sensorlesssrm_hossain2003
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IEEE TRANSACTIONS ON INDUSTRY APPLICATIONS, VOL. 39, NO. 5, SEPTEMBER/OCTOBER 2003 1343
Four-Quadrant and Zero-Speed Sensorless Controlof a Switched Reluctance Motor
Syed A. Hossain, Member, IEEE, Iqbal Husain, Senior Member, IEEE, Harald Klode, Bruno Lequesne , Fellow, IEEE,Avoki M. Omekanda, Senior Member, IEEE, and Suresh Gopalakrishnan, Senior Member, IEEE
AbstractA four-quadrant sensorless controller for switchedreluctance motor (SRM) drives is presented in this paper. Thedrive system with appropriate turn-on and turn-off angles foreach operating quadrant delivers excellent dynamic performanceover a wide speed range including zero speed. The problemsassociated with practical implementation especially at low andzero speeds have been addressed and overcome with engineeringsolutions. Experimental results for a 1kW SRM obtained on adSPACE-based system are presented along with useful guidelinesfor practical implementation.
Index TermsFour-quadrant control, position and speed esti-mations, sensorless control, sliding-mode observer, switched reluc-
tance motors (SRMs), zero-speed control.
I. INTRODUCTION
SWITCHED reluctance motor (SRM) drives today aregradually penetrating the market with applications alreadydeveloped or being developed for the consumer product,
aerospace, and automobile industries. The SRM drives have the
attractive features of fault tolerance and the absence of magnets.
However, the control of an SRM depends on the commutation
of the stator phases in synchronism with the rotor position. The
position-sensing requirement increases the overall cost and
calls for extra space and complexity. This drawback excludes
the SRM from many cost sensitive industrial applications.Sensorless operation is a key requirement for the success of
SRM drives in various industries [1][4].
One method of sensorless operation is to detect the phase cur-
rent waveform and determine the rotor position by calculating
the phase inductance from rate of change of the phase current
[1], [2]. This method needs the injection of diagnostic pulses
into an inactive phase. However, the diagnostic pulses generate
Paper IPCSD 03059, presented at the 2002 Industry Applications SocietyAnnual Meeting, Pittsburgh, PA, October 1318, and approved for publica-tion in the IEEE TRANSACTIONS ON INDUSTRY APPLICATIONS by the IndustrialDrives Committee of the IEEE Industry Applications Society. Manuscript sub-
mitted for review November 1, 2002 and released for publication May 31, 2003.This work was supported by a contract between Delphi and The University ofAkron.
S. A. Hossain was with the Department of Electrical Engineering, The Uni-versity of Akron, Akron, OH 44325-3904 USA. He is now with Globe Motors,Dayton, OH 45404-1249 USA (e-mail: [email protected]).
I. Husain is with the Department of Electrical Engineering, The University ofAkron, Akron, OH 44325-3904 USA (e-mail: [email protected]).
H. Klode is with the DaytonTechnical Center, DelphiE&C Systems, Dayton,OH 45408 USA (e-mail: [email protected]).
B. Lequesne, A. M. Omekanda, and S. Gopalakrishnan are withDelphi Research Labs, Shelby Township, MI 48315 USA (e-mail: [email protected];[email protected];[email protected]).
Digital Object Identifier 10.1109/TIA.2003.816541
a negative torque, and limit the resolution at high speed. Am-
plitude modulation [3] is another technique to obtain the rotor
position from modulated amplitude of the sensed current. How-
ever, this technique requires external hardware circuitry, which
adds cost and complexity to the system. Another simple sensor-
less technique is based on a currentfluxrotor position lookup
table [4]. Such an approach is simple and effective, but fails at
low and zero speeds due to the flux integrator problem. Addi-
tionally, this method demands a high-memory processor to store
a good resolution lookup table. The observer-based techniques
present an attractive alternativewhere terminal measurements ofphase voltages and currents are used to model the motor char-
acteristics and calculate the rotor position [5][7]. The design
and robustness analysis of sliding-mode-observer-based posi-
tion and speed estimation are well explained in [7].
Unfortunately, all of these studies focused exclusively on the
first quadrant operation: some methods are good for low and
medium speed only, while the rest are good for medium and
high speed only. The strategies provided are not sufficient for
highly dynamic loads, which require four-quadrant operation of
the SRM. The combination of two methods, one for low speed
and the other for high speed, may solve the problem. However,
it will increase the implementation complexity, and incur addi-
tional expense for a higher memory processor and better reso-lution current sensor.
Successful sensorless motor operation for a highly dy-
namic load demands four-quadrant sensorless operation of
the SRM including zero-speed position hold. In this paper,
a sliding-mode-observer-based sensorless technique [7] with
safeguards against observer stability, flux estimator accuracy,
model imperfection, and measurement noise is used for
four-quadrant sensorless operation. The primary focus is to
find the problems associated with practical implementation
and then to solve those for the development of a four-quadrant
sensorless controller that covers a wide speed range including
low- and zero-speed operation. The developed four-quadrant
sensorless drive system has been evaluated experimentally.
II. SYSTEM DESCRIPTION
The four-quadrant sensorless SRM drive consists of an
outer loop speed or torque controller and an inner loop current
controller. The current controller has appropriate turn-on and
turn-off angles for each operating quadrant, which are set based
on a chosen criterion such as torque-per-ampere maximization
or torque-ripple minimization [8]. The firing angle positions are
switched when the motor operation changes from one quadrant
0093-9994/03$17.00 2003 IEEE
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Fig. 1. Four-quadrant sensorless SRM drive.
to another. A sliding-mode-observer (SMO)-based position
and speed estimation method is used for sensorless control.
The block diagram of the system is given in Fig. 1.
A. Brief Review of SMO
A second-order SMO for the SRM of the following form is
considered:
(1)
where
with
Here, is the estimated position, is the estimated speed,
is the error function of measured flux and estimated flux
, and are the observer gains, and is the rotor po-
sition dependent term which can be considered as 1 for mo-
toring operation and 1 for generating operation.
The SMO-based sensorless operation was previously re-
ported for one-quadrant operation [7]. For dynamic actuator
type applications, four-quadrant operation is essential. The
dynamic load demands a small convergence rate of the observer
to enhance the robustness and the poles of the closed-loop
system should be chosen accordingly.
B. SRM Model and Control Strategy
An accurate, but simplified, SRM model is desired for the
model-based estimators. The following SRM flux model [9] ex-
pressed as a function of phase current and rotor position has
been used in the implementation:
(2)
where , , , ,
Here, is the number of turns per pole, is the number
of series paths, is the number of parallel paths, is the
stack length, is the stacking factor, is the radius to rotor
pole tips, is the air-gap length, is the total length of rotor
and stator pole, is the rotor pole width, is the iron per-meability, is the relative permeability, is the saturation
flux density, is the unaligned inductance, and is phase cur-
rent. The function is related to the unsaturated phase induc-
tance characteristics of the motor. The coefficient in is a
number between 01, which depends on the profile of the unsat-
urated phase inductance characteristics. The details of deriva-
tion of the value of from geometry and material properties
are described in [9]. Fig. 2 shows the comparison of fluxcur-
rent-position characteristics for measured and model data. The
solid lines represent the measured data, and the dotted lines rep-
resent the data obtained from the model.
A four-quadrant controller for SRM drives developed in [8]
with optimal turn-on and turn-off angles in each operating quad-rant for torque/ampere maximization is chosen for motor con-
trol. The firing angle positions are switched when the motor op-
eration changes from one quadrant to another.
C. Flux Estimator
The phase flux is estimated from the integral form of
Faradays law using phase current and phase voltage
measurements
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HOSSAIN et al.: FOUR-QUADRANT AND ZERO-SPEED SENSORLESS CONTROL OF SRM 1345
Fig. 2. Comparison of fluxcurrent-position characteristics for measured andmodel data.
The flux linkage integration is implemented in discrete time
using Euler Method
(3)
where is the sampling time, and are the flux
linkages at th and th sampling instants, and and
are the phase current and phase voltage at the th sampling
instant, respectively.
III. THEORETICAL AND PRACTICAL ASPECTS
A. Existence of Information
The observer subsystem is driven by the difference between
the observer output and the plant output. The region of existence
of sliding surface and the stability of the observer on the sliding
surface must be satisfied for proper operation of the observer. Atzero speed, if there is no phase excitation, the position estima-
tion becomes unstable due to the lack of information. Therefore,
the observer needs continuous information to function properly.
B. Zero-Speed Sensorless Operation
To avoid the unobservability at zero speed with no phase cur-
rent, a high-frequency bipolar speed is commanded, which will
dither the motor at a constant position. This allows extracting
information from the response of the system. The frequency of
command speed is chosen such that it allows transferring the
excitation from one phase to another. In effect, it consists of
phase-excitation dithering. This may obviously result in somerotor movement on the order of 15 . The dithering of rotor shaft
around a fixed position allows the elimination of flux estimator
integrator problem and the successful operation of observer.
Fig. 3 shows a comparison between the rotor angular position
measured with a 360-lines-per-revolution encoder and the esti-
mated position during zero-speed operation. The measured and
estimated position matches very well, one being on top of the
other, as shown in Fig. 3. The actual and estimated speeds are
also presented for comparison. A high-frequency square-wave
speed command between 2000 and 2000 r/min is applied for
the zero-speed position-hold test. Additional copper and iron
losses are generated due to the dithering around zero speed for
Fig. 3. Measured and estimated position and speed during speed inversion andzero-speed operation.
Fig. 4. Equivalent circuit for SRM.
constant position hold. The additional power losses have a neg-
ligible impact on the efficiency of the drive system.
C. Effect of Motor Losses
The phase current component contributing to the electro-
mechanical energy conversion must be separated from the
core loss component of phase current for greater accuracy
of position estimation in model-based estimators. In order to
model the effects of core losses, the phase voltage equation for
an SRM assuming a linear SRM model (i.e., ) is
considered
(4)
where is the phase resistance, and is the phase induc-tance. A resistive element to represent the core loss is con-
sidered in parallel with theback electromotive force (EMF) term
of (4) as shown in Fig. 4.
The energy balance equation from the equivalent circuit can
be expressed as
where is the total energy supplied by the electrical source,
is the winding loss, is the energy supplied to the elec-
tromagnetic field by the electrical system, is the core
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Fig. 5. Flow diagram for the modified flux observer.
losses, and is the energy converted from the electromag-
netic field. The phase current can be divided into two com-
ponents as
where and are the currents associated with the stored cou-
pling field energy and core losses, respectively. This is re-
sponsible for producing the energy associated with the energy
conversion loop. Therefore, the flux model needs to be modified
to
(5)
where , and is a core-loss-dependentparameter, and
it varies from 0.9 to 1.0 depending on the operating motor speed.
D. Modified Flux EstimatorThe common approach to estimate the flux is to integrate the
measured phase voltage according to (3). The method works
well in the higher speed range. However, at low and zero speeds
the voltage measurement noise and integration drift pose a sig-
nificant problem. The digital sampling error sometimes results
in zero flux estimation even when the phase current is nonzero.
The performance of the simplex flux observer has been im-
proved by incorporating the phase current information more
dominantly as follows.
1) The estimator output will be greater than zero if the phase
current is nonzero. The minimum value of the flux has
been set to the minimum theoretical level of .
where .
2) The saturation flux of the SRM is the flux linkage at
the aligned position when the motor draws the maximum
current.
At low speeds, the flux estimator output may exceed the sat-
uration flux due to measurement noise, which will make the
observer unstable. The effective solution is to reset the esti-
mator output at some reasonable value when the flux estimation
reaches . The reset value is chosen as
Fig. 6. Measured current, estimated current, and estimated flux using nominalintegrator.
Fig. 7. Measured current, estimatedcurrent,and estimatedfluxusingmodifiedintegrator.
is the aligned inductance and is the unaligned in-
ductance. The algorithm of the modified flux observer is given
in the flowchart of Fig. 5.
The estimated flux using the nominal integrator is observedto have saturated at 31 mWb in Fig. 6 due to integrator problem.
Consequently, the estimated current from estimated flux be-
comes unobservable. Fig. 7 shows the measured current, es-
timated current and estimated flux using modified integrator.
The flux estimator output was reset to when the integrator
output flux saturates to .
E. Voltage Measurement
During regeneration, the kinetic energy of the motor and
load is converted into electrical energy. Therefore, the capacitor
voltage rise due to regeneration must be considered for accurate
flux estimation. Fig. 8 shows the significant increase of the
phase voltage due to the increase of the dc-link bus voltage
from the nominal value during regeneration.
F. Reference Current Lower Limit
A reference current isgenerated to maintain the command
speed or position by regulating the phase currents. Sometimes
the outer loop controller may desire a zero reference current for
strong regulation of the command signal. The zero forces
zero phase currents and, consequently, the SMO becomes un-
observable due to nonexistence of information. For the SMO to
receive the continuous information, the lower limit of the
is set to a small current level of 1 A. This may lead to a small
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Fig. 8. Measured phase voltage for four-quadrant operation.
steady-state error in the outer loop controller, but the observ-
ability of the SMO will be continuously maintained.
G. Sensorless Starting
Although the time to reach the sliding surface for the ob-
server is finite, the error may be large at startup, leading to im-
proper phase excitation, hesitation and possibly reverse rotation.To overcome this undesirable effect, the motor is driven toward
the desired direction using preset phase voltages when the load
dynamic characteristics is somewhat known. The motor starts in
an open-loop fashion in a short time, which is sufficient for the
SMO to converge. However, the open-loop starting may fail for
a highly dynamic load.
H. Implementation of SMO
From the controls point of view, the chattering noise may in-
duce a problem in the estimation accuracy due to high innova-
tion gain. However, the chattering problems can be neglected
if the system time constant is higher than the controller exe-
cution time. For the proposed four-quadrant sensorless control,the execution time is 110 s. However, the rotor time constant
is at least ten times higher than the execution
time. Therefore, the chattering noise does not affect the esti-
mated position.
I. Comparison With Table-Based Approach
In comparison with the conventional flux-current-rotor po-
sition lookup-table-based rotor position estimation technique,
the SMO-based approach delivers a robust estimation of posi-
tion and speed. The SMO exhibits high degree of robustnessin the face of model uncertainty, parameter variation, initial
rotor position error, and load torque disturbance, and possessesan automatic adaptation property with respect to the intensity
of measurement noise [10]. The lookup-table-based approach
is highly dependent on the accuracy of the static characteris-
tics of the machine. The error in flux estimation or model un-
certainty will easily lead to error in position estimation. Fur-
thermore, the motor speed in the lookup-table-based method is
obtained by differentiating the position, which may lead to sta-
bility problems during four-quadrant operation in the case of er-
roneous position estimation. On the other hand, the modification
in flux estimation helps the SMO to be observable at zero-speed
crossing, enabling the SMO to give both the rotor position and
speed simultaneously.
Fig. 9. Hardware setup for SRM drive system.
Fig. 10. Measured and estimated speed for four-quadrant speed control.
Fig. 11. Measured and estimated position during speed inversion.
IV. EXPERIMENTAL RESULTS
The prototype setup to verify the four-quadrant sensorless
control method experimentally is shown in Fig. 9. The test setup
was designed for motion control applications, which can beoperated in the variable-speed-controlled or position-controlled
loop. The controller algorithm has been implemented within a
dSPACE rapid prototyping platform. The classic bridge power
converter was used to meet the commutation requirements.
Relevant experimental results showing the performance of the
proposed sensorless scheme are presented. The SRM drive
was operated in closed-loop four-quadrant mode completely
sensorlessly using the position and speed information obtained
from the observer. Position information from an encoder is
presented for comparison only.
Figs. 10 and 11 show a comparison between the measured po-
sition and estimated position, and measured speed and estimated
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Fig. 12. Measured current, estimated current, and estimated flux in the first orthird quadrant current-controlled mode.
Fig. 13. Measured current, estimated current, and estimated flux in thevoltage-controlled mode.
Fig. 14. Measured current, estimated current, and estimated flux at secondquadrant operation.
speed, respectively, during motor speed inversion. A speed ref-erence switching from 3500 to 3500 r/min is applied, necessi-
tating four-quadrant operation of the drive system. The rotor po-
sition has been wrapped to confine measurement and estimation
within one electrical cycle. In the first and third quadrants, the
motor operates above the base speed. The measured current, es-
timated flux, andthe estimated current duringthe current control
mode and single-pulse mode for first or third quadrant operation
are presented in Figs. 12 and 13, respectively. Fig. 14 shows the
flux and current estimation for second quadrant operation. Fi-
nally, Fig. 15 shows the position estimation of the system oper-
ating at a constant, but very low speed. The speed reference in
this case is 60 r/min.
Fig. 15. Measured and estimated position at 60 r/min.
The larger difference in the measured and estimated currents
at higher speeds (Fig. 13) is due to modeling imperfections.
At higher speeds, the motor operates in the voltage-controlled
mode with lower current magnitudes. The flux value from the
motor model at lower current levels differs significantly from
the actual value for a given current as can be seen from Fig. 2.This effect is reflected in the measured and estimated current
of Fig. 13. However, the SMO is robust enough to overcome
the model inaccuracy and provide correct position and speed
information.
V. CONCLUSION
This paper presented a four-quadrant sensorless controller de-
veloped in a test bench considering the practical implementa-
tion issues. The motor speed command was toggled from one
rotational direction to another through zero speed without any
mechanical position sensor. The rotor position of the SRM is es-
timated at zero operating speed by imposing a high-frequency
speed command. The flux estimator and the SR motor modeling
imperfection were modified to reduce the cumulative error at
zero and low speeds. The experimental results demonstrate the
feasibility of the proposed four-quadrant sensorless scheme.
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[9] S. A. Hossain and I. Husain, A geometry based simplified analyticalmodel of switched reluctance machines for real-time controller imple-mentation, in Proc. IEEE PESC, Cairns, Australia, June 2002, pp.839844.
[10] M. S. Islam, I. Husain, R. J. Veillette, and C. Batur, Design and per-formance analysis of sliding-mode observers for sensorless operationof switched reluctance motors, IEEE Trans. Contr. Syst. Technol., sub-mitted for publication.
Syed A. Hossain (S01M02) received the B.Sc.and M.Sc. degrees in electrical and electronic engi-neering from Bangladesh University of Engineeringand Technology, Dhaka, Bangladesh, in 1994 and1997, respectively, and the Ph.D. degree in electricalengineering from The University of Akron, Akron,OH, in 2002.
From 1994 to 1998, he was a Lecturer and thenan Assistant Professor at Bangladesh University ofEngineeringand Technology. In the summers of 2000and2001, he waswith DelphiResearch Laboratories,
Shelby Township, MI. He is currently a Senior Project Engineer with GlobeMotors, Dayton, OH, where he is engaged in the design and development ofcontrols for brushless motors. His technical interests include the developmentof high-performance brushless motor servo drives for automotive applications.
Iqbal Husain (S89M89SM99) receivedthe B.Sc. degree from Bangladesh University ofEngineering and Technology, Dhaka, Bangladesh,in 1987, and the M.S. and Ph.D. degrees from TexasA&M University, College Station, in 1989 and 1993,respectively, all in electrical engineering.
He is currently a Professor in the Department ofElectrical and Computer Engineering, The Univer-sity of Akron, Akron, OH, engaged in teaching andresearch. He was a summer researcher at WrightPatterson AFB Laboratories in 1996 and 1997.
Previously, he was a Lecturer at Texas A&M University and also a ConsultingEngineer with Delco Chassis, Dayton, OH. His research interests are in theareas of control and modeling of electrical drives, design of electric machines,and development of power conditioning circuits. He has worked extensively
in the development of switched reluctance motor drives, including sensorlesscontrollers.
Dr. Husain received the 2000 IEEE Third Millennium Medal and the 1998IEEE Industry Applications Society Outstanding Young Member Award. He isalso the recipient of three IEEE Committee Prize Paper Awards.
Harald Klode received the Dipl. Ing. degree inelectrical engineering from the Rheno-WestphalianSchool of Technology (RWTH), Aachen, Germany,in 1984.
In 1985, he was a Research Assistant in the De-partment of Electrical and Computer Engineering,University of Colorado, Boulder. From 1986 until1988, he was with the General Motors ResearchLaboratories, Warren, MI, working in the areas of
electromechanical actuators and motors for vehicularsystems. He continued his work on various brush,
brushless, and SR motor-and-actuator-related projects at Delco Products,Delphi Chassis, ITT Automotive, and VALEO in Dayton, OH. In 1999, he joined Delphis Technical and Innovation Center in Dayton, OH, where he iscurrently a Senior Research Engineer and Team Leader for Advanced MotorDevelopment for Controlled Braking Systems. He is the holder of severalU.S. and international patents and has published papers in the areas of electricmotors. His current interest is focused on the development of mechatronics andactuators for automotive applications.
Bruno Lequesne (M85SM89F97) received theCertified-Engineer degree from the Ecole SuprieuredElectricit, Gif-sur-Yvette, France, in 1978, and thePh.D. degree in electrical engineering from the Uni-versity of Missouri, Rolla, in 1984.
His is currently a Senior Staff Research Engineerwith Delphi Research Labs, Shelby Township, MI.His research interests are in the areas of electricalautomotive systems, drive-by-wire mechatronic sys-
tems, power generators, sensors, and related issues.He is the holder of 25 patents, primarily on sensors and linear actuators.Dr. Lequesne is the recipient of several Best Paper Awards from the IEEE
Industry Applications Society (IAS), its Electrical Machines Committee, andthe Society of Automotive Engineers.
Avoki M. Omekanda (M95SM97) receivedthe bachelors degree in physics from MohammedV University, Rabat, Morocco, in 1984, and the
Engineer and Ph.D. degrees in electrical engineeringfrom the Facult Polytechnique de Mons, Mons,Belgium, in 1987 and 1993, respectively.
Following the receipt of the Engineers diploma,he worked for A.C.E.C Corporation, Charleroi, Bel-gium. In January 1990, he joined the Facult Poly-technique de Mons as a Research Engineer. His re-search interests included computer-aided design for
switched reluctance machines and magnetic field computation using numer-ical methods. After receiving the Ph.D. degree, he was an Assistant Professorin the Electrical Engineering Department, Facult Polytechnique de Mons, fortwo years. In June 1995, he joined the General Motors Research and Develop-ment Center, Warren, MI, as a Senior Research Engineer. In 1999, he becamepart of Delphi Research Labs, Shelby Township, MI, where he is currently aStaff Research Engineer. His research interests include design, analysis, andcontrol of electric machines, in particular, switched reluctance, for automotiveapplications.
Dr. Omekanda is a Member of the Association des Ingnieurs de Mons (Bel-gium) and Socit des Electriciens et des Electroniciens (France).
Suresh Gopalakrishnan (S95M00SM03)received the B.E. degree from Annamalai University,Annamalai Nagar, India, in 1989, the M.S. degreefrom Indian Institute of Technology, Chennai, India,in 1992, and the Ph.D. degree from Texas A&M
University, College Station, in 2000, all in electricalengineering.
From June 1992 to August 1995, he was with theR&D department of Kirloskar Electric Company,Bangalore, India. In January 2000, he joined theMechatronics Group at Delphi Corporation, Shelby
Township, MI, where he is involved with automotive power electronics andmotor drive applications. His research interests include power electronics, con-trol of variable-speed motor drives, and microcontroller and DSP applicationsin automotive actuators.