the high-side device. When an internal
switch in the Gate Driver Integrated Circuit (IC) connects node VB to the high-side
gate, the high-side device will turn on. It will then turn off when the gate is
disconnected from VB and connected to VS by internal switches in the Gate Driver IC.
However, the high-side device will also turn off if the charge on the bootstrap
capacitor is depleted due to parasitic gate current. Because of this, the duty cycle of
the high-side device switching must be limited and the bootstrap capacitor sized
accordingly to prevent premature/uncontrolled turn-off of the high-side device.
For our project, we decided to use the Si8234BB ISOdriver manufactured by
Silicon Labs as our High-Voltage Integrated Circuit (HVIC) Gate Driver. This recently
released HVIC Gate Driver contains two completely isolated high-side/low-side
drivers in one package that are each capable of sourcing 4.0A peak output current.
The isolated drivers are controlled by a single PWM Control Input signal and an
external resistor used to program the deadtime created between the switching of
the high-side and low-side devices. The input logic side of the device is 5V TTL
compatible, while the output side can support the 15V supply used to switch our
IGBTs. Also note that we have incorporated the Disable pin of the Si8234BB device
into our circuit design to provide the functionality of being able to turn combinations
of our phase output voltages on or off [5].
We consulted IR’s “Design Tips for Using Monolithic High Voltage Gate
Drivers” during the design process for our HVIC gate drivers and floating bootstrap
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supply [6]. To size the bootstrap capacitor, we started by calculating the maximum
voltage that the bootstrap capacitor voltage was allowed to drop (∆VBS) when the
high-side IGBT was supposed to be on. To do this, we decided from Fig. 8 of our
IGBT datasheet that the minimum gate-to-emitter voltage to allow should be 11V in
order to guarantee a collector-to-emitter voltage of about 2V given a collector-to-
emitter current around 33A. Also, we used a value of 1V for the typical forward
voltage drop of the MUR460 power rectifier used to protect VCC as shown in
Figure 4.3 [7]. As a result, we obtain
∆ = − − , − , (Eq. 4-2)
∴ ∆ = 15 − 1 − 11 − 2 ≅ 1
We then confirm that VGE,min > VBSUV- where VBSUV- is the high-side supply
undervoltage negative going threshold of 8.10V as indicated in Table 1 of the
“Si823x” datasheet from Silicon Labs [5].
The next step in sizing the bootstrap capacitor was to consider the following
factors contributing to a decrease in VBS:
- IGBT turn-on required Gate charge (QG) = 308nC (max) [4]
- IGBT Gate-Emitter leakage current (IGES) = 100nA [4]
- Output supply quiescent current (IDDAQ) = 3.0mA (max) [5]
- Bootstrap diode instantaneous reverse current (ILK_D) = 50μA [7]
- Bootstrap capacitor leakage current (ILK_C) = 0μA (use ceramic capacitors)
- High-side on time (TH,on) = 24.5μs (98% duty cycle at 40kHz)
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Then we have
#$% = # + ' + (() + %*_, + %*_- ∗ ./, (Eq. 4-3)
∴ #$% = 30812 + 31001 + 3.04 + 505 + 056 ∗ 24.558 ≅ 38312
And the minimum size of the bootstrap capacitor can be calculated by
2, = )9:9;<
∆=>? (Eq. 4-4)
∴ 2, = @A@
B=≅ 3831C
So, to account for estimation error and temperature drift, we decided to use a
bootstrap capacitance of 660nF, almost twice as big as the calculated CBOOT,min. As
mentioned earlier, MUR460 power rectifiers are an ideal choice for use as the
bootstrap diode in our bootstrap supply design. These devices were also donated to
our project and can withstand a reverse voltage of 600V and have a reverse recovery
time of less than 100ns [7].
The final design issues to be mentioned regarding the design of the IGBT gate
drivers are the addition of decoupling capacitors, sizing of gate resistances, and
measures taken for protecting the IGBTs and HVIC Gate Drivers. Sufficient
decoupling capacitance was added to our gate driver design by placing ceramic and
electrolytic capacitors in parallel with the gate drive supply voltage very close to
both the low-side Gate Driver output pins and the bootstrap diode. The ceramic
capacitor provides a fast charge tank and limits D
DEF by reducing the equivalent
series resistance while the electrolytic provides a longer lasting charge tank.
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The process for sizing the gate resistances consisted of both calculations to
derive ballpark figures and hardware experimentation. From “Design Tips for Using
Monolithic High Voltage Gate Drivers,” we can estimate the necessary size of the
turn-on gate resistor by fixing the switching-time. As shown in Figure 4.4, the
switching time is defined
as the time spent to
reach the end of the
plateau voltage resulting
from charging the IGBT
gate capacitances with
QGC and QGE. Estimating
an appropriate switching time to be about 115ns and knowing QGC and QGE to be
105nC and 45nC, respectively, we can calculate
$=$ = )GHI)GJ
KLM (Eq. 4-5)
∴ $=$ = BNOIPO
BBOQ≅ 1.3
And
R$% =HH T =UVW;XJY;GJ
(Eq. 4-6)
where Vge* is approximated to be 6.2V from Fig. 17 of our IGBT datasheet [4], and
R$% RZ3Q [\]^6 & R, (Eq. 4-7)
Fig. 4.4 – Nomenclature Used for IGBT Switching Transition
Source: International Rectifier [6]
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Where RON(source) is 2.7Ω according to the Si8234BB datasheet, and RG,on is the value
for the high-side IGBT gate resistor [5]. As a result, we have
R, = BO=T_.`=
B.@$− 2.7Ω ≅ 4Ω
And following IR’s Design Tip, we size the low-side IGBT gate resistor to be larger
than the gate resistor of the high-side device – about 5Ω. This will result in softer
switching of the low-side device and a reduction in magnitude of the voltage
transients caused by parasitic inductances during switching.
Lastly, the design of the Power stage includes devices added to protect IGBTs
and HVIC Gate Drivers from transient voltage spikes caused by parasitic inductances
in the circuit. First, Zener clamp diodes with a reverse voltage breakdown voltage of
16V are added across the gate-to-emitter junctions of both high-side and low-side
devices. Shown in Figure 4.3, these Zener clamps protect the HVIC Gate Driver
output, sink current generated by transient voltage spikes occurring on the collector,
and keep the IGBT gate-to-emitter voltage from exceeding the maximum limit of
20V [4]. Another clamp device used is the series combination of a 16V Zener diode
and MUR460 Power Rectifier positioned between the VS pin of the HVIC Gate Driver
and the –DC rail also shown in Figure 4.3. The purpose of this clamp device is to
guarantee that VS does not exceed maximum undervoltage limits when negative
voltage transient spikes are induced by parasitic inductances. The production level
version of our inverter will include the placement of reverse-biased transient voltage
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suppression diodes with a reverse breakdown voltage <600V across the collector-to-
emitter IGBT terminals. These will protect the IGBTs from damage caused by voltage
transients on the DC supply rails or half-bridge output node. Due to the DC input
supply test limits, we omitted these diodes from our proof-of-concept design.
The circuit schematics for the four Power Stages of our inverter design can be
found on Sheets 11, 12, 13, and 14 of the system schematic in the Appendices. In
the next section of this report, we will discuss the PWM Control Circuit and signal
flow.
4.3 The PWM Control Circuit and Signal Flow
The PWM Control Circuit is the “brain” of our inverter project and is
responsible for generating our three-phase sinusoidal reference signals, producing
PWM Control signals for all three-phases and neutral, limiting the duty cycle of the
PWM Control signals, and interfacing logic levels. It was designed using discrete
analog components with the exception of a Microchip dsPIC 16-bit Digital Signal
Controller-based function generator. Considerations for choosing the discrete
analog devices we used included availability, ease of prototype implementation,
proven reliability, low replacement cost, and extreme temperature tolerance for
military temperature requirements.
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In this section of the report, we will present a discussion of the circuit
components used to perform these tasks and cover the details of the circuit design
required to interface these components and generate PWM Control Input signals for
the HVIC Gate Driver of each IGBT half-bridge. Figure 4.5 illustrates the general flow
of a single phase PWM Control signal.
Fig. 4.5 – PWM Control Signal Flowchart
Source: John Brewer, Jr.
19
4.3.1 Generating Three-Phase Sinusoidal Reference Signals
The first step in the design of the PWM Control Circuit was to generate three
sinusoidal reference voltages, each having 120° of phase displacement from the
others. Fortunately, this step was already complete before we began our project.
Manufactured and donated by GA-ASI, the Microchip dsPIC Digital Signal Controller-
Based Function Generator shown in Figure 4.6 supplies three-phase sinusoidal
waveforms with accurate sine shape and phase displacement. The frequency and
amplitude of the output sinusoids
are adjustable, but for our
application they are set to have a
frequency of 400 Hz and peak-to-
peak amplitude of 2V.
In order to make the
amplitude of our inverter output
voltage waveforms adjustable,
remove the DC offset from the reference sinusoids, and buffer the reference
sinusoids, we AC coupled each of the sinusoidal phase voltages from the function
generator to adjustable gain, non-inverting amplifiers designed using TL082 JFET
Input Op-Amps. Simple RC highpass filters with a cutoff frequency of 1 Hz were used
for the AC coupling. The TL082 op-amps were chosen because of their suitable slew
rate of 13V/μs, low Total Harmonic Distortion of 0.003%, ability to operate from
Fig. 4.6 – dsPIC-based Function Generator
Source: John Brewer, Jr.
20
±15V supplies, and compact 8-pin packages containing two op-amps each. The
circuit schematic for this step in the PWM Control Circuit can be located on Sheet 3
of the system schematic in the Appendices.
4.3.2 Generating PWM Signals from Reference Sinusoids
The next step in the design of the PWM Control Circuit was to generate the
PWM Control signals for each phase including neutral by comparing the reference
sinusoids to a triangle wave having a frequency equal to the desired IGBT switching
frequency. Using a PWM Controller IC is the most efficient way to do this, so we
chose the Unitrode UC3637 Switched-Mode PWM Controller for DC Motor Drives.
The UC3637 was chosen because of its high reliability, robustness, and
widespread use in industry. It is easy to program and provides a built in error
amplifier, under-voltage lockout, and can operate from dual power supplies [8].
Concurrently, multiple UC3637 ICs can be readily synchronized according to
Unitrode’s Design Note about “Design Considerations for Synchronizing Multiple
UC3637 PWMs” [9]. This was an important quality of the UC3637 since four PWM
Controller ICs were required in the PWM Control Circuit and the ability to
synchronize them would simplify circuit construction.
We arbitrarily decided to establish the Neutral phase PWM Controller as the
Master PWM device. This IC was “programmed” with the passive components
shown in Figure 4.7 according to the following design requirements:
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• Triangle Wave frequency of 40kHz (same as the IGBT switching frequency).
• Triangle wave amplitude of 20 VP-P (large to increase noise immunity).
• Modulation scheme with no deadtime (since the Si8234BB IGBT Gate Driver
supplies the necessary high-side/low-side switching deadtime).
• Under-voltage lockout level of 10.75V (to prevent switching IGBTs when
there is not enough supply voltage to fully turn them on).
Fig. 4.7 – Passive Component Nomenclature for UC3637
Master Device Programming
Source: John Brewer, Jr.
Consulting the Unitrode UC3637 Datasheet and following the Unitrode
Application Note U-102, we calculated the following [8] [10]:
R 3I=9c6T3T=?6W?
(4-8)
∴ R 3IBN =6T3T BO =6
N.O$= 50Ω ≅ 47.5Ω
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2 W?`de3I=9c6T3T=9c6f (4-9)
∴ 2 N.O$
`∗PNg/h∗e3IBN =6T3TBN =6f= 313iC ≅ 300 iC
For clarity, we note that the Unitrode Application Note U-102 suggests that the
constant current used to charge the external capacitor, CT, be within the range of 0.3
to 0.5 mA. Because the amplitude of the triangle wave has been designed fairly
large, we programmed ISET to a value on the higher end of this range, 0.5 mA, as
used in Eq. 4-9. Using this higher charging current performs a secondary feature of
allowing the use of a larger capacitor, CT, that will be able to store enough charge to
drive the input of a TL082 op-amp configured as a voltage-follower. This will
produce a buffered triangle wave used to drive the UC3637 slave devices and the
AD823AN op-amp used for generating a trigger pulse for the HCF4538B Monostable
Multivibrator
Since +VTH and -VTH should be symmetrical at ±10V in our application, we set
R1 = R5 and calculate REQ (where REQ = R2 + R3 + R4) after choosing reasonable values
for R1 and R5. Using an iterative process to determine values for R1 and R5, we
• Calculated REQ
• Calculated the approximate bias current, IBIAS, through the resistor
divider created by R1, REQ, and R5 between +VS and -VS.
• Adjusted values accordingly to limit the bias current to an order of
hundreds of microamps. This prevented unnecessary power loss while
23
maintaining the ability to adequately charge the PWM controller
comparator inputs.
As a result,
RB RO 20.4Ω
R) = ` ∗ j ∗ =9c
=? T =9c (4-10)
∴ R) = ` ∗ `N,PNNk ∗ BN=
BO= T BN== 81,600 Ω
We also needed to ensure that the +VSLV node voltage indicated in Figure 4.7
was always less than the magnitude of the triangle wave despite any drift in
resistance, the UC3637 Master PWM device characteristics, or the AD823AN op-amp
characteristics. This will guarantee the generation of a trigger signal for the
HCF4538B Monostable Multivibrator which is used to create a square wave with
frequency equal to the triangle wave and duty cycle of 98%. In order to do this, we
needed to determine the minimum voltage difference, ∆Vmin, required between +VTH
and +VSLV. Following the procedure outlined in Unitrode Design Note DN-53A, we
determined ∆Vmin to be about 1.5V, requiring a ballpark resistance for R2 and R4 to
be 6.3kΩ [9]. However, based upon the hardware available during the construction
phase of our project,
R` = RP = 5.62Ω and R@ = 68.1Ω
Yielding
W$ = I=?T3T=?6
mInIjIoIp (4-11)
24
∴ W$ IBO= T 3TBO=6
`N,PNNk I O,_`Nk I _A,BNNk I O,_`Nk I `N,PNNk≅ 2505
Lastly, we used the equation provided in the UC3637 IC datasheet to
establish an undervoltage lockout level of 10.75V. Using a 100kΩ resistor for R6, we
calculated
$ = `.O∗3qIr6
q (4-12)
∴ Rs = =?9;Y9 ∗ q
`.O− R_ = BN.sO=∗BNNgk
`.O− 100Ω = 330Ω
At this point, the simplicity of synchronizing the other three UC3637 slave
devices becomes evident. Besides adding 0.1μF decoupling capacitors to all device
pins that are tied to a fixed voltage, we simply connect the +VSLV node to the +VTH
slave device pins, the –VSLV node to the –VTH slave device pins, the SD pin of the
master device to the SD pins of the slave devices, and the buffered triangle wave
output from the TL082 voltage-follower to pins 2, 8, and 10 of the slave PWM
devices.
The -15V low/+15V high PWM Control Input signals are each interfaced with
their respective 74AC00 CMOS NAND Gates by a current limiting resistor/voltage
divider/Schottky diode network that reduces the signal to 0.4V low/+5V high.
In the next sections of this report, we will discuss the portions of the PWM
Control Circuit that limits the duty cycle of the PWM Control Inputs to 98%.
25
4.3.3 Generating a Trigger Pulse
As mentioned in the previous section, our PWM Control Circuit design
includes the use of an AD823AN rail-to-rail FET Input op-amp as a comparator.
According to the AD823AN datasheet, this op-amp has a high slew rate of 22V/μs
and can operate from ±15V supplies [11]. As a result, this op-amp provides the
speed needed for a short switching transition time and required no voltage level
shifting to interface the ±20V buffered triangle wave. Although the AD823AN is a
dual op-amp package, only one of the op-amps is needed by our control circuit.
With the buffered triangle wave tied to the positive input and the +VSLV
voltage tied to the negative input of the comparator, a +15V pulse with duration of
about 1μs is generated when the triangle wave is at its peak and exceeds the +VSLV
threshold as illustrated in Figure 4.8.
This -15V low/+15V high trigger pulse
is interfaced with the HCF4538B
Monostable Multivibrator through a
current limiting resistor and Schottky
diode network that reduce the trigger
pulse to a 0.4V low / +15V high pulse.
4.3.4 Monostable Multivibrator
After being triggered by the trigger pulse delivered by the AD823AN
comparator, the HCF4538B Monostable Multivibrator configured as a non-
Fig. 4.8 – Generating a Trigger Pulse
Source: John Brewer, Jr.
26
retriggerable one-shot generates a 24.5μs pulse. Since the trigger pulse is delivered
every 25μs, the equivalent waveform produced is a 40kHz square wave with a duty
cycle of 98%. This 0V low/15V high signal is interfaced with the 74AC00 CMOS
NAND Gates through a simple resistor divider reducing it to a 0V low/+5V high
signal. The timing equations and wiring configuration for a non-retriggerable one-
shot design were given by the HCF4538B datasheet [12]. As illustrated in our
schematic (See Appendix) we paired a 5,600pF timing capacitor, C38, with a 10kΩ
potentiometer, R22, so we could adjust the output pulse of width, T, according to the
equation
. R`` 2@A (4-13)
∴ R`` jt `P.OuQ
O,_NNv= 4.375Ω
4.3.5 High-speed CMOS NAND Gates
The 74AC00 CMOS NAND Gates used in our PWM Control Circuit provide the
logical AND function needed to limit the duty cycle of the PWM Control Input signals
to 98% [13]. By “ANDing” the PWM Control input signal for each phase of our
inverter with the square wave output by the One-Shot, the duty cycle of the PWM
Control Input signals are effectively limited to 98%. This provides the high-side IGBT
off-time necessary for recharging the bootstrap capacitor as discussed in Section
4.2.1.
27
4.3.6 Supplying Power to the PWM Control Circuit and Bootstrap Supply
After having figured out how to drive our inverter IGBTs and design the PWM
Control Circuit, we needed to figure out how to supply power to the low-voltage side
of our project. Since the function generator donated to our project by GA-ASI came
with its own power supply, we only needed to supply +15 VDC, -15 VDC, and +5 VDC
to our circuit. For these voltages, we bought two 15V and one 5V isolated AC/DC
wall adapters – the first two sold as “Notebook Adapters” and the latter as an
“Internet Router Adapter.” Since these adapters are isolated, we were able to
reference our PWM Control Circuit DC Bias Supply voltages to the most negative
voltage used for the DC Input Supply to our inverter – a requirement for properly
driving our Half-Bridge IGBT topology with a Bootstrap Supply.
4.3.7 Using Decoupling Capacitors
As we complete our discussion of the PWM Control Circuit, it is important to
note the use of decoupling capacitors throughout our circuit design. The use of
0.1μF ceramic capacitors tied between logic ground and any IC pin connected to a
bias voltage provides sufficient AC decoupling and noise immunity. It is also
important to note the use of sufficiently larg electrolytic bias supply capacitors
located at the circuit board D-sub connector where the power is delivered to the
board.
28
4.4 The LC Output Filters
The design process for our inverter project included the design of three
Second-Order LC filters to be used for smoothing the output voltage waveforms for
each phase of our inverter. The design of these LC output filters was based on the
400Hz output voltage frequency and the 40kHz PWM switching frequency. As
illustrated by the Bode plot in
Figure 4.9, we designed the LC
output filter to have a corner
frequency of 2kHz so it would
effectively pass the 400Hz
voltage waveform while
sufficiently attenuating the 40kHz
PWM switching frequencies. We
also designed the LC filter to have
a low output impedance of 2Ω.
Therefore, using
L = 159μH and C = 40μF,
w B`x√% (4-14)
∴ w B`xzBOu/PNu 1,995~ " 2~
Fig. 4.9 – Bode Plot of Second Order LC Filter
Source: John Brewer, Jr.
29
And,
% (4-15)
∴ BOu/PNu 1.99Ω ≅ 2Ω
4.4.1 Inductor Design
During the design process of the inductors for our inverter, we received
some much needed help from Jeff Brewer [2]. The most significant factor in the
inductor design process was the desired inductance and maximum amount of
current that would flow through an inductor during inverter operation.
Although the nominal output current of each inverter phase is 33A, we
designed the inductors for our inverter to be able to carry up to 50A. Based on the
equation for energy stored in an inductor, we needed to design inductors that could
each store
% = B
`` (4-16)
∴ QK \^ = B
`∗ 1595 ∗ 3506` = 0.19875 8
Then using
= `∗LV∗BNo
∗*∗* (4-17)
∴ = `∗N.BAsO∗BNo
ONNN∗P_A∗N.O= 34.2 4P
where
AP = area product in cm4.
30
Kj = the current density coefficient for a given core and a given
temperature rise.
Ku = the cross sectional area of copper to the total window area or packing
factor.
Bmax = the maximum flux density in Gauss.
from selecting an AMCC-50, size 10, PowerLite C-Core [2] [14] [15]. These PowerLite
cut C-cores are made out of Metglas iron alloy material and will not only make our
inductors easy to fabricate but also allow for fine tuning of inductance by adjusting
the air gap and using an Impedance Bridge
To determine the minimum number of turns, Nmin, and the length of air gap,
Lgap, needed in each leg of the cut C-core inductor, we used
%WH,∗BNt
∗$U (4-18)
∴ = BOu/∗ON$∗BNt
O,NNN∗@.`]n = 49 E18
where
L = Inductance of the inductor in microHenries.
IDC,max = Maximum current through the inductor in Amps.
Agap = Total cross sectional area of the air gap including fringing.
And
v =.`∗x∗$U∗BNn∗Zn
% (4-19)
∴ v = .`∗x∗@.`]n∗BNn∗Pn
BOu/= 0.304 1ℎ8.
31
Lastly, we determined that although making an inductor by wrapping
insulated Copper Foil around a Ferrite Core would result in lower core losses for the
beneficial design tradeoff of higher copper loss, it would be hard to fabricate for a
prototype. So, we chose 10AWG magnet wire with a heavy insulation build for
withstanding temperatures up to 200°C to wrap our AMCC-50 cores with [16]. We
were able to successfully wrap our inductor bobbins with 49 turns and connect two
bobbins in parallel, one on each inductor leg, for a generous inductor current
capacity of 50A.
In the next section of this report, we will discuss the construction phase of
our inverter project.
32
V.V.V.V. CONSTRUCTIONCONSTRUCTIONCONSTRUCTIONCONSTRUCTION
The construction and assembly phase of our proof-of-concept inverter
project consisted of six main parts – PWM Control Circuit assembly, Inductor
construction, Wire Harnesses, Connectors, and Cable fabrication, Power Plane
construction, Enclosure fabrication, and System assembly.
5.1 PWM Control Circuit Assembly
Before starting construction of the PWM Control Circuit, we used Windows
Paint to create scale drawings of our perforated circuit board (PerfBoard),
components, and ICs. We then copied these scale drawings into Microsoft
PowerPoint where we were then
able to freely move, place, label, and
“wire” components according to our
circuit design. Figure 5.1 shows a
part of our Circuit Board Layout.
To make connections on our
circuit board, we used a combination
of soldering and wire wrapping;
however, soldering was only used to solder short connections like decoupling
capacitors to IC pins while wire wrapping constitutes a majority of our connections.
Fig. 5.1 – Portion of Circuit Board Layout Graphic
Source: John Brewer, Jr.
33
A common prototype technique, wire wrapping uses a wire wrap tool to tightly wrap
30AWG Kynar wire around special wire wrap “posts.”
Using two PerfBoards, one on top of the other, provides a
much stronger circuit board to work with and helps keep
wire wrap posts straight. Figure 5.2 illustrates this
technique. For our proof-of-concept prototype, the design
and fabrication of a Printed Circuit Board (PCB) would not
have been cost effective and would have made circuit
modifications difficult.
5.2 Inductor Construction
To construct the inductors, we needed to wrap 10AWG enameled wire 49
times around the inductor bobbins shown in Figure 5.3. As shown in Figure 5.4, we
needed to guarantee that the wire was wrapped very tightly around each bobbin so
that two bobbins would fit on one core. In
order to prevent cracking a bobbin during
the wrapping process, Jeff Brewer
fabricated the wood handle shown in
Figure 5.5 to fit snugly inside each bobbin
as it was wound.
Fig. 5.2 – Wire Wrapping
Source: John Brewer, Jr.
Fig. 5.3 – Inductor Bobbin
Source: John Brewer, Jr.
34
When it was time to put two wire-wrapped
bobbins on a core, we used the right-hand-rule to
determine the orientation of the bobbins on the
core to guarantee that the flux induced by the
coiled wire on each bobbin was flowing through
the core in the same direction. Using an
Impedance Bridge, we adjusted the air gap of
each inductor to obtain our desired inductance at 2kHz – 159μH. We then used
small squares of PerfBoard as spacers inside the bobbins between the core halves to
maintain the necessary air
gap of each inductor.
Using a sharp edge,
we scraped about an inch of enamel coating from each end of the wires to be
connected. Lastly, we crimped and soldered them to a connector and wrapped up
the inductor using high-
temperature Mylar tape
as shown in Figure 5.6.
Fig. 5.5 – Wood Handle to Support Bobbin
Source: John Brewer, Jr.
Fig. 5.4 – Tightly Wound Inductor
Source: John Brewer, Jr.
Fig. 5.6 – Finished Inductor with Connectors and Mylar Tape
Source: John Brewer, Jr.
35
5.3 Wire Harnesses, Connectors, and Cable Fabrication
In order to simplify the assembly, transportation, testing, and modification
process, we designed and fabricated the following wire harnesses, connectors, and
cables:
• For signals and voltages delivered to our circuit board from the function
generator and low-voltage bias power supply jacks, we wired, soldered, and
applied heat-shrink to the 15-pin D-sub connector shown in Figure 5.7.
• To connect to the function generator 8-pin inline header output pins, we
used the mating female crimp contact receptacle also shown in Figure 5.7.
• To connect to the output enable switch voltages from the front panel of our
enclosure, we used a 10-pin inline header with mating crimp contact
receptacle also shown
in Figure 5.7.
• To connect the DC
Input Voltages to our
Input Capacitors and
Power Planes, we used
three parallel lines of
stranded 10AWG wire with crimp/ring connectors.
Fig. 5.7 – Fabricated Wire Harnesses
Source: John Brewer, Jr.
36
• To connect output voltage nodes from the copper-clad circuit board to the
inductors and the LC output filters to the enclosure panel, we used stranded
10AWG wire with crimp/ring connectors. These ring connectors in
conjunction with nuts, bolts, washers, and lock washers made it quick to
assemble and disassemble our prototype for modifications.
5.4 Power Plane Construction
In order to effectively reduce parasitic inductances in the DC Input Voltage
supply path, we used double-sided copper-clad board for the ±input voltage
delivered to the IGBTs. We used a combination of precise cutting and drilling to
create isolated copper pads with at
least a 3:1 ratio of length to width for
current flow. A section of both the
top and bottom power planes are
shown in Figure 5.8.
5.5 Enclosure Fabrication
For ease of transportation,
setup, and testing of our inverter
prototype, Jaime Carmo generously donated his time and materials to fabricate a
Plexiglas enclosure for us. This enclosure allowed us to effectively and efficiently
mount all of our system components and display our project for exhibition.
Fig. 5.8 – Top and Bottom Sides of Copper-Clad Board
Source: John Brewer, Jr.
37
5.6 System Assembly
System assembly consisted of placing and arranging system components,
drilling mounting holes in the Plexiglas enclosure, and fastening components
together or to the enclosure with wire ties, circuit board standoffs, nuts, bolts,
washers, and lock washers. Our final System Assembly is shown in Figure 5.9.
Fig. 5.9 – Inverter System Assembly
Source: John Brewer, Jr.
38
VI.VI.VI.VI. TESTINGTESTINGTESTINGTESTING
For our project, we performed several stages of testing – Ideal Inverter
Pspice simulation, IGBT Gate Driver and Half-Bridge Pspice simulation, PWM Control
Circuit hardware testing, PWM Control Circuit and single IGBT Half-Bridge hardware
low power testing, and full system testing.
For the Ideal Inverter Pspice simulation, we simulated an open-loop
switched-mode single phase PWM inverter circuit with Neutral phase using ideal
components as shown in Figure 6.1 to obtain the output sinusoidal waveform shown
in Figure 6.2.
Fig. 6.1 – Ideal Inverter Pspice Simulation
Source: John Brewer, Jr.
39
For the IGBT Gate Driver and Half-Bridge Pspice simulation shown in
Figure 6.3, we simulated an IR2113 Gate Driver and IRGP50B60PD1 Half-Bridge
driven with a 40kHz, 50% duty cycle square wave with 1μs of deadtime programmed
in between high-side and low-side switching. Despite not being able to use the
Si8234BB IGBT gate driver in our simulation, we were still able to analyze the
bootstrap power supply topology used to turn the high-side IGBT on. The gate-to-
Time
45.0ms 45.5ms 46.0ms 46.5ms 47.0ms 47.5ms 48.0ms 48.5ms 49.0ms 49.5ms 50.0msV(R_LOAD:1)- V(R_LOAD:2)
-120V
-80V
-40V
-0V
40V
80V
120V
Fig. 6.2 – Output Voltage Waveform of Ideal Inverter Simulation
Source: John Brewer, Jr.
Fig. 6.3 – IGBT Gate Driver and Half-Bridge Pspice Simulation
Source: John Brewer, Jr.
40
emitter voltage waveforms
and output current waveform
are shown in Figure 6.4.
We tried to limit the
time spent developing and
analyzing the Pspice
simulations for our inverter
project because it was difficult
to accurately model all of the
parasitic elements that would
affect the high-power performance of our hardware design in the end.
Concurrently, our detail-oriented approach to the design of the PWM Control Circuit
and the thorough analysis of the aforementioned design tips and application notes
published by International Rectifier and Silicon Labs regarding HVIC Gate Drivers and
the bootstrap supply topology warranted immediate prototyping and hardware
testing.
As a result, we constructed a prototype of our PWM Control Circuit design,
tested it, and observed successful results. Because we implemented resistance
trimmers at critical points in the circuit, we were able to fully tune the prototype
design. Next, we constructed a low-power single phase prototype of the IGBT Gate
Driver with bootstrap supply and Half-Bridge topology. At this point in the testing,
0s 5us 10us 15us 20us 25us 30usV(U2:2)- V(U2:3) V(U3:2)- V(U3:3)
-10V
0V
10V
20V
SEL>>
I(Rload)-20A
0A
20A
40A
Fig. 6.4 – High-side (green) and low-side (blue) IGBT
gate-to-emitter voltage waveforms. Load
current waveform (top).
Source: John Brewer, Jr.
41
we encountered problems regarding bias supply ground referencing, low-side
decoupling capacitor sizing, and gate resistance sizing which caused us to take a
closer look at IR’s design notes and modify our circuit design. After doing so, our
testing yielded successful results for low-power switching of our IGBTs using ±39VDC
input supply and less than 1A output current.
After completing assembly of the final version of our proof-of-concept three-
phase inverter design, we performed full system tests. Due to a miscommunication
during a discussion about the DC Power available for testing in Cal Poly’s EE labs, we
were only able to test all three-phases of our inverter with a ±DC input supply
voltage of ±48V due to test equipment voltage and current limits. However, these
tests were all successful.
After powering-up the PWM Control Circuit with the inverter outputs
disabled, we turned on each phase and gradually increased the ±DC input supply
voltage while monitoring all node voltages on the high-voltage side of our circuit –
IGBT Gate Driver pin voltages, IGBT gate, collector, and emitter voltages, supply
voltages, and output voltage. After reaching test equipment current limits, we
reported the following about Figure 6.5 through Figure 6.10:
Fig. 6.5 – Adjustable Three
38kHz Triangle Wave successfully generated and compared wi
signals to produce three
Fig. 6.6 – Trigger Pulse successfully generated by AD823AN Op
Three-Phase Sinusoidal Reference signals successfully generated, UC3637
38kHz Triangle Wave successfully generated and compared with Sinusoidal Reference
signals to produce three-phase PWM Control Input signals.
ger Pulse successfully generated by AD823AN Op-Amp Comparator.
42
signals successfully generated, UC3637
th Sinusoidal Reference
Amp Comparator.
Fig. 6.7 – Square wave with 97% duty cycle successfully generated by Trigger Pulse and HCF4538B
One-Shot.
Fig. 6.8 – Three-phase and Neutral
generated.
Square wave with 97% duty cycle successfully generated by Trigger Pulse and HCF4538B
phase and Neutral-phase Duty Cycle limited PWM Control Input sign
43
Square wave with 97% duty cycle successfully generated by Trigger Pulse and HCF4538B
Duty Cycle limited PWM Control Input signals successfully
Fig. 6.9 –Three-phase Inverter Output Voltage referenced to supply ground with ±48VDC Input
Voltage. Output voltage is 87 V
current is supply limit of 6.5 A.
Fig. 6.10 –Three-phase Inverter Output Voltage reference
Voltage. Output voltage is 86 V
supply limit of 6.5 A.
phase Inverter Output Voltage referenced to supply ground with ±48VDC Input
Voltage. Output voltage is 87 VP-P, 61 VRMS. Output RMS current is 6.2 A. Input RMS
current is supply limit of 6.5 A.
phase Inverter Output Voltage referenced to virtual ground with ±46VDC Input
Voltage. Output voltage is 86 VP-P, 61 VRMS. Output RMS current is 6.2 A. Input RMS current is
44
phase Inverter Output Voltage referenced to supply ground with ±48VDC Input
. Output RMS current is 6.2 A. Input RMS
to virtual ground with ±46VDC Input
. Output RMS current is 6.2 A. Input RMS current is
45
VII.VII.VII.VII. CONCLUSIONCONCLUSIONCONCLUSIONCONCLUSIONSSSS AND RECOMMENDATIONSAND RECOMMENDATIONSAND RECOMMENDATIONSAND RECOMMENDATIONS
Designing and fabricating a proof-of-concept high-voltage switched-mode
three-phase inverter capable of supplying 10kW covered a multitude of design
processes and proved to be a challenging endeavor. However, ensuring that a
detail-oriented approach was taken in the research, design, construction, and testing
stages of this project contributed to its successful completion and thorough
presentation in this report. While the original requirements for this project were
not met due to limitations in lab test equipment, observed test results yielded
successful system performance at lower power levels than intended for nominal
operation. Continued development of the proof-of-concept inverter system that has
been designed and fabricated for this project will assuredly lead to a production-
level version with closed-loop feedback and possibly the following
recommendations.
Given the relatively high-current output capabilities of the Si8234BB HVIC
IGBT Gate Driver, up to two more IGBTs can be placed in parallel with each high-side
and low-side IGBT in the power stage to increase the system current output
capability while maintaining suitable IGBT switching transition times. However,
limitations to this increase in current output capability will rise from parasitic
inductance in the supply current path and action will be necessary to protect against
46
transient voltages. Limitations will also rise from the inability to sufficiently cool
IGBTs while minimizing parasitic inductance by maintaining close IGBT proximity.
The development of a floating supply to replace the bootstrap supply
topology designed for this project would eliminate the duty cycle limitations on the
high-side IGBT. A floating supply able to be ground referenced to the switching
output of the half-bridge would provide for unlimited high-side IGBT on time under
closed-loop control.
Development of a digital microprocessor-based PWM Control system could
potentially reduce the amount of space required by the PWM Control block and
allow for more versatile or accurate control performance. A digital PWM control
system could also have improved noise immunity and temperature tolerance.
If analog PWM control is desired, the design of a well laid-out surface mount
technology PCB is recommended. The signal voltages of the analog system designed
for this project could then be reduced for faster edge transitions so long as the
control circuit is effectively protected from noise and electromagnetic interference
(EMI).
As mention in Section 4.2.3.1, using a ferrite core wrapped with insulated
copper foil for the system inductors would result in lower core and copper losses
than the inductors in the current proof-of-concept system exhibit. This would
decrease the amount of cooling required by the inductors which would increase the
system quality.
47
Having made these recommendations, we maintain that the High-Voltage
Switched-Mode Power Supply for Three-Phase AC Aircraft Systems that we have
designed for this senior project presented to the Electrical Engineering faculty at
California Polytechnic State University, San Luis Obispo will fulfill the requirements
set by the sponsor, Jeff Brewer, after proper high-power testing, tuning, and no
significant design changes have been made.
48
VIII.VIII.VIII.VIII. BIBLIOGRAPHYBIBLIOGRAPHYBIBLIOGRAPHYBIBLIOGRAPHY
[1] Power Semiconductor Device,
http://en.wikipedia.org/wiki/Power_semiconductor_device,
Accessed June 4, 2010.
[2] Brewer, John (Jeff), Director of Electrical Engineering, Aircraft Systems Group,
General Atomics Aeronautical Systems, Inc. Interview.
[3] MIL-STD-704F,
http://www.wbdg.org/ccb/FEDMIL/std704f.pdf,
Accessed June 5, 2010.
[4] International Rectifier Datasheet PD-94625B,
http://www.irf.com/product-info/datasheets/data/irgp50b60pd1.pdf,
Accessed June 6, 2010.
[5] Silicon Labs Datasheet Si8234x,
http://www.silabs.com/Support%20Documents/TechnicalDocs/Si823x.pdf,
Accessed June 7, 2010.
[6] International Rectifier Design Tips DT04-4 Rev A,
http://www.irf.com/technical-info/designtp/dt04-4.pdf,
Accessed June 7, 2010.
[7] ON Semiconductor Datasheet MUR460,
http://www.onsemi.com/pub_link/Collateral/MUR420-D.PDF,
Accessed June 7, 2010.
[8] Unitrode Datasheet UC3637,
http://focus.ti.com/lit/ds/symlink/uc1637.pdf,
Accessed June 7, 2010.
49
[9] Unitrode Design Note DN-53A,
http://focus.tij.co.jp/jp/lit/an/slua184/slua184.pdf,
Accessed June 7, 2010.
[10] Unitrode Application Note U-102,
http://focus.ti.com/lit/an/slua137/slua137.pdf,
Accessed June 7, 2010.
[11] Analog Devices Datasheet AD823AN,
http://www.analog.com/static/imported-files/data_sheets/AD823.pdf,
Accessed June 7, 2010.
[12] STMicroelectronics Datasheet HCF4538B,
http://www.st.com/stonline/books/pdf/docs/2089.pdf,
Accessed June 7, 2010.
[13] Fairchild Semiconductor Datasheet 74AC00,
http://www.fairchildsemi.com/ds/74%2F74AC00.pdf,
Accessed June 7, 2010.
[14] McLyman, Colonel Wm. T. Transformer and Inductor Design Handbook.
Marcel Dekker Inc., Monticello, New York. 2004
[15] PowerLite C-Cores,
http://www.metglas.com/downloads/powerlite.pdf,
Accessed June 8, 2010.
[16] Applied Magnets AWG10-11,
http://www.magnet4less.com/product_info.php?products_id=175,
Accessed June 8, 2010.
50
APPENDICESAPPENDICESAPPENDICESAPPENDICES
A. Schematic
The following pages, 51 through 65, contain the Three-Phase Sinusoidal Inverter
schematic generated for this project.
5 5
4 4
3 3
2 2
1 1
DD
CC
BB
AA
THREE PHASE INVERTER
NOTES: UNLESS OTHERWISE SPECIFIED
CONTENTS
1. ALL RESISTORS ARE 1/8W, 1%
2. ALL CAPACITORS ARE 10%, 50V.
TABLE OF CONTENTS
1 2 3 4 5 6 7
IO CONNECTORS
SIGNAL BUFFERING
NEUTRAL PWM
PHASE-A PWM
PHASE-B PWM
PHASE-C PWM
8
10 11
12
13
14
15
PWM LIMIT LOGIC
PHASE-A GATE DRIVER
9
PWM LIMIT TIMING
PWM LIMIT LOGIC
PHASE-B GATE DRIVER
PHASE-C GATE DRIVER
NEUTRAL GATE DRIVER
OUTPUT FILTERS
Eng
inee
r: J
. BR
EW
ER
, JR
.
Siz
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ev
Dat
e:S
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of
A
115
Sun
day,
Jun
e 06
, 201
0
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CH
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of
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115
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of
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115
Sun
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0
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CH
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5 5
4 4
3 3
2 2
1 1
DD
CC
BB
AA
IO CONNECTORS
THREE PHASE INVERTER
J2
1 9 2 3 10
4 11
5 6 13
7 14
8 15
12
SPARE
SPARE
J1
1 2 3 4 5 6 7 8 9 10
NC
Eng
inee
r: J
. BR
EW
ER
, JR
.
DG
ND
+5V
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TN
5V_R
TN
+15
V-1
5V+
5V15
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TN
5V_R
TN
12V
_RT
N
DG
ND
-190
V_S
UP
PLY
SIN
_A
[3]
SIN
_B
[3]
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_C
[3]
+5V
+5V
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D_S
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H
[16]
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N_S
D_S
WC
H
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4,15
]
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215
Sun
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, 201
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215
Sun
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215
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5 5
4 4
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CC
BB
AA
SIGNAL BUFFERING
THREE PHASE INVERTER
Eng
inee
r: J
. BR
EW
ER
, JR
.
+15
V
-15V
+15
V
-15V
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ND
15V
_RT
N
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ND
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DG
ND
15V
_RT
N
15V
_RT
N
+15
V
15V
_RT
N
-15V
15V
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N
+15
V
15V
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N
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+15
V
+15
V
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-15V
[2]
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_A
SIN
_A_B
UF
[5
]
[2]
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_B
SIN
_B_B
UF
[6
]
TR
I_B
UF
[5
,6,7
,9]
[4]
TR
I_W
AV
E
[2]
SIN
_C
SIN
_C_B
UF
[7
]
Siz
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ev
Dat
e:S
heet
of
A
315
Mon
day,
Jun
e 07
, 201
0
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CH
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AT
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315
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315
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5 5
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CC
BB
AA
MASTER PWM
THREE PHASE INVERTER
Eng
inee
r: J
. BR
EW
ER
, JR
.-1
5V
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15V
_RT
N
+15
V
15V
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N
15V
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N
15V
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N
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V
+15
V
15V
_RT
N
+15
V
-15V
15V
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N
TR
I_W
AV
E
[3]
NE
UT
RA
L_P
WM
[1
1]
SLV
_TH
RS
H+
[5
,6,7
,9]
SLV
_TH
RS
H-
[5,
6,7,
9]
PW
M_U
VLO
[5
,6,7
]
Siz
eD
ocum
ent N
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rR
ev
Dat
e:S
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of
A
415
Mon
day,
Jun
e 07
, 201
0
ES
CH
EM
AT
IC, T
HR
EE
PH
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Dat
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of
A
415
Mon
day,
Jun
e 07
, 201
0
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CH
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HR
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of
A
415
Mon
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Jun
e 07
, 201
0
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CH
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HR
EE
PH
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ER
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kR
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CC
BB
AA
PHASE-A PWM
THREE PHASE INVERTER
Eng
inee
r: J
. BR
EW
ER
, JR
.
+15
V
15V
_RT
N
-15V
15V
_RT
N15
V_R
TN
15V
_RT
N15
V_R
TN
[4]
SLV
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RS
H+
[4]
SLV
_TH
RS
H-
[3]
TR
I_B
UF
A_P
WM
[1
0]
[4]
PW
M_U
VLO
[3]
SIN
_A_B
UF
Siz
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ocum
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ev
Dat
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of
A
515
Mon
day,
Jun
e 07
, 201
0
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CH
EM
AT
IC, T
HR
EE
PH
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E IN
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Siz
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ev
Dat
e:S
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of
A
515
Mon
day,
Jun
e 07
, 201
0
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CH
EM
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HR
EE
PH
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Siz
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ev
Dat
e:S
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of
A
515
Mon
day,
Jun
e 07
, 201
0
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CH
EM
AT
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HR
EE
PH
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RT
ER
C20
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3637
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2
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10
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9
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UT
4
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UT
7
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14
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1
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5 5
4 4
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DD
CC
BB
AA
PHASE-B PWM
THREE PHASE INVERTER
Eng
inee
r: J
. BR
EW
ER
, JR
.
+15
V
15V
_RT
N
-15V
15V
_RT
N15
V_R
TN
15V
_RT
N15
V_R
TN
[4]
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RS
H+
[4]
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RS
H-
[3]
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I_B
UF
B_P
WM
[1
0]
[4]
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M_U
VLO
[3]
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_B_B
UF
Siz
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Dat
e:S
heet
of
A
615
Mon
day,
Jun
e 07
, 201
0
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CH
EM
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IC, T
HR
EE
PH
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Dat
e:S
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of
A
615
Mon
day,
Jun
e 07
, 201
0
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CH
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HR
EE
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Siz
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Dat
e:S
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of
A
615
Mon
day,
Jun
e 07
, 201
0
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HR
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PH
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C28
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5 5
4 4
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DD
CC
BB
AA
PHASE-C PWM
THREE PHASE INVERTER
Eng
inee
r: J
. BR
EW
ER
, JR
.
+15
V
15V
_RT
N
-15V
15V
_RT
N15
V_R
TN
15V
_RT
N15
V_R
TN
[4]
SLV
_TH
RS
H+
[4]
SLV
_TH
RS
H-
[3]
TR
I_B
UF
C_P
WM
[1
1]
[4]
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M_U
VLO
[3]
SIN
_C_B
UF
Siz
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Dat
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of
A
715
Mon
day,
Jun
e 07
, 201
0
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CH
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HR
EE
PH
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Dat
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of
A
715
Mon
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Jun
e 07
, 201
0
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PH
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Siz
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Dat
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of
A
715
Mon
day,
Jun
e 07
, 201
0
ES
CH
EM
AT
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HR
EE
PH
AS
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RT
ER
C31
0.1u
FC
310.
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C30
0.1u
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300.
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F
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UT
7
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5 5
4 4
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2 2
1 1
DD
CC
BB
AA
PWM LIMIT TIMING
THREE PHASE INVERTER
16 8
6 10
1 2 3 4 5 11 12 13 14 15
7 9
Cx(
1)
RxC
x(1)
RE
SE
T(1
)
+T
R(1
)
-TR
(1)
-TR
(2)
+T
R(2
)
RE
SE
T(2
)
RxC
x(2)
Cx(
2)V
ss
VD
D
Q1
Q1/
Q2
Q2/
HC
F45
38B
U8
Eng
inee
r: J
. BR
EW
ER
, JR
.
+15
V
+15
V
15V
_RT
N
+15
V
15V
_RT
N
15V
_RT
N
15V
_RT
N
+15
V
-15V
-15V
15V
_RT
N
-15V
15V
_RT
N
15V
_RT
N
DU
TY
_LIM
IT
[10,
11]
[4]
SLV
_TH
RS
H+
[3]
TR
I_B
UF
Siz
eD
ocum
ent N
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ev
Dat
e:S
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of
A
815
Mon
day,
Jun
e 07
, 201
0
ES
CH
EM
AT
IC, T
HR
EE
PH
AS
E IN
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RT
ER
Siz
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Dat
e:S
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of
A
815
Mon
day,
Jun
e 07
, 201
0
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CH
EM
AT
IC, T
HR
EE
PH
AS
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Siz
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ev
Dat
e:S
heet
of
A
815
Mon
day,
Jun
e 07
, 201
0
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CH
EM
AT
IC, T
HR
EE
PH
AS
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RT
ER
R21
1.0k
R21
1.0k
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103A
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SD
103A
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823A
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pFC
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1/4W
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FC
360.
1uF
C35
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FC
350.
1uF
5 5
4 4
3 3
2 2
1 1
DD
CC
BB
AA
PWM LIMIT LOGIC
THREE PHASE INVERTER
Eng
inee
r: J
. BR
EW
ER
, JR
.
15V
_RT
N
15V
_RT
N
15V
_RT
N
15V
_RT
N
+5V
5V_R
TN
15V
_RT
N
15V
_RT
N
[9]
DU
TY
_LIM
IT
[5]
A_P
WM
A_D
RIV
E
[14]
B_D
RIV
E
[15]
[9]
DU
TY
_LIM
IT
[6]
B_P
WM
Siz
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ocum
ent N
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ev
Dat
e:S
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of
A
915
Sun
day,
Jun
e 06
, 201
0
ES
CH
EM
AT
IC, T
HR
EE
PH
AS
E IN
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RT
ER
Siz
eD
ocum
ent N
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rR
ev
Dat
e:S
heet
of
A
915
Sun
day,
Jun
e 06
, 201
0
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CH
EM
AT
IC, T
HR
EE
PH
AS
E IN
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RT
ER
Siz
eD
ocum
ent N
umbe
rR
ev
Dat
e:S
heet
of
A
915
Sun
day,
Jun
e 06
, 201
0
ES
CH
EM
AT
IC, T
HR
EE
PH
AS
E IN
VE
RT
ER
R24
10.2
k
R24
10.2
k
C40
0.1u
FC
400.
1uF
R23
10.2
k
R23
10.2
k
U9D
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12 1311
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103A
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SD
103A
R28
10.2
k
R28
10.2
k
R26
20.5
k
R26
20.5
k
R25
10.2
kR
2510
.2k
U9B
74A
C00
U9B
74A
C00
4 56
R27
10.2
kR
2710
.2k
D3
SD
103A
D3
SD
103A
U9C
74A
C00
U9C
74A
C00
9 108
R31
20.5
k
R31
20.5
k
R29
10.2
k
R29
10.2
k
U9A
74A
C00
U9A
74A
C00
1 23
R32
10.2
kR
3210
.2k
R30
10.2
kR
3010
.2k
5 5
4 4
3 3
2 2
1 1
DD
CC
BB
AA
PWM LIMIT LOGIC
THREE PHASE INVERTER
Eng
inee
r: J
. BR
EW
ER
, JR
.
15V
_RT
N
15V
_RT
N
15V
_RT
N
15V
_RT
N
+5V
5V_R
TN
15V
_RT
N
15V
_RT
N
[9]
DU
TY
_LIM
IT
[9]
DU
TY
_LIM
IT
[7]
C_P
WM
[4]
NE
UT
RA
L_P
WM
C_D
RIV
E
[16]
NE
UT
RA
L_D
RIV
E
[17]
Siz
eD
ocum
ent N
umbe
rR
ev
Dat
e:S
heet
of
A
1015
Sun
day,
Jun
e 06
, 201
0
ES
CH
EM
AT
IC, T
HR
EE
PH
AS
E IN
VE
RT
ER
Siz
eD
ocum
ent N
umbe
rR
ev
Dat
e:S
heet
of
A
1015
Sun
day,
Jun
e 06
, 201
0
ES
CH
EM
AT
IC, T
HR
EE
PH
AS
E IN
VE
RT
ER
Siz
eD
ocum
ent N
umbe
rR
ev
Dat
e:S
heet
of
A
1015
Sun
day,
Jun
e 06
, 201
0
ES
CH
EM
AT
IC, T
HR
EE
PH
AS
E IN
VE
RT
ER
R36
20.5
k
R36
20.5
k
U10
C
74A
C00
U10
C
74A
C00
9 108
R33
10.2
k
R33
10.2
k
R37
10.2
kR
3710
.2k
R39
10.2
k
R39
10.2
kR
4010
.2k
R40
10.2
k
R41
20.5
k
R41
20.5
k
U10
D
74A
C00
U10
D
74A
C00
12 1311
D4
SD
103A
D4
SD
103A
R42
10.2
kR
4210
.2k
U10
A
74A
C00
U10
A
74A
C00
1 23
R38
10.2
k
R38
10.2
k
R35
10.2
kR
3510
.2k
D5
SD
103A
D5
SD
103A
C41
0.1u
FC
410.
1uF
U10
B
74A
C00
U10
B
74A
C00
4 56
R34
10.2
k
R34
10.2
k
5 5
4 4
3 3
2 2
1 1
DD
CC
BB
AA
PHASE-A GATE DRIVER
THREE PHASE INVERTER
6
10
4 5
11121314
7
9
DIS
AB
LE
DT
NC
VD
DI
GN
DI
GN
DB
Si8
234B
B
U11
1 2 3 8
1516P
WM
NC
VD
DI
VO
B
VD
DB
NC
NC
GN
DA
VO
A
VD
DA
Eng
inee
r: J
. BR
EW
ER
, JR
.
+5V
5V_R
TN
15V
_RT
N
+15
V
+19
0V
-190
V15
V_R
TN
+15
V
5V_R
TN
[2]
A_B
_SD
_SW
CH
PH
AS
E_A
[1
8]
[10]
A
_DR
IVE
Siz
eD
ocum
ent N
umbe
rR
ev
Dat
e:S
heet
of
A
1115
Mon
day,
Jun
e 07
, 201
0
ES
CH
EM
AT
IC, T
HR
EE
PH
AS
E IN
VE
RT
ER
Siz
eD
ocum
ent N
umbe
rR
ev
Dat
e:S
heet
of
A
1115
Mon
day,
Jun
e 07
, 201
0
ES
CH
EM
AT
IC, T
HR
EE
PH
AS
E IN
VE
RT
ER
Siz
eD
ocum
ent N
umbe
rR
ev
Dat
e:S
heet
of
A
1115
Mon
day,
Jun
e 07
, 201
0
ES
CH
EM
AT
IC, T
HR
EE
PH
AS
E IN
VE
RT
ER
C45
0.1u
FC
450.
1uF
R45 4.
7
R45 4.
7
D8
MU
R46
0D
8M
UR
460
D6
MU
R46
0D
6M
UR
460
C49
0.1u
FC
490.
1uF
16V
D10
16V
D10
C48
10uF
C48
10uF
C46
0.33
uFC
460.
33uF
U12
IRG
P50
B60
PD
1
U12
IRG
P50
B60
PD
1
11
22
33
R43
100k
1/4W
R43
100k
1/4W
C43
0.1u
FC
430.
1uF
16V
D9
16V
D9
C47
0.33
uFC
470.
33uF
U13
U13
11
22
33
C82
0.33
uFC
820.
33uF
16V
D7
16V
D7
C44
10uF
C44
10uF
R44 3.
9
R44 3.
9
C42
0.1u
F
C42
0.1u
F
C86
0.1u
FC
860.
1uF
5 5
4 4
3 3
2 2
1 1
DD
CC
BB
AA
PHASE-B GATE DRIVER
THREE PHASE INVERTER
Eng
inee
r: J
. BR
EW
ER
, JR
.
21 83
16 15N
C
PW
M
VO
B
VD
DI
NC
VD
DB
GN
DA
NC
VD
DA
VO
A
10
611
5413 1214
7
9
DT
DIS
AB
LE
NC
GN
DI
VD
DI
GN
DB
U14
Si8
234B
B
+5V
5V_R
TN
15V
_RT
N
+15
V
+19
0V
-190
V15
V_R
TN
+15
V
5V_R
TN
[2]
A_B
_SD
_SW
CH
PH
AS
E_B
[1
8]
[10]
B
_DR
IVE
Siz
eD
ocum
ent N
umbe
rR
ev
Dat
e:S
heet
of
A
1215
Mon
day,
Jun
e 07
, 201
0
ES
CH
EM
AT
IC, T
HR
EE
PH
AS
E IN
VE
RT
ER
Siz
eD
ocum
ent N
umbe
rR
ev
Dat
e:S
heet
of
A
1215
Mon
day,
Jun
e 07
, 201
0
ES
CH
EM
AT
IC, T
HR
EE
PH
AS
E IN
VE
RT
ER
Siz
eD
ocum
ent N
umbe
rR
ev
Dat
e:S
heet
of
A
1215
Mon
day,
Jun
e 07
, 201
0
ES
CH
EM
AT
IC, T
HR
EE
PH
AS
E IN
VE
RT
ER
16V
D14
16V
D14
C83
0.33
uFC
830.
33uF
16V
D16
16V
D16
C50
0.1u
F
C50
0.1u
F
C56
10uF
C56
10uF
D15
MU
R46
0D
15M
UR
460
C88
0.1u
FC
880.
1uF
C53
0.1u
FC
530.
1uF C
550.
33uF
C55
0.33
uF
U15
IRG
P50
B60
PD
1
U15
IRG
P50
B60
PD
1
11
22
33
R46
100k
1/4W
R46
100k
1/4W
C51
0.1u
FC
510.
1uF
C52
10uF
C52
10uF
R47 3.
9
R47 3.
9
U16
U16
11
22
33
R48 4.
7
R48 4.
7
C57
0.1u
FC
570.
1uF
C54
0.33
uFC
540.
33uF
16V
D17
16V
D17
D13
MU
R46
0D
13M
UR
460
5 5
4 4
3 3
2 2
1 1
DD
CC
BB
AA
PHASE-C GATE DRIVER
THREE PHASE INVERTER
Eng
inee
r: J
. BR
EW
ER
, JR
.
21 83
16 15N
C
PW
M
VO
B
VD
DI
NC
VD
DB
GN
DA
NC
VD
DA
VO
A
10
611
5413 1214
7
9
DT
DIS
AB
LE
NC
GN
DI
VD
DI
GN
DB
U17
Si8
234B
B
+5V
5V_R
TN
15V
_RT
N
+15
V
+19
0V
-190
V15
V_R
TN
+15
V
5V_R
TN
[2]
C_S
D_S
WC
H
PH
AS
E_C
[1
8]
[11]
C
_DR
IVE
Siz
eD
ocum
ent N
umbe
rR
ev
Dat
e:S
heet
of
A
1315
Mon
day,
Jun
e 07
, 201
0
ES
CH
EM
AT
IC, T
HR
EE
PH
AS
E IN
VE
RT
ER
Siz
eD
ocum
ent N
umbe
rR
ev
Dat
e:S
heet
of
A
1315
Mon
day,
Jun
e 07
, 201
0
ES
CH
EM
AT
IC, T
HR
EE
PH
AS
E IN
VE
RT
ER
Siz
eD
ocum
ent N
umbe
rR
ev
Dat
e:S
heet
of
A
1315
Mon
day,
Jun
e 07
, 201
0
ES
CH
EM
AT
IC, T
HR
EE
PH
AS
E IN
VE
RT
ER
C63
0.33
uFC
630.
33uF
U18
IRG
P50
B60
PD
1
U18
IRG
P50
B60
PD
1
11
22
33
C59
0.1u
FC
590.
1uF
C60
10uF
C60
10uF
R50 3.
9
R50 3.
9
U19
U19
11
22
33
R51 4.
7
R51 4.
7
C65
0.1u
FC
650.
1uF
C89
0.1u
FC
890.
1uF
C62
0.33
uFC
620.
33uF
16V
D24
16V
D24
D20
MU
R46
0D
20M
UR
460
16V
D21
16V
D21
16V
D23
16V
D23
C84
0.33
uFC
840.
33uF
C58
0.1u
F
C58
0.1u
F
R49
100k
1/4W
R49
100k
1/4W
C64
10uF
C64
10uF
D22
MU
R46
0D
22M
UR
460
C61
0.1u
FC
610.
1uF
5 5
4 4
3 3
2 2
1 1
DD
CC
BB
AA
NEUTRAL GATE DRIVER
THREE PHASE INVERTER
Eng
inee
r: J
. BR
EW
ER
, JR
.
21 83
16 15N
C
PW
M
VO
B
VD
DI
NC
VD
DB
GN
DA
NC
VD
DA
VO
A
10
611
5413 1214
7
9
DT
DIS
AB
LE
NC
GN
DI
VD
DI
GN
DB
U21
Si8
234B
B
+5V
5V_R
TN
15V
_RT
N
+15
V
+19
0V
-190
V15
V_R
TN
+15
V
5V_R
TN
[2]
N_S
D_S
WC
H
NE
UT
RA
L [
18]
[11]
N
EU
TR
AL_
DR
IVE
Siz
eD
ocum
ent N
umbe
rR
ev
Dat
e:S
heet
of
A
1415
Mon
day,
Jun
e 07
, 201
0
ES
CH
EM
AT
IC, T
HR
EE
PH
AS
E IN
VE
RT
ER
Siz
eD
ocum
ent N
umbe
rR
ev
Dat
e:S
heet
of
A
1415
Mon
day,
Jun
e 07
, 201
0
ES
CH
EM
AT
IC, T
HR
EE
PH
AS
E IN
VE
RT
ER
Siz
eD
ocum
ent N
umbe
rR
ev
Dat
e:S
heet
of
A
1415
Mon
day,
Jun
e 07
, 201
0
ES
CH
EM
AT
IC, T
HR
EE
PH
AS
E IN
VE
RT
ER
R53 3.
9
R53 3.
9
U22
U22
11
22
33
R52
100k
1/4W
R52
100k
1/4W
R54 4.
7
R54 4.
7
C73
0.1u
FC
730.
1uF
C70
0.33
uFC
700.
33uF
16V
D31
16V
D31
D27
MU
R46
0D
27M
UR
460
C85
0.33
uFC
850.
33uF
16V
D28
16V
D28
16V
D30
16V
D30
C66
0.1u
F
C66
0.1u
F
C72
10uF
C72
10uF
D29
MU
R46
0D
29M
UR
460
C69
0.1u
FC
690.
1uF C
710.
33uF
C71
0.33
uF
U21
IRG
P50
B60
PD
1
U21
IRG
P50
B60
PD
1
11
22
33
C67
0.1u
FC
670.
1uF
C90
0.1u
FC
900.
1uF
C68
10uF
C68
10uF
5 5
4 4
3 3
2 2
1 1
DD
CC
BB
AA
OUTPUT FILTERS
THREE PHASE INVERTER
Eng
inee
r: J
. BR
EW
ER
, JR
.
-190
V
+19
0V
PW
R_G
ND
PW
R_G
ND
PW
R_G
ND
PW
R_G
ND
SIN
_A_O
UT
SIN
_B_O
UT
SIN
_C_O
UT
[14]
P
HA
SE
_A
[15]
P
HA
SE
_B
[16]
P
HA
SE
_C
[17]
N
EU
TR
AL
Siz
eD
ocum
ent N
umbe
rR
ev
Dat
e:S
heet
of
A
1515
Sun
day,
Jun
e 06
, 201
0
ES
CH
EM
AT
IC, T
HR
EE
PH
AS
E IN
VE
RT
ER
Siz
eD
ocum
ent N
umbe
rR
ev
Dat
e:S
heet
of
A
1515
Sun
day,
Jun
e 06
, 201
0
ES
CH
EM
AT
IC, T
HR
EE
PH
AS
E IN
VE
RT
ER
Siz
eD
ocum
ent N
umbe
rR
ev
Dat
e:S
heet
of
A
1515
Sun
day,
Jun
e 06
, 201
0
ES
CH
EM
AT
IC, T
HR
EE
PH
AS
E IN
VE
RT
ER
C80
3300
uF35
0V
C80
3300
uF35
0V
C74
20uF
400V
C74
20uF
400V
L1 160u
H
L1 160u
H
C81
3300
uF35
0V
C81
3300
uF35
0V
L2 160u
H
L2 160u
H
C79
20uF
400V
C79
20uF
400V
L3 160u
H
L3 160u
H
C77
20uF
400V
C77
20uF
400V
L4 160u
H
L4 160u
H
C78
20uF
400V
C78
20uF
400V
C76
20uF
400V
C76
20uF
400V
C75
20uF
400V
C75
20uF
400V
66
B. Bill of Materials
Table B.1 – Bill of Materials and Donated Items
Item Unit
Price ($) Quantity
Total
Price ($)
Hardware
CS Hyde Metalized Mylar Tape, 2.2 mil. Thick,
1' x 72 yds 13.5 1 13.5
SPDT 6A F.LVR Switch 3.69 2 7.38
SPDT 6A R.LVR Switch 3.69 1 3.69
D-Sub 15 Pin Male 2.49 1 2.49
D-Sub 15 Pin Female 2.49 1 2.49
Pre-Punched IC-Spacing Perfboard 2-3/4"x6" 3.99 3 11.97
2-Sided Cooper Clad Board 4.5"x6.125" 3.99 3 11.97
Assorted Cable Ties 8" 5.99 1 5.99
8-10 Stud Ring Terminals 0.14 21 2.94
Door Handles 3.49 2 6.98
PCB Standoff 1" 0.45 4 1.8
PCB Standoff 2 1/4" 0.35 2 0.7
Crimp Pins Male 0.1 15 1.5
Plastic Rectangular Crimp Pin Receptacle 0.5 2 1
Corner Brace 1-1/2" 0.63 4 2.52
White Screw Bumper 0.49 8 3.92
Ring Tongue Connector 0.25 13 3.25
#4-40 x 1/2' Round Head - Slotted Bolt 0.1 12 1.2
#4-40 x 1/2' Round Head - Phillips Bolt 0.1 4 0.4
#4-40 Nut 0.03 10 0.3
#6-32 x 3/8' Round Head - Slotted Bolt 0.1 16 1.6
#6-32 Nut 0.03 16 0.48
#6 Lock Washer 0.06 28 1.68
#6 SAE Washer 0.03 40 1.2
#10-32 x 3/8" Round Head - Slotted Bolt 0.1 8 0.8
#10-32 x 1/2" Round Head - Slotted Bolt 0.1 8 0.8
#10-32 x 5/8" Round Head - Slotted Bolt 0.1 5 0.5
#10-32 x 3/4" Round Head - Slotted Bolt 0.1 16 1.6
#10-32 x 1" Rounded - Slotted Bolt 0.1 9 0.9
#10-32 x 1/2" Flat Head- Phillips Bolt 0.1 8 0.8
#10-32 Nut 0.03 59 1.77
#10 Lock Washer 0.06 75 4.5
#10 SAE Washer 0.03 69 2.07
Aluminum Flat Plate 9.85 1 9.85
67
Polyolenfin Heat Shrink Tubing 3/32" 1.79 1 1.79
Polyolenfin Heat Shrink Tubing 3/32" 1.95 1 1.95
IC Socket Mach Pin WW 8Pos Gold - AR08-HZW/T-R 1.69 3 5.07
IC Socket Mach Pin WW 14Pos Gold - AR14-HZW/T-R 2.53 2 5.06
IC Socket Mach Pin WW 16Pos Gold - AR16-HZW/T-R 2.9 5 14.5
IC Socket Mach Pin WW 18Pos Gold - AR18-HZW/T-R 2.9 4 11.6
Square Machine Post - 100 4.99 1 4.99
Coaxial DC Power Jack 3.29 4 13.16
Coaxial DC Power Plug 3.29 4 13.16
Electronics
Texas Instruments - OpAmp Dual JFET Input -
TL082CP 0.77 2 1.54
Unitrode - SM Crtl for DC Motor Drive - UC3637 7.28 4 29.12
Analog Devices Inc - OpAmp JFET R-R Dual -
AD823AN 5.64 1 5.64
Fairchild Semiconductor - Quad 2 Input Nand -
74AC00B 0.6 2 1.2
International Rectifier - IGBT - IRGP50B60PD1 8.28 16 132.48
STMicroelectronics - Multivibrator - HCF4538B 0.65 1 0.65
Silicon Labs - High Side / Low Side Driver - Si8234BB 3.71 4 14.84
Mallory CGS332T350X5L 3300μF 350VDC Capacitor 71.45 2 142.9
United Chemi-Con - Cap Elect 820uF 50V 1.29 3 3.87
Panasonic - ECG - Cap 4.7uf 25V Cer - PCC2251CT-ND 0.79 3 2.37
TDK Corp - Cap Cer 10uF 16V X7R RAD -
FK20X7R1C106K 0.83 3 2.49
Panasonic - ECG - Cap Elect 10uF 400V - EEU-
ED2G100 0.67 8 5.36
BC Components - Cap Cer .10UF 50V -
K104K15X7RF5TH5 0.06 51 3.06
Murata Electronics NA - Cap Cer 300pF 50V 0.3 1 0.3
Murata Electronics NA - Cap Cer 5600pF 50V 0.62 1 0.62
TDK Corporation - Cap Cer 0.33uF 50V -
FK24X7R1H334K 0.21 12 2.52
United Chemi-Con - Cap Elect 560uF 50V 0.86 1 0.86
Diodes Inc - Diode Schottky 40V 400MW - SD103A-T 0.65 5 3.25
ON Semiconductor - Switchmode -Diode 4A 600V 0.65 8 5.2
Murata Electronics NA - Trim Pot Cerm 100kOhm - 1.38 8 11.04
Stackpole Electronics Inc - RES 1kOhm 1/8W 5% - 0.09 4 0.36
Murata Electronics NA - Trim Pot Cer 20kOhm 1.38 3 4.14
Yageo - Res 20.5kohm 1/4W 1% Metal Film 0.57 6 3.42
Stackpole Electronics - Res MF 1/8W 5.62kOhm 1% 0.15 2 0.3
Stackpole Electronics Inc - Res MF 1/8W
68.1kOhm 1% 0.15 1 0.15
68
Stackpole Electronics Inc - Res MF 1/8W
47.5kOhm 1% 0.15 1 0.15
Murata Electronics NA - Trim Pot Cerm
10kOhm 12Trn 1.81 2 3.62
Stackpole Electronics Inc - Res MF 1/8W
330kOhm 1% 0.15 1 0.15
Stackpole Electronics Inc - Res MF 1/8W
150kOhm 1% 0.15 2 0.3
Stackpole Electronics Inc - Res MF 1/8W
10.2kOhm 1% 0.15 16 2.4
Stackpole Electronics Inc - Res MF 1/8W 3.9Ohm 1% 0.15 4 0.6
Stackpole Electronics Inc - Res MF 1/8W 4.7Ohm 1% 0.15 4 0.6
Wire
UL- Stranded Hookup Wire - 22AWG - Red 25' 2.33 1 2.33
UL- Stranded Hookup Wire - 22AWG - Green 25' 2.33 1 2.33
UL- Stranded Hookup Wire - 22AWG - Black 25' 2.33 1 2.33
10AWG - Mil Spec - M81044/ 9-10-9 - White 10' 4 1 4
10AWG - Mil Spec - M81044/ 9-10-0 - Black 10' 4 1 4
26AWG - Stranded HookupWire - Red - 25' 2.25 1 2.25
26AWG - Stranded HookupWire - Black - 25' 2.25 1 2.25
26AWG - Assorted Stranded HookupWire - 25' 4.99 1 4.99
Magnet Wire / Winding Wire - 10 AWG, 11LBS 124.99 1 124.99
Wire Roll Repl 30AWG Blue 50' 9.12 1 9.12
Wire Roll Repl 30AWG Yellow 50' 9.12 1 9.12
Wire Roll Repl 30AWG Green 50' 9.12 1 9.12
Wire Roll Repl 30AWG Orange 50' 9.12 1 9.12
Grand
Total 757.27
Donated Items Quantity
Plexiglass Project Box 22 3/8"X 20 1/8" X 9 1/4" 1
dsPIC Funtion Generator 1
Electrocube 945B 20μF 400VDC Capacitor 6
Powerlite C-Core AMCC 50 8
Powerlite Bobbin AMCC-50BOB 8
69
C. Circuit Board Layout
Fig. C.1 – Microsoft PowerPoint Circuit Board Layout
Source: John Brewer, Jr. and Kamaljit Bagha
70
D. Circuit Board IC and Component Locations
Fig. D.1 – IC and Component Circuit Board Location
Source: John Brewer, Jr. and Kamaljit Bagha
71
E. Hardware Configuration and Layout
Fig. E.1 – Hardware Configuration and Layout
Source: Kamaljit Bagha
72
Fig. E.2 – Test Bench Setup
Source: Kamaljit Bagha