hybrid electric vehicle power train
DESCRIPTION
To improve the performance of epileptic seizuredetection, Hybrid electric vehicle power train independent component analysis (ICA) is applied tomulti-channel signals to separate artifacts and signals of interest.FastICA is an efficient algorithm to compute ICA. To reduce theenergy dissipation, eigenvalue decomposition (EVD) is utilized inthe preprocessing stage to reduce the convergence time of iterativecalculation of ICA components. EVD is computed efficientlythrough an array structure of processing elements running in parallel.Area-efficient EVD architecture is realized by leveraging theapproximate Jacobi algorithm, leading to a 77.2% area reduction.TRANSCRIPT
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Vehicle
Dynamics
Brake
Torque
Vehicle
Driver
Longitudinal
Dynamics
Tire/Roadccelerator
Command
Brake
Command
Vehicle Velocity
Controller
Brake
Torque
Brake
Hardware
Longitudinal
Dynamics
Tire/Road
Brake Hydraulic
Command Brake System
.
nterface
Load Forces
InverteriMotor
Controller
InverteriMotor
Control
-
Braking Control
Motor Torque
Vehicle Velocity
Interface
LoadForces
Traction Motor
Motor
Torque
Delivered
Motor Nonlinearities
1q
ommandI
Driveline
Dynamics
Dynamic
Weight
Transfer
-----+I I
Battery
Motorhverter
Efficiency
Battery Dynamics
Battery Nonlinearities
Battery Efficiencies
Energy Recovered
Inverter Load
Current
Fig.
I .
Electric vehicle dynamic model.
The driveline efficiency of the conventional powertrain portion
of the HEV system can be improved by the inclusion of an auto-
matic manual transmissioddry clutch driveline combination. Au-
tomation of a manual transmission alleviates driver interaction
with the clutch and gear shift lever required in a standard manual
bansmissiodclutch combination, while providing near automatic
transmission performance.
This
type of driveline, combined with
the proper choice of “shift points,” and elimination of the torque
converter (prevalent in automatic transmissions) can enhance fuel
economy while mitigating emission effects.
Such combinations of components, with an array of energy
and power levels (as well as perhaps dissimilar dynamic proper-
ties), yields
a
potentially difficult ensemble dynamic control
problem. A powertrain dynamic model of such a complex pro-
cess enables the development of a measure of performance and
allows insight into the dominant dynamic effects in control law
synthesis. Additionally, a powertrain model can be used to help
determine optimum powerplantldriveline combinations, elimi-
nating unnecessary vehicle builds. This article contains a de-
scription of HEV dynamic models; many of the important
dynamic control related issues are highlighted. The primary
components presented include a vehicle driver, coordinated con-
troller, a phenomenological model of a Spark Ignited
(SI)
Inter-
nal Combustion Engine
(ICE),
variable field altemator, dynamic
lead acid battery,
dry
clutch, automated manual layshaft trans-
mission, brake system, complete vehicle longitudinal dynamics
with tire-road interface characterization, and an ac induction mo-
tor electric drive system.
Also discussed in this article are automated manual layshaft
conventional powertrain test results and simulations that demon-
strate dynamic interactive effects and aid
in
the formulation of
dynamic control laws for powertrain control. Presented also are
simulations of the
PHEV
dynamic model, which demonstrate the
added complexity
of
the electric powertrain dynamic interactive
effects, the understanding of which is a precursor to dynamic
control law synthesis.
EV Powertrain System
Vehicle Driver and Coordinated Control
Generally, for all the vehicle configurations discussed herein,
the driver model includes an implicit vehicle velocity controller,
with driver velocity error and
Propohonal-Integral-Denvatrve
(PID)capability, and a collection of drive cycles to provide a ve-
hicle input command. The vehicle driver model uses vehicle ve-
locity feedback from the vehicle dynamics and a commanded
vehicle velocity to generate braking to the brakes, and for an EV,
a coordinated vehicle controller then provides motoring and re-
generative commands to the motor controller for corresponding
positive and negative motor torque. Perhaps command informa-
tion is also provided to a clutch and transmission system when a
manual or automatic manual transmssion
is
employed. A sche-
matic representation of an EV dynamic powertrain without a
gear changing transmission is shown in Fig.
1.
Inverter/Motor Controller
The traction motor and controller
[lo],
[11] extract power
from the battery, or alternative energy storage device, and pro-
vide torque to the driveline
[
121, [
131,
which in turn provides the
EV motive power. Additionally, the traction motor and controller
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may be operated as a starter/alternator combination [14] or as a
generator used to recover the vehicle kinetic energy dissipated
during braking [1.51, [161. The traction motor and controller then
provide power to the battery or altemative power source, and
negative torque to the driveline, which in turn brakes the vehicle.
The coordination of electric and hydraulic blending, during
braking, is performed by the traction motor controller to meet the
driver brake torque command. Compression braking torque,
electric braking torque used to emulate the feel of engine drag
present on an IC engine vehicle, is also determined by the trac-
tion motor controller.
All
negative motor torque is reduced lin-
early at low vehicle speeds where no energy can be recovered.
Clompression braking torque allows braking to occur while re-
covering the maximum energy, due to all braking being per-
folrmed electrically.
Traction Motor Dynamics
The traction motor dynamic model [lo] represents the dy-
namics of a specific field oriented controlled ac induction motor
as described by the following equations:
h,, = L .iqs L , .iqr
h,, =
L,T
id +L ,
.id
A = L m . i q a L;iq,
h ,
= L , . L , i
The inverter load current is a function of traction motor speed,
torque delivered, and terminal voltage of the battery during mo-
toring and during regeneration as:
where
elb
is battery terminal voltage, V; Tmposdels positive motor
torque delivered during motoring, Nm.;
q
is motor and inverter
combined efficiency.
Battery
The battery model is a lumped parameter dynamic character-
ization of a lead acid battery [8], [14]. The open circuit voltage is
a function of traction battery state of charge and empirical pa-
rameters for lead acid batteries. The dynamic relationships be-
tween battery voltage and current are modeled, including the
polarization capacitive effect, incipient capacitance of the bat-
tery, internal battery resistance, and terminal ohmic resistance.
For example,
V,, = 338.8.[0.94246
+
0.0.05754.(
S O C ) ]
R~ .
elb = zCh
R ~
lh
dt
where C, is capacitive impedance, F; C, is polarization capaci-
tance, F;Zlbisvoltage drop due to_polarization capacitance, V; ilb
is battery discharge current,
A; R
is battery intemal resistance,
ohms;
Rb
is battery terminal resistance, ohms; SOC is battery
state of charge, percent; V,, is battery open circuit voltage, V.
wlherei,,, iqr are d q axis rotor current respectively, A; i d s i q s are
d ,
q
axis primary current respectively, A ; L are mutual induc-
tance, H; r ,LJ are resolved rotor, stator inductance respec-
tively, H; P is poles; Rr,
Rs
re resolved rotor, stator resistance
reispectively, ohms;
V,,
Vqsare d
q
axis primary voltage respec-
tively, V; h,,,h
qr
are d q axis rotor equivalent flux respectively,
V-sec; h,, h , are
d q
axis stator equivalent flux respectively,
V-sec;
o s synchronous frequency,rps ;ors rotor frequency,
rps;
&,is
rotor acceleration,
rps*;
T,is electric motor torque, Nm.
The traction motor torque delivered is modeled as a function
of the motor dynamics, motor nonlinearities, and losses in both
the motor and inverter as a function of motor speed. The traction
motor torque limit is characterized by functions of the form:
Brake Controller
The dissipation of kinetic energy during braking, by an electric
or hybrid vehicle, can be recovered advantageouslyby controlling
power electronics such that the electric traction motor behaves as a
generator [121. The energy recovered during this process can be
returned to the energy storage device for future use.
A parallel braking system applies regenerative braking torque
(to the driven wheels), in addition to hydraulic braking torque
provided by the foundation braking system. Hydraulic brake
torque is determined in the brake controller, based on HEV coor-
dinated control commands
[
1.51,
[
161. Regenerative brake com-
mands are predetermined as a function of master cylinder
pressure in the traction motor controller and are based on PHEV
coordinated control commands. In a series braking system, not
illustrated here, integrated control exists between the brake con-
troller and the traction motor controller [16], [17].
T,
= a r e d
a <a
Vehicle Dynamics
The vehicle dynamic model in this instance includes four
wheel longitudinal vehicle dynamics for
a
front wheel drive ve-
hicle. The inputs to the vehicle drivetrain are the motor torque or
output
from a gearbox (transmission) with motor torque
as
gear
where
0
s motor base speed, Tm ;
0
is m~ ha ni ca l otor
W e d q m ;
rated motor
torque, Nm.;
T,
is mechanical motor torque, Nm.
rated
motor
power, hp; Trared
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box input. In addition, the vehicle drivetrain receives hydraulic
brakmg torque or other driveline loads, and vehicle velocity is
determined via integration of the longitudinal equations of mo-
tion. Rotational dynamics for each wheel, and halfshafts, and
a
representation of the forces acting on the vehicle, are modeled.
Rotational wheel dynamics include wheel slip (skid), tireiroad
surface adhesion coefficient, wheel tractive force as a function of
dynamic weight transfer, road load torque for each wheel, and
rotational wheel speed.
Wheel slip (skid) is used to determine the tireiroad surface ad-
hesion coefficient with a nonlinear analytic tireiroad surface inter-
face model
[l], [ 3 ] , [17].
The tire model used for this study
assumed a high road surface adhesion coefficient for dry pave-
ment, because these are conventional driving conditions. The
wheel tractive force as a function of dynamic weight transfer is
the product of the road surface adhesion coefficient and the nor-
mal force acting on the wheel:
In calculating the normal forces acting on each wheel, the dy-
namic weight transfer is modeled for each of both front and rear
wheels in terms of the vehicle pitch and lever arms (wheel base)
to the vehicle center of mass. The road load torque for each wheel
is then determined from the wheel diameter and tractive force:
The torques acting on the wheels include the halfshaft torque,
Ts,
road load torque,
Tb,
bearing friction torque, and the braking
torque. Rotational wheel acceleration is obtained by the sum of
the torque acting on the wheel divided by the wheel inertia.
Wheel speed is obtained by integrating rotational wheel acceler-
ation:
The halfshaft model accounts for the torsional compliance be-
tween the differential and wheel. The resulting halfshaft torque is
applied to the wheel. The relations for shaft torque, and shaft com-
pliance in terms of physical parameters are shown below:
The four wheel tractive forces, aerodynamic drag, grade
forces, and rolling resistance, describe the forces acting on the
vehicle and are depicted below:
Ft”,= Ft,, + lr Ft + Fdf - Fa,, Fry
grada
The aerodynamic drag on the vehicle is a function of vehicle
velocity squared, air density, vehicle frontal area, and coefficient
of drag, where the vehicle velocity is determined by solving €or
vehicle acceleration and integrating over time:
The rolling resistance force is a function
of
vehicle weight, roll-
ing resistance coefficient, and vehicle speed:
F,, = f, .
W ,
.1.3558(1+
k ,
. V k, .
V’)
The grade forces acting on the vehicle are a function of vehi-
cle weight and grade angle:
FgrOd, W,
.1.3558
sin0
.
The total forces on the vehicle equal the vehicle mass multi-
plied by the vehicle acceleration.
In these equations,4 s frontal area of vehicle,m2;Cd s aero-
dynamic drag coefficient; Fa,, is aerodynamic drag force on ve-
hicle,
N ;
Fgrad,s grade force on vehicle, N; Frr is rolling
resistance force on vehicle, N;
f , s
rolling resistance coefficient;
ev
s tractive force on left front wheel, N;
c,rs
tractive force on
left rear wheel, N;
e,,
s total forces acting on vehicle, N; F, is
tractive force on right front wheel, N ; Jdq
is
differential inertia,
kg.m2 ; Jfd dg
s final drive inertia on differential side,
k g , m 2 ;
J ,
is
wheel inertia,
kg
.m2
K ,
is halfshaft stiffness, “/rad;
K ,
is
empirical constant;
K 2
is empirical constant; R,, is loss in shaft
bearings, k g . m 2 sec.rad
;
R, s wheel radius, ft; Tb is brake
torque, Nm; T is final drive output torque, Nm; TIoads road
torque, Nm
Tsis
halfshaft torque, Nm; V is vehicle velocity,
m i
sec2 ;
W,is vehicle weight, lbf; y is air density, kg i m ;8 is
grade angle, rad;
0 ,
is halfshaft displacement, rad;
p ( 7 r , l r , r f , y )
s
coefficient of friction on right rear, left rear, right front, and left
front wheels respectively; 03 is wheel speed, radfsec;
ofd
is final
drive speed on differential side, radfsec;ol s left wheel speed,
radisec; w is right wheel speed, radisec.
fd.
Series
HEV
Powertrain System
Vehicle
Driver
and
Coordinated Control
A Series HEV (SHEV) powertrain may be achieved with the
addition of an auxiliary power plant to the electric vehicle in
power series connection with the traction battery and traction
motor. In a “senes” configuration, the power unit interacts with
the vehicle system controller and the rest of the vehicle electrical
system, which includes the vehicle traction motor and other an-
cillary loads such as power steering or air conditioning. The ve-
hicle system controller provides a desired power command and a
desired engine speed command to the SHEV system. Two or
more control variables may be used to attempt to achieve the de-
sired altemator power at a desired engine speed. In addition, the
coordinated vehicle controller provides motoring and regenera-
tive commands to the motor controller. A schmatic representa-
tion of a series HEV is given in Fig.
2.
Engine Dynamic Model
The key exogenous control variable to the
SI
ICE engine sys-
tem
[9]
is the throttle angle (or mechanical equivalent). For a die-
sel engine it might be the fuel control system command. Control
variables such as spark advance, Exhaust Gas Recirculation
(EGR), and Air-to-Fuel ratio AF),nd variable geometry
turbocharger on a supercharged power plant, are for this current
representation considered
to
be precalibrated emission control
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ATR Brake System
-
Vehicle Dynamics
Fixed Field
aximum Power Command SI Engines Speed
Meet Emission
Turbine *Variable Field
tilization
Constraints Diesel
10
to
60
kW
Accel and Brake
ICommands -
Follow Specified
13rive Cycle
-
Brake Torque
High Fidelity Modelof
Brake Components
IMC and Motor
Fixed Field
aximum Power Command SI Engines Speed
Meet Emission
Turbine Variable Field
Utilization
Constraints Diesel
10
to
60
kW
High Fidelity Induction Motor Provides
Motoring Torque
Regen Braking Torque
No
Pedal Torque
Inverter Load
Strateav
&
t Energy Storage
otational Dynamics
*Tire/Road lntetface
Longitudinal Dynamics
Driveline Dynamics
Device
Batteries
Powerplant
Fig. 2.
Series HEV dynam ic model.
variables. The throttle control law includes
a
variable gain PI
(proportional plus integral) controller to provide
a
limited throt-
tle command to the engine, based on commands from the vehicle
driver controller. Included also in the throttle command control
law are the Wide Open Throttle (WOT) operating logic and an
engine Idle Speed Control (ISC) law.
The throttle body is considered as a variable nozzle for air
flow modeling. By considering one dimensional, steady, com-
pressible, isentropic flow of
an
deal gas, the equation represent-
ing mass flow across
a
valve opening or orifice results in
a
quasi-steady relation. In terms of the throttle valve or cross sec-
tional area, Ae, and pressure ratio, the mass flow rate through the
valve is given by
temperature,
KO;
y is ratio of constant pressure to constant vol-
ume specific heats.
The changing flow area, Ae, is
a
function of the obstructing
geometry presented to the flow field. For example, employing
experimentally obtained engine pumping flow rate data for a cir-
cular bore of approximately
34
mm the flow rate (kgh r) may be
given in terms of throttle angle (theta) in degrees
as
F ( e )= c , ( e ) A ( e ) = 3.765-0.1058e 0.05479e*
The manifold dynamic equations that result from using en-
ergy balance and thermodynamic principles
[8]
are
P
=
- Th,,,
Y
- T h o ) + Qm-1
‘
V V
where
where
P, is downstream pressure, kPa;P, is upstream pressure, kPa; R is
specific gas constant, atm
.liter I
gm .mole .
K ; Tu
is upstream
where
C,, C
is constant pressure, volume specific heats; m is
sum
of
manifold intake mass flow rates, kghr;
iz
is sum of all
outflow mass rates, kghr ;
Q,
is rate of heat flow into the mani-
fold, Jouleslsec;
Tt
is temperature of intake masses, deg;
V
is
manifold volume, cm3.
Mass and momentum balance are achieved by assuming uni-
form temperature, pressure and density in each open thermody-
namic volume
as
well as assuming
a
conservation
of
mass
constituents where
no
chemical reactions ake place. In some in-
stances, a further simplified model is justified by assuming in-
variant manifold temperature without loss of the dominant
manifold filling effect. However, temperature effects should not
be neglected when “cold” engine conditions, cold dense air
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charge, or evaporating and condensing fuel are important dy-
namic issues.
An estimation of mass flow rates out of the manifold is given
approximately by a product of the engine speed, engine displace-
ment, and volumetric efficiency, which in turn is resolved in
terms of engine speed, intake temperature, manifold pressure,
and exhaust gas pressure. Manifold mass flow rate egress is
given in terms of manifold pressure and engine speed by an ap-
proximate polynomial functional form
. N
N
M
= ---(OS22 O.OS553(-))(0.17P+ 0 .0 0 0 9 8 P 2 ) ,
1000
1000
where M is speed density mass flow rate, kg/hr and
N
is engine
speed, rpm.
The engine torque developed at any time is a function of the
mass rates (mass charge) or ratios of rates (mass constituents)
that were sampled one engine induction event earlier. This
breathing event is a crank angle synchronized relationship that is
primarily dependent 011engine speed. For a zero order extrapola-
tion, the minimum delay in torque generation that results from
ingestion of the manifold constituents is
180
crankangle degrees.
For a four cylinder engine with a speed of N
RPM,
this is repre-
sented by a propagation lag relationship with idealized delay T is
30/N
seconds.
A similar lag exists for the mixed A/F from the end
of
com-
bustion to exhaust valve closure. In addition,
a
nonspeed depend-
ent propagation lag, and some gaseous diffusion, is assumed to
persist in the exhaust pipe before the A/F sensor location [18].
Representation of the A/F delays in an SI ICE is extremely im-
portant as the torque response is highly sensitive to A/F tran-
sients, including throttle input and fuel control system transients.
The nonlinear structure for the A/F (Air/Fuel) system con-
sists of an EGO (exhaust gas oxygen) A/F sensor in the exhaust
pipe, with a time constant of the order of
70
ms, followed
by
a
nonlinear (Nernst) rich/lean Signum function and
a
PI fuel com-
mand control law
[18].
An intake runner port fuel injector is as-
sumed with a fuel rate output, and with fuel condensation and
evaporation dynamics
[
191. The resulting system equations are
dm
.
,
T - ‘=rp~~-m~,
” dt
m = (1
l)rifi
mi,
m is manifold fuel flow rate, kglhr; m t~ is injector fuel rate com-
mand, kg/hr;nifLs injected fuel flow rate, kglhr;m is fuel evapo-
ration rate, kg hr ;q is fuel accumulation parameter, = 0.25sec;
T~
is injector time constant,
=
50 ms; 7 is condensation and evapo-
ration time, = 0.5 sec.
The fuel mass flow rate is combined with the throttle mass air
flow rate to form the manifold A/F. This A/F is delayed by the in-
duction breathing lag, preparatory to combustion torque genera-
tion, followed by a combustion torque delay, a power-stroke to
exhaust delay, and a plug stroke exhaust system delay that is de-
pendent on the location of the EGO sensor.
Torque generated from the combustion process is dependent
on the ignition of a cylinder charge o f air, fuel, and residual gas,
as well as other variables and parameters that influence combus-
tion efficiency. Assuming a spark advance, EGR (exhaust gas
recirculation), and fuel emission calibrated 1.8 liter engine, an
approximate brake torque relationship is of the form
T
= q A l F , A /F ) 2 , M ,
M 2 , N
...,N 4 , E G R ) .
The rotational motion of the engine crankshaft is given in
terms of the engine polar moment of inertia, angular accelera-
tion, and the difference between the net torque generated by the
engine and the load torque on the driveshaft. Thus,
J , N = (30 / E) T ,
where the load torque may be the starter-alternator (S/A) load,
clutch torque, air conditioning, power steering, or any driveshaft
load and J , is
engine flywhee l inertia, kg .m ’.
StartedAlternator
The alternator model is empirically derived from data taken at
several voltage, field current, and speed operating points. Using
voltage, field current, and speed as inputs, the alternator current
output is determined by functional relationships. This model rep-
resents a three phase synchronous machine generating full wave
rectified DC current [
161.
The starter portion of the StartedAlter-
nator (S/A) is also empirically derived from data and dynamic
simulation results
[7]
t is depicted by a 1.4 kW ac motor directly
connected to the voltage
bus
and geared to the ICE crank. The
S/A
system is controlled via on/off logic and field current com-
mands to control the S/A torque input (or output) of the device.
For an HEV application, the alternator may be assumet to out-
put 70 amps over a voltage operating range from 200 to 380
Volts. The alternator output current can be represented as a func-
tion of field current, speed, voltage and temperature where the al-
ternator field current is a separate dynamic control component.
The alternator output current approximation at a certain speed
and varying output voltage
is
The field current can be represented as follows:
The inductance and resistance vary with speed, load and interior
alternator temperature.
Here,
I l
is alternator output current, A;
I ,
is alternator field
current, A; Lfld s alternator field inductance, H; R , is alternator
filed resistance, ohms; V is al ternator field voltage,V; V,,, is al-
ternator output voltage,V
s alternator rotational speed, krpm.
Series
HEV
Control
A large ICE powerplant (approximately 60kW or more),
could be employed to directly supply the demand power while
using a scaled down battery for partial load leveling or
as
a direct
power source during high power demand. In such a power source
tradeoff the nature of the performance requirements, limitations
on sensor and control mechanisms, and dynamic control law
structure will likely change. The control objectives with
a
more
powerful ICE/alternator and reduced traction battery system
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34
338
336
334
332
33
328
326
324
1000 \
1
5 I
0
0
5
10 15
Fig. 3. Series pow er
unit
control.
might yield a load leveling or load following strategy [20]. In this
instance, the combined powerplanthattery system would be the
prime vehicle power source used to follow the desired vehicle pro-
file while the battery power supply would be used to mitigate the
traction motor transient demands to the ICE/altemator system.
Simulation results for such a combination are shown in Fig.
3 .
In this simulation, the vehicle driver would like to follow the
the first few active (non-idle) seconds
of
the Federal Urban
Driving Cycle (FUDS). In the transient behavior depicted in
Fig. 3 , the driver’s input goes directly to the Induction Motor
Control IMC) of the traction motor and simultaneously to the
thirottle command of the ICE. Until the ICE/alternator can
achieve alternator “cut-in’’ (i.e., that speed at which there is a
power output from the alternator), the traction motor draws
power from the energy storage device which in this case i s a low
storage (small) battery pack. The combination of components
thus illustrated would require a smaller battery pack and re-
duced ICE by proper sizing and proration of power between the
ICE and energy storage device.
Simulations that include engine, alternator, battery, and trac-
tion motor/driveline sizing and dynamic interactions, could be
used to examine energy tradeoffs and transient tradeoffs by vary-
ing control and sizing (kW output) between an alternator and bat-
tery system as series power sources. For instance, for a small
ICE-alternator-battery power source (about
25
kW), a system
operating strategy could be such that the “Range Extender” RE)
is to be activated during estimated low battery State-of-Charge
(SOC)
and simply operates until a desired SOC [8], [20]has been
achieved. There exists dynamic interaction among the
ICE,
alter-
nator, battery and vehicle traction motor (drivetrain) such that en-
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ified operating strategy. speed and alternator kW errors must be simultaneously con-
trolled by the throttle and alternator field current, with
an
inter-
active control law [21].
Engine speed is the pnma q variable to be controlled by the throt-
tle using
a
modified
Proportional-Integral-Differentd
(PID) type
control.
As
mentioned earlier,conditions for wide open throttle (con-
trol variable saturation) and throttle damping (throttle dashpot) must
beaccommodated. Control nteractionof the kW set point is provided
by a modulation of the throttle voltage command.
A
desireable control objective for
a RE
HEV is to control to
a
commanded engine speed (RPM)-alternator kW trajectory with
minimum speed and A/F transients, to provide idle stability at the
lowest possible engine idle speed, to yield a smooth transition to
and from idle speed set point, and to yield a speed profile that is
impervious to exogenous disturbances suchas changes in electric
vehicle driver demand. This objective may be accomplished with
feedback control
on
the engine throttle and alternator field current.
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+
Starter/ Energy
Control Device
Alternator b Starter/ 4 Storage
Alternator
t
Vehicle
Driver
and
Coordinated
Control
Clutch Clutch
Control Mechanism
-
Transmission
Layshaft
Differentiall
Control
Transmission 4 Driveline
Hydraulic
Brake System
Vehicle
Dynamics
and
Tire Road
Interface
Fig.
5.
Automated layshaji transmission vehicle dynamic model.
When altemator field current
is a
control variable, kW error
may be the primary variable to be controlled using perhaps a
modulated
PID
control. The use
of
altemator field current allows
a
rapid variation in alternator kW output at a given altemator
speed with,
of
course, corresponding rapid loading and unload-
ing of the power source (the ICE). Modulation
of
the kW control
can eliminate engine speed transients during altemator loading
and unloading from bus load variations resulting from rapid
changes in vehicle driver demand.
A
simulation result for assumed
RPM
and kW command pro-
files (RPMcom and kWcom) with engine speed
(RPM)
and alterna-
tor kW
as
feedback variables, s shown in Fig.4.Throttle command
to Ihe engine is relatively well behaved resulting in
a
minimization
of A/F
transients, where the extemal
RE
input disturmance is the
traction motor kW demand. In the simulation he battery is initially
at
40
percent State-of-Charge (SOC). Any increase in battery volt-
age:
is due to alternator activation and is especially evident during
motor inactivity (vehicle idle). In
this
instance, the simulation did
not include a regenerative braking system.
An Autom atic Manual Transm ission
Powertrain System
Vehicle Driver and Coordinated Control
The automated manual layshaft transmission and dry clutch
combination dynamic model, depicted in Fig.
5,
consists of a
driver, ICE engine and controller, starter-alternator and control-
ler, dry clutch and controller, automated manual layshaft trans-
mission and controller, hydraulic brakes, vehicle dynamics, and
tirehoad surface interfaces. In the case of n automatic transmis-
sion powertrain system, the vehicle controller provides the en-
gine throttle commands to the engine controller, and to the
clutch, transmission, and brake system. In particular, the control-
ler provides engine, clutch and transmission control during shift-
ing, or braking. Throttle blade commands from the controller to
the engine may be based on transmission gear, driver accelerator
pedal position, engine speed, shift status, and clutch status.
Engine Controller
The key exogenous control variable to the SI ICE engine sys-
tem is the throttle angle (or mechanical equivalent). Control vari-
ables such
as
spark advance, Exhaust Gas Recirculation
(EGR),
and Air-to-Fuel ratio
( A / F ) ,are
for this current representationcon-
sidered to be precalibrated emission control variables. However,
the engine dynamic model does have provision
for
independent
control of these variables if desired. The throttle control law in-
cludes a variable gain
PI
(proportional plus integral) controller to
provide
a
limited throttle command to the engine, based on com-
mands from the vehicle driver controller. Included
also
in the
throttle
command
control
law
are the
Wide Open
Throttle
W m )
operating logic and an engine Idle Speed Control (ISC) law. The
throttle command is received by a throttle dynamic control mecha-
nism which may contain representations
for
throttle springs, link-
ages, deadband, and throttle motor characteristics if desired.
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Clutch Controller
The description of the clutch dynamic model is contained in
the Driveline Dynamics section. The clutch will be commanded
to disengage if upshifting or downshifting is requested, braking
is commanded, engine speed falls below idle, or no engage clutch
command is present and the clutch is not presently engaged.
Clutch engagement will be commanded when engine speed is
sufficient, the brakes are not commanded,
no
upshift and no
downshift requests exist, the transmission is in gear, and
no
dis-
engage clutch command is present.
The clutch uses friction to transmit torque to the manual
transmission. The clutch plate friction allows the plates to slide
before becoming fully engaged preventing jerking. The condi-
tions for slipping are a function of engine speed, transmission
speed, clutch pressure, clutch wear, clutch temperature, and
drive shaft resonance. When the engine speed is much greater
than the transmission input speed, then slipping is necessary to
allow the clutch friction to load the engine, thus reducing the en-
gine speed to the transmission input speed level so that smooth
engagement can take place. When the engine speed is much
slower than the transmission input speed, clutch slippage allows
engine speed to be increased, via the throttle, while exposing the
engine to a very small load, thus avoiding engine stall. During
engagement, essential negative damping causing “clutch shud-
der”
as
well as halfshaft resonance may be present in a magni-
tude that can be felt by the driver, in which case the modulation of
the clutch pressure
in
a variable slipping state is desirable in or-
der to damp such oscillations. Furthermore, it is possible to mod-
ulate clutch pressure to affect torque transmission during
engagement, as well.
Transmission Controller
The dynamic model of the transmission is described in the
Driveline Dynamics section. The transmission controller deter-
mines when a shift event shall occur and selects the appropriate
transmission gear based on transmission output speed, throttle
angle, current gear and clutch state. The occurrence of a shift
event depends
on
piecewise linear functions, called shift sched-
ules. Separate shift schedules exist for upshifting and downskift-
ing. During braking the clutch is disengaged, the engine is
ramped to idle speed, and the transmission continues to shift al-
lowing the transmission to be in the proper gear when an engage-
ment is requested.
A
shift command and gear change are
not
initiated until the clutch controller initiates a clutch disengage
command and the clutch fully disengages. The transmission gear
shift is emulated by modeling a delay, which represents fork
movement and gear engagement time, based
on
experimental
data. Forces
are
not transmitted to the
drivetrain
when the clutch
is disengaged, thus a delay is a sufficient representation. Once
the shift is complete, the clutch is engaged. The transmission will
then remain in gear
as
long as the shift schedule dictates and the
clutch remains engaged.
Brakes
Hydraulic brake pressure commands are received directly
from the vehicle driver. These brake pressure commands are ap-
plied to the brake hardware and then the resultant braking torque
is applied to the vehicle wheels.
Transmisslor
Engine
Fig. 6 utomated Layshaft Transmission Powertrain.
Driveline Dynamics
The driveline dynamic model includes the rotational dynamics
for an automated manual layshaft transmission and
dry
clutch com-
bination, which accepts engine torque, and delivers orque to the ve-
hicle wheels through the differential and halfshafts. The engine is
connected directly to the differential through the clutch, transmis-
sion,
and a final drive, as a conventionalpowertrain. Rotational dy-
namics and nonlinearities for the engine, clutch, transmission, final
drive and differential are modeled.A simplified diagram, represent-
ing
this
nonlinear dynamic powertrain, is given in Fig.
6.
When engine torque is transmitted, the engine inertia coupled
to the clutch inertia on the engine side is accelerated. The altema-
tor is an additional engine load, and torque from the starter aids
the engine during starting.Three states of the clutch are modeled:
fully engaged, slipping, and disengaged. Constitutive relation-
ships allow seamless transition between differential equations
that represent each of the three clutch states. If the speeds
of
both
clutch plates are not equivalent, then the clutch plate may be slip-
ping or disengaged. The acceleration equation for the engine
crankshaft is:
In
this
constitutive relationship for slipping during clutch en-
gagement, the fi st multiplicative relation characterizes the drive-
shaft stiffness and is a function of the integral of the speed
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difference between the two clutch plates. The second bracketed
term characterizes the percentage of torque transmitted through
the clutch due to the speed difference between the plates. The neg-
ative damping imposed by this term can be felt by the driver, when
sufficient slip is not present and the clutch is nearing lockup. The
driveline stiffness and the percentage of torque transmitted
through the clutch are also a function of the clutch friction material
temperature and the clutch wear. The third multiplicative term
f o ,
-
oce, l
s the normalized clutch capacity and shows that
the clutch can be modulated as a function of the halfshaft reso-
naince to enhance stability and driver feel. When the clutch is en-
gaged, the fully engaged conditions areo
o c a :
The constitutive relationship characterization of the clutch in the
fully engaged state includes the driveshaft stiffness and damping
due to the speed difference between the two clutch plates.
Included in the driveline
is
a layshaft transmission which lies
between the clutch and the differential. The synchromesh pre-
vents gears inside the transmission from engaging at different
speeds. Before any forward gear is selected, gear wheels driven
by the engine free-wheel on the transmission shaft. Before gear
engagement the gear and the shaft must be brought to the same
speed and locked together. The synchromesh uses friction to ac-
complish this. The selector fork pushes a collar along the trans-
mission shaft, the collar rotating with the shaft. The collar fits
over a cone on the gear wheel, allowing the gear wheel to speed
up
or slow down until both gear wheel and shaft are moving at the
sarne speed. An outer toothed ring on the collar engages dog
teeth on the cone, locking the collar to the gear wheel. When the
synchromesh is disengaged, the collar and gear wheel are not
connected. The gear wheel rotates with the transmission shaft.
When the synchromesh is engaged the collar makes contact with
the cone and friction between them brings them to the same
speed. The teeth mesh together to lock the gear to the transmis-
sion shaft and allow torque through from the engine.
When the transmission is in gear, assuming 100 mechan-
ical efficiency, rigid gears, and no gearlash or dead band, then
ace,a,g,. Engine torque is transmitted through the trans-
mission:
When the transmission is in gear, but gearlash and or dead band is
present in the transmission:
When the transmission is in gear and no gear lash or dead band is
present:
where
When the transmission is not in gear
Assuming 100 mechanical efficiency, rigid gears, and no
gearlash or dead band, then ag =0 .hen torque is trans-
mitted to the differential:
m
When gearlash and or dead band is present in the final drive
Assuming 100 mechanical efficiency, rigid gears, and no
gearlash and or dead band, then torque is transmitted to the
halfshafts:
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140
7
120:
100:
2 801
> :
60
1
L
i
o ~ ' ' ' ' ' ' ' ' ' ' '
0
10
20
30 40
50
60
0
0 10
20
30
40 50 60
Time sec)
Fig. 7. Wide open throttle data.
1000~
7
6
e
500
400
300
200
1004
~ ' ' ' ' ~
0 10 20 30 40 50
60
Time sec)
,000 l
04
' I
0 10 20 30 40 50 60
Time sec)
Fig.
8.
Wide-open throttle simulation.
28
Test Data and Simulation
Results
An automatic manual layshaft
transmission/dry clutch vehicle
was built. Test data was taken for
model validation for an array of ve-
hicle operating conditions, includ-
ing medium acceleration and Wide
Open Throttle (WOT) on various
grades and road surfaces. For ex-
ample, Figs.
7
and
8
show WOT
test data
and
simulation results on
flat terrain. In this context, WOT
implies maximum driver demand
on
the powertrain system. The test
data plotted is vehicle velocity in
kph, throttle position in counts,
gear, and engine speed in
rpm.
Comparing the test data versus
the simulation, six seconds after
the vehicle begins acceleration it
has attained a speed
of
45
kph with
the test data and
40
kph with the
simulation. Shifting takes place at
about six seconds,
10
seconds,
20
seconds, etc., in both the simula-
tion and the vehicle. The vehicle
speed and gear shifting relation-
ships show close correlation. Gen-
erally, the automatic layshaft
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--c
Diesel Turbocharged
Fuel Diesel
Control
Driveline
Dynamics
Vehicle
Driver
and
Coordinated
Fig
9. Pre-transmission (motor ahead of transmission) coupled PHEV dynamic model.
*
Clutch Clutch
Control Mechanism
Rotational
Dynamics
Induction Differential Tire/Road
Generator
I
nverter
Motorl
-
Motorl - Transmission
+
Generator
Control
Driveline -+ Interface
*
3-
Transmission
Control
c Energy Storage
Battery
Flywheel
Ultracap
I
Parallel
transmission vehicle test data and simulation results correlate
quite closely. When comparing the test data and simulation,
model parameters are adjusted for one operating condition until
very close correlation exists. The resulting parameter set is fixed
and remains the same for all other simulation and test vehicle op-
erating conditions. The tests were conducted over several differ-
ent road conditions and grades for all comparison studies. The
primary objective of the comparison was to establish a reason-
able dynamic powertrain model upon which hybridization of the
vehicle could take place.
1
PHEV
Component Models
and
Controllers
The model for a PHEV powertrain contains many of the com-
ponents of a conventional thermomechanical system. It also in-
cludes electric vehicle components such as a traction motor and
traction motor controller, as well as a traction energy storage
source suitable for electric only or hybrid vehicle operation. The
PHEV
dynamic model, depicted in Figs. 9 and 10,consists of a
drker, startedalternator, startedaltemator controller, engine, en-
gine controller, a traction motor controller, a traction motor, hy-
draulic and regenerative braking system, a battery, engine clutch
cointroller, engine clutch, motor clutch controller, motor clutch,
transmission controller, transmission, vehicle dynamics, PHEV
coordinated controller, and tire/road surface interfaces. The
coimponents of such a hybrid are discussed subsequently.
Regenerative
Brake System
Vehicle Driver and Coordinated Control
Power, energy, or torque partitioning between two power
sources is dependent on vehicle objectives and may be based on
bal.tery State Of Charge (SOC), motor speed versus torque limits,
transmission gear, driver accelerator pedal position, engine
speed, average drive wheel power, shift status, engine clutch sta-
tus, estimated engine torque, and estimated engine torque avail-
able. Torque may be partitioned to operate in an engine only
mode, a motor only mode, or a two traction device mode. Addi-
tionally, the motor provides torque during shifting so that torque
disruption to the powertrain is eliminated
[
171. The powertrain
will provide negative torque via the motor during braking for en-
ergy recovery. During periods of low battery SOC, the engine
may be loaded with the alternator to charge the battery.
StartedAlternator Controller
The starter portion of the Starter/Alternator S/A) is empirically
derived from data and dynamic simulation results [141.An ac motor
is directly connected to the voltage bus and geared to the SI ICE
crank. The S/A system is controlled via on/off logic and field current
commands to control the S/A torque input (output) of the device.
Engine, Clutch and Transmission Controllers
The throttle control law includes a variable gain Proportional
plus Integral (PI) controller to provide a limited throttle com-
mand to the engine, based on commands from the
PHEV
coordi-
nated controller. Included in the throttle command control law
are many of the functions discussed earlier such as the Wide
Open Throttle (WOT) operating logic and an engine idle speed
control law.
The coordinated control of the engine, engine clutch, and
transmission for an HEV could be conducted in a manner similar
to the Automatic Layshaft Powertrain
ALP),
especially for the
post transmission configuration shown in Fig. 10. However, the
added complexity of regenerative brake capability could greatly
increase control complexity [
161,
[ 221. For the post transmission
configuration, one relatively simple addition to the autolayshaft
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Started
Alternator Alternator
Control
Differential/
Layshaft + Driveline
ransmission
Control Transmission
ehicle
Driver
and
Coordinated
t--
Control
1
+
Engine IC Engine
Control
Motor
Clutch
Inverter Induction Motor
Generator Generator Control
Motor1 Motor/ t lutch 4 F
-
ontrol
Engine Engine
Clutch Clutch
Control
I
i
Storage
Regenerative
Brake System
Vehicle
Dynamil
and
Tire
Ro;
lnterfac
Fig.
10.
Post-transmission coupled
PHEV
dynamic model.
control might be to simply open the engine clutch and idle or shut
down the ICE during electric regenerative braking.
InvertedMotor Controller
The traction motor and controller extract power from the bat-
tery, or alternative power source, and provide torque to the
driveline, which in turn provides the EV motive power. Addi-
tionally, the traction motor and controller may be operated
as
a
generator and recover kinetic energy dissipated during braking.
The traction motor and controller then provide power to the en-
ergy storage device, and negative torque to the driveline, which
in turn brakes the vehicle. The coordination of electric and hy-
draulic blending, during braking, is performed by the traction
motor controller to meet the driver brake torque command. The
motor torque command
is
input
to
a torque loop compensator
that controls drivetrain stability.
Brake System Dynamic Model and Control
Dissipation of kinetic energy during braking, by an EV or
HEV, can be recovered by controlling power electronics such
that the electric traction motor behaves as a generator, and re-
turned to the energy storage device for future use
[13],
[14].
A
parallel braking system applies regenerative braking torque to
the driven wheels, in addition to hydraulic braking torque pro-
vided by the foundation braking system. The amount of electric
brake torque that can be added to the hydraulic brake torque is
derived from static brake force relationships, motor torque char-
acteristics, driver feel, and the tire/road surface interface.
The brake hardware model includes dynamics of the hydrau-
lic brake system. Brake pressure commands are received directly
from the PHEV coordinated controller and applied to brake hard-
ware. The resultant brake torque is applied to the wheels.
Driveline Dynamics
The driveline dynamic model includes rotational dynamics
for a PHEV, which accepts engine and motor torque (in a regen-
erative or motoring mode), and delivers torque to the wheels
through a differential and halfshafts. Motor torque is delivered,
via a transaxle, to the differential through
a 4 x 4
coupler con-
nected to
a
halfshaft, and summed with engine torque at the dif-
ferential. The engine is connected directly to the differential
through the clutch, transmission and final drive, as in a conven-
tional powertrain. Rotational dynamics and nonlinearities for the
engine, engine clutch, transmission, final drive, differential,
4
x
4
coupler, motor clutch, motor transaxle, and motor are mod-
eled in
a
manner similar to that discussed earlier. See Fig. 11for
a
simplified diagram representing this nonlinear dynamic PHEV
powertrain.
When motor torque is transmitted, the motor inertia, coupled
to the transaxle inertia, is accelerated. Assuming
100
mechani-
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Motor Transaxle
Assembly
Fig.
11.
Parallel
hybrid
powertrain.
cal efficiency, rigid gears, and
no
gearlash or dead band, then
toirque is transmitted to the motor clutch and
om
wale .
gale:
( J m + Ju/e m m
=
T , a / e g a i e .
When gearlash and or dead band exist in the transaxle then:
Three states of the motor clutch are modeled: disengaged, fully
engaged, and slipping. The motor will be commanded to engage
when the PHEV coordinated controller initiates motor opera-
tion. When the motor clutch is disengaged:
( J a i e c c m
+ J c m ) C i ) a i e = Tale
When torque is applied to the transaxle, torque is transmitted to
the
motor clutch during engagement or slipping:
( J a r 1 e - m + J c m N a i e = L i e
- T m l .
When the motor clutch is slipping or engaged:
f(wa,
- w c m l ) j k w a l e
wcm1 dt
=
L I .
When torque is transmitted through the motor clutch to the 4x4
coupler, assuming
100
mechanical efficiency, rigid gears, and
no gearlash and or dead band:
When gearlash and or dead band is present in the 4x4 coupler:
Assuming
100
mechanical efficiency, rigid gears, and no
gearlash and or dead band, then torque is transmitted to the
hailfshafts and
w f d
= o :
Simulation Results
Typical PHEV simulation results (see Fig.
12) show vehicle velocity (mph), throttle angle
(degrees), engine speed (rpm), gear, drive wheel
average power (kWatts), halfshaft torque (Nm),
engine and motor torque (Nm). The PHEV simu-
lation shows the vehicle accelerating and decel-
erating, highlighting regenerative braking.
When
the
vehicle accelerates from rest in first
gear, the motor provides the necessary torque. As
the vehicle begins to accelerate the throttle angle
and engine speed are at idle. The vehicle operates
in motor only mode until third gear. The motor
also provides torque to the drive wheels during
shifting. During third gear the vehicle
runs
in en-
gine only mode. Application of motor torque can
be seen, in third
ge ,
just after
5
seconds, in or-
der to meet the driver acceleration command,
when the engine is already delivering full torque.
This occurs again in fourth gear just before 10 seconds.
As
the
vehicle decelerates there is
a
downshift, while the clutch is disen-
gaged, and the engine
is
ramped to idle. The motor provides neg-
ative brake torque to the drive wheels slowing the vehicle, while
recovering energy.
Conclusions
This paper describes the mathematical modeling, analysis,
and simulation of
a
dynamic automatic manual layshaft trans-
mission and dry clutch combination powertrain model, and cor-
responding coordinated control laws synthesized using a
conventional SI ICE powerplant-alternator combination, a dry
clutch and manual transmissioddifferential,variable field alter-
nator, brakes, and complete vehicle longitudinal dynamics with
tire-road interface characterization. The conventional power-
train model is validated using experimental test data confirming
accurate emulation of dynamic components of the pre-hybrid-
ized vehicle. In addition, the development of dynamic series and
parallel HEV powertrain models and corresponding coordinated
control laws are described. The HEV models are developed by
modeling the additional traction motor transaxle and gearing. A
discussion of the key issues associated with coordinated control
law development is provided
Simulations of the dynamic behavior of two types of series
HEV's vehicle are shown. Also, simulations depicting the dy-
namic behavior of vehicle test data for an automatic manual
transmission vehicle and simulations of
a
PHEV are shown. The
simulation environment consists of the modular code of Xmath/
Systembuild (ISI) and Matlab/Simulink (Mathworks) with mod-
ifications to the code in order to implant real time stiff integration
methods into the ICE, battery system, traction motor system, and
driveline dynamics. The nominal integration time step (frame-
time) for simulation is on the order of two to ten msec, depending
on
the model version and custom developed real time integration
method employed.
The dynamic model is currently being used to provide the
framework
for
hybrid vehicle control law development, and
for
the
DI
dieseVautomatic manual layshaft transmission vehicles al-
ready being developed in the
U.S.
and Europe. Versions of the
model, including on board computer emulation and communica-
tion
network latencies and delays, are being employed for control
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100
80
60
40
20
ouu
400
200
0
-200
t iear3 I
-400 ’
120
~ _ _ _ _ _ _ _ _ _ _ , - _ _ _ _ _ _ _ _
60
- - - - - - - - - ,
- r - - - - - - - - -
0 5
10 15 20 25 30
Fig.
12.
P ar a l le l hybrid ve h ic le
simulation
and con t r o l .
algorithm code processor implementation and as a foundation for
Hardware-in-the-Loop simulation.
[Z] R.G. Delosh, et al, “Dynamic Computer Simulation of
a
Vehicle with
Electronic Engine Control,” SAE Paper 8 10447, Detroit, Michigan, Febru-
ary 1981.
Acknowledgements
The authors would like to acknowledge technical contribu-
tions to the automated manual layshaft transmission dynamic
model of D. B. Bell, W. J. Weber, Miroslava Jankovic, and N.
Sureshbabu, as well as the technical discussions with our Euro-
pean collegues R. Busch and
C.
Krauss. The authors also ac-
knowledge the efforts of
D.
B. Bell,
J.
R.
Blankenship, and
R. D.
Gilland in test data collection as well as hybrid vehicle consult-
ing from
M.A.
Tamor, W. Buschhaus,
L.
R. Brandenburg,
R.I.
Sims. and B. Bates.
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bility of Electric Vehicle Braking Systems,”
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Symp.
Ad-
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[
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ordinated Control System for a Hybrid Electric Vehicle,” Proc. 14th
Int.
Electric Vehicle
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(EVS-14), Orlando , Fla., Decem ber 16, 1997.
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search Technical Report
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tral Fuel Injection Engine,” SAE 810494, Detroit Michigan, February 1 981.
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[21]
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Barry Powell
received degrees from the University of Michigan in Applied
Mathe matics, Aeronautica l and Astronautical Engine ering, Instrume ntation
Engineering, and Information and C ontrol Theory. He has been a Research
Engine er at Ford Resea rch Laboratory, since October, 1976. Prior to that time
he worked in Ford Automotive Safety Research, Bendix Research Labora-
tories, and Excel lo Corporation Resea rch. His responsibilities have included
mathematical modeling, analysis, simulation and control development of
high performance aircraft, space vehicles, and automotive powerplant and
powertra in systems. He has had responsibility for the technical direction of
real-time simulation and hardware-in-the-loopdevelop ment of advanced en-
gine con trol systems. Mr. Powell is currently involved in the ana lysis, devel-
opme nt and impleme ntation of hybrid electric vehicle dynamic systems.
Kathleen Bailey received
a
BS degree in M athematics from Lawrence Tech-
nologica l University in 1978 and a MSE in Comp uter, Informa tion and Con-
trol Engineerin g from the University of Michigan in 1979. She joined the
Ford Mo tor Company R esearch Laboratory in 1993 and is currently partici-
pating in the development of hybrid vehicle subsystem mathematical mod-
els, synthesis of system dynamic models for various hybrid vehicle
configurations, and dynamic analysis and control system development for
selected hybrid power source vehicles. Prior to that time she worked at
Hughes M issile Systems Group, and General Dynam ics Land Systems Divi-
sion. Her responsibilitie s have includ ed electronic control system optimiza-
tion for missile seeke r systems, senior project engineer on arobotic machine
vision testbed program, and an alysis and development of a model reference
adaptive electronic fuel metering system for automob iles.
Susan Cikanek is employed with Ford Motor Company on the Hybrid Elec-
tric Vehicle program, as a Research Engineer. He r current responsibilities in-
clude dynamic system modeling, control law development, simulation and
testing of conv entional, hybrid, and electric vehicles, as well a s establish-
ment of system and subsystem design requirements a nd architectures. After
receiving a B.S. and M .S. in Electrical Engineering from Wayne State Univer-
sity, Detroit, Michigan, she worked at Eaton Corporation. She modeled, de-
signed, implemented, and tested real-time closed loop control algorithms for
automotive, truck and motor applications applying robust, optimal, adaptive,
digital, classical, and m odern control techniques. In addition, she worked on
electric vehicle induction motor and driveline control applications. She holds
patents on regenerative braking control, and induction motor control for elec-
tric and hybrid vehicle applications.
October
1998
33