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Electrical Load Emulator for Unbalanced Loads and
with Power Regeneration
Y. Srinivasa Rao∗
Department of Electronics Engineering
Sardar Patel Institute of Technology
Mumbai, India 400 058
Email: [email protected]
Mukul Chandorkar
Department of Electrical Engineering
Indian Institute of Technology
Mumbai, India 400 076
Email: [email protected]
Abstract—The paper presents a method of emulating electricalloads using power electronic Voltage Source Inverters (VSIs). Theloads include machines such as induction motors and three phasediode rectifiers as well as larger electrical systems. The emulationof unbalanced four-wire loads has been achieved using a four-legVSI. The load emulator is effectively a dynamically controllablesource or sink which is capable of bidirectional power exchangewith either a grid or another power electronic converter system.Using load emulation, the feasibility of connecting a particularmachine to a grid or converter under various load conditionscan be examined without the need for any electromechanicalmachinery. The additional feature of the load emulation tech-nique described in the paper is the feedback of power absorbedby the emulator back to the grid. This feedback of power hasbeen termed as power regeneration and has been achieved byanother VSI in current controlled mode with the referencesgenerated using instantaneous p-q-r theory. The consistency ofthe experimental results with the simulation results proves theability of emulator and the proposed testing approach.
I. INTRODUCTION
Load emulation is the concept of controlling a power
electronic converter such as a Voltage Source Inverter (VSI) in
such a manner that its behavior resembles that of an electrical
load such as an induction machine. Real-time simulation
[1]–[6], rapid prototyping [7], [8], hardware-in-loop (HIL)
technologies [9]–[14] used to test control design have been
well reported in literature. In contrast, load emulation as
presented in this paper provides a platform where the behavior
of an electrical load can be emulated in hardware at real power
levels using a controllable VSI. The load emulator can provide
different load characteristics with which the control algorithms
and inverter design can be tested [15], [16]. Therefore, load
emulation offers a more flexible platform for testing inverters
in a laboratory environment.
The load emulator consists of a VSI with its output filter
that can draw or supply currents so that it behaves as the load
that is desired to be emulated. As shown in Fig. 1, an inductor-
capacitor-inductor (L-C-L) filter is chosen as the output filter
to remove the switching frequency harmonics generated by
the VSI. The method to design the L-C-L filter with respect
to the switching frequency of the VSI has been described.
The four-leg VSI has been chosen as the topology of the
emulator VSI since the loads to be emulated are four-wire
unbalanced loads. Moreover, since the VSI draws or supplies
idc
Lf
Ls
Cf
Vdc
n vsavsbvsc
Cdc
isa
Regen.
Converter
Fig. 1. Schematic diagram of four-leg emulator with LCL filter.
current from another source to emulate a load, another VSI
has been connected between the dc link of the load emulator
VSI and the ac grid to regulate the dc bus voltage of the
load emulator VSI. This auxiliary VSI has been termed as
the Regenerative Converter and is a bidirectional power flow
converter.
In a distribution system, the undesirable operation of loads
can adversely affect the source. This is particularly the case
when the source is another VSI. An example is that of a
faulty induction motor fed by a three phase VSI in V/f
control mode. For this purpose, the load emulator has been
made to emulate loads such as the faulty induction motor and
severely unbalanced loads. The results will show the excellent
performance of the load emulator in all the cases. The results
will also show the performance of the Regenerative Converter
and how power is exchanged between the ac grid and the dc
bus of the load emulator VSI.
The current control technique of both the load emulator VSI
and the regenerative converter has been described in [17]. In
this paper, the optimal control technique described in [17] has
been extended for the four-leg VSI. [17] also describes the
method of generating references for the currents to be drawn
by the load emulator VSIs. The Phase Locked Loop (PLL)
that is used in generating smooth sinusoidal templates of the
978-1-4673-0158-9/12/$31.00 ©2012 IEEE 320
+
if (s) is(s)sLf sLs
vs(s)
vf (s)
U(s)Vdc
1/sCf
Fig. 2. VSI with L-C-L filter.
(i)
(ii)
Fig. 3. Transfer function for an LCL filter.
grid voltages has been described in the [17]. Furthermore, the
model of the healthy induction motor and other loads such as
diode rectifiers has been described in [17].
II. DESIGN OF THE L-C-L FILTER
In this section, a procedure to design the LCL filter has
been discussed [18], [19]. The parameters of the LCL filter
have been designed with respect to the resonance frequency
of the filter using the transfer function approach in the splane. Detailed frequency responses of the LCL filter have
been presented in the later part of this section.
Fig. 2 shows the Laplace transform of the circuit with VSI
interfaced through an LCL filter to the ac grid. It is to be noted
that the resistances associated with the inductors Lf and Ls
have been ignored for simplicity. When compared with the
exact Bode plots, it will be observed that the deviations are
minimal. The expression for the resonant frequency of the LCL
filter can be written as
ω0 =
√
Lf + Ls
LfLsCf
(1)
The above expression for the resonant frequency provides
a criterion for designing the LCL filter parameters i.e. Lf ,
Ls and Cf . The gain of the transfer function will fall at a
-60 db/decade after the resonant frequency of ω0. In order to
produce a current is that is devoid of the switching frequency
harmonics that are generated by the VSI, the switching fre-
quency should be chosen sufficiently higher than the resonant
frequency ω0. The switching frequency of the VSIs in the
case of the load emulator is around 10 kHz. Therefore, to
provide adequate filtering capability, the resonant frequency
of the filter has been chosen to be 800 Hz. The filter capacitor
Cf being available only in discrete values is chosen to be
50 µF. The filter inductor Lf has been chosen to be 1 mH.
Therefore, from Eqn. (1), the desired value of Ls is obtained as
3.79 mH. The value of inductor closest to the desired value that
was available in the laboratory was 3 mH. Therefore, Ls has
been chosen to be 3 mH. This results in a resonant frequency
of 821 Hz which is acceptable. These designed values of LCL
filter parameters are used in the simulation and experimental
results.
The transfer function between the current injected by the
VSI into the ac grid and the control signal for a VSI interfaced
to the grid using an LCL filter is shown in Fig. 3. The
frequency response characteristics of the VSI with LCL filter
has a resonance peak at approximately 795 Hz. Moreover, the
gain of the transfer function is not sufficiently low at the range
of frequencies where the switching frequency component
occurs. Therefore, the objective of the controller will be to
increase the gain at lower frequencies to ensure that current
references are tracked with negligible error. Moreover, the
switching frequency of the VSI has to be chosen sufficiently
higher than the resonance frequency.
III. CONTROLLER DESIGN
The control system ensures that the emulator draws a
current is that is approximately equal to the desired reference.
The transient response of the system determines the tracking
accuracy between the demanded and actual current drawn
from the inverter under test. Here the control technique used
is a state feedback control strategy. The literature contains
several methods of controlling a VSI with LC filter. Many
of these are PI controller based. However, for such a multi-
variable dynamical system, control of more than one variable
simultaneously would yield better performance. The LQR is
a method of designing a state feedback controller that enables
the control signal to be affected by the errors in all state
variables simultaneously. The primary advantage of using such
a state feedback controller is the ease in implementation.
The final control implementation merely requires the errors
in the state variables to be multiplied by their respective gain
constants and the final products to be summed. This leads to
ease of implementation especially for load emulation where
the code execution time is required to be of the order of 10
µs.Fig. 4 shows the closed loop control scheme employed for
the VSI of Fig. 3. The state vector chosen is:
x = [is vf if ]T (2)
The state space equations are obtained by applying Kirchoff’s
Current Law and Kirchoff’s Voltage Law to Fig. 3:
x =
−rs/Ls −1/Ls 01/Cf 0 −1/Cf
0 1/Lf −rf/Lf
x
+
00
−Vdc/Lf
u +
1/Ls
00
vs (3)321
cr
+−
e
x
x uu yInverter
Hysteresis
switchingK
Fig. 4. Closed loop control scheme of the optimal feedback controller.
y = is = [1 0 0] x (4)
The output variable y is therefore the current is that is
injected into the grid. However, as stated in the previous
section both currents if and is are measured. The voltage vf
across the filter capacitor Cf also forms the state vector along
with if and is. However, its measurement has been excluded
(a description has been provided later in the section).
The objective of the VSI is to inject a current is that is
approximately equal to a desired reference isr. In the above
equation, u is the emulator inverter’s switching function and
ac grid voltage vs is considered to be a disturbance. The state
feedback controller is an optimal controller designed using the
Linear Quadratic Regulator (LQR) to achieve the objective.
For implementation using DSP, the controller is realized in
a discrete-time form. The continuous time state equations are
converted to standard state space discrete-time form.
x(n + 1) = Gx(n) + Huu(n) + Hww(n) (5)
y(n) = Cx(n) (6)
In this w(n) = vs(nTs) is a disturbance, and Ts is the sam-
pling time interval. The LQR seeks to minimize a performance
index,
J =1
2
∞∑
n=0
[
eT (n)Qe(n) + ucT (n)Ruc(n)
]
(7)
where e = xr−x and the T stands for the transpose of a vector.
Here (7), Q is a diagonal matrix that decides the importance
to be given to the state variables and R is the penalty which is
imposed on the controller. The dlqr function of the simulation
provides the state feedback matrix K,
uc(n) = K (xr(n) − x(n)) (8)
x(n + 1) = (G − HuK)x(n) + HuKxr(n) + Hww(n) (9)
Y (n) = Cx(n) (10)
To obtain the transfer function between the output variable
y and the reference state vector xr, the disturbance w(n)is neglected. Equations (9), (10) are the closed loop state
equations. The system parameters are chosen as Ls = 3 mH,
Rs = 0.01 Ω, Lf = 1 mH, Rf = 0.01 Ω, Cf = 50 µF. Thechoice of Q and R are:
Q =
50 0 00 0.05 00 0 0.01
;R = 65 (11)
where the weightage for is is chosen to be much larger than the
other states in the matrix Q. K = [0.6188 0.0404 0.0929]
with a sampling time of 20 µs. Since the control coefficient
for error in vf is extremely small [0.0404], it is possible to set
this constant at zero. In the case of the emulator presented in
this paper, it was found reasonable to neglect the value 0.04.
This lead to a reduction in the measurement requirement of
vf , and the controller functioned without measuring the filter
capacitor voltages.
The control signals ua, ub, uc for the three phases a, b, c aregenerated from the state feedback control strategy. However,
the fourth leg of the VSI is controlled by applying hysteresis
control to the following control signal:
un = −(ua + ub + uc) (12)
The hysteresis band was chosen such that the average switch-
ing frequency was about 5 kHz. The switching losses in the
emulator inverter at this switching frequency were well within
the maximum permissible losses.
IV. SIMULATION RESULTS
It is desired that the faulty induction motor be emulated
using Digital Signal Processor. This section will describe the
mathematical model that will be solved iteratively to emulate
the faulty induction motor. Fig. 5 shows an equivalent circuit
diagram of three phase induction motor with stator inter-turn
fault [20]–[22]. The model is represented using differential
equations (13) to (20). In this model, fault is not considered
symmetrical with other two phases of the stator. Eqns. (13)
to (18) shows three phase induction motor having stator inter-
turn fault in stationary q-d frame. Eqn. (19) shows the relation
between machine current with machine flux linkage, where
A is the inductance matrix. Eqn. (20) is the electromagnetic
torque equation.
θ r
Rs
Rsibs
ias
ics
N s
N s
iar
ibr
icr
N r
N r
N r
ifRfRsµ
N sµ
N s
Rs
N
N
Stator
Rotor
A
CB
A
C
B
i − ias f
R
R
Rr
r
r
Fig. 5. Induction motor with stator inter-turn fault.
322
d
dtλqs = vqs − Rsiqs +
2
3µRsif (13)
d
dtλds = vds − Rsids (14)
d
dtλqr = −Rriqr − ωrλdr (15)
d
dtλdr = −Rridr + ωrλqr (16)
d
dtλf = −µRsiqs + (µRs + Rf ) if (17)
d
dtωr =
P
2
(
Tem − TL
J
)
(18)
i = A−1λ (19)
where,
i =[
iqs ids iqr idr if]T
λ =[
λqs λds λqr λdr λf
]T
A =
Ls 0 M 0 −Lqs
0 Ls 0 M −Lds
M 0 Lr 0 −Lqr
0 M 0 Lr −Ldr
1.5Lqs 1.5Lds 1.5Lqr 1.5Ldr −Lff
and
Tem =3P
4M
(
isqsisdr − isdsi
sqr
)
−
3P
4Ldr
(
isqrif)
+3P
4Lqr (isdrif ) (20)
where λ is the flux linkage, i = current, v = voltage, Rs = stator
resistance, Rr = rotor resistance, Rf = external resistance to
limit the fault current, ωr = electrical angular speed, µ =Nf
Ns
is the extent of fault, if = fault current, M = 3/2 ·Lms, Ls
= Lls + 3/2 ·Lms, Lr = Llr + 3/2 ·Lms, Lqs = q-axis stator
inductance due to fault, Lds = d-axis stator inductance due to
fault, Lqr = q-axis rotor inductance due to fault, Ldr = d-axis
rotor inductance due to fault, Lff = self inductance of fault
loop.
TABLE IIM PARAMETERS WITH STATOR INTER-TURN FAULT
Rs = 4.9 Ω Rr = 8.1 Ω Rf = 2.64 Ω
Ls = 0.8416 H M = 0.8095 H Lqs = 0.0442 H
Lds = 0.0160 H Lqr = 0.0440 H Ldr = 0.0160 H
Lff = 0.0043 H J = 0.0967 kgm2 P = 4
µ = 0.0833 L − Lvg = 415 vrms Freq. = 50 Hz
Fig. 6 shows the simulation of faulty induction motor using
the two-step Adams-Bashforth integration method with a 20
µs time step. For simulations, the motor with parameters
mentioned in Table I is taken as a reference model. The peak
value of the stator current goes as high as 15 A peak to
peak while starting, which is approximately 8-10 times the
steady state value of full load. From the simulations results
of Fig. 6, it can be seen that unbalanced current references
isa ref , isb ref , isc ref can be tracked with negligible error.
The lower trace shows the tracking performance of a-phase
current. The results of transient response and stability of the
system are shown in [17].
0 0.1 0.2
-10
-5
0
5
10
0
-10
0
10
(i)
(ii)
isa refisb ref isc ref
isa
Time (s)A
A
Fig. 6. Simulation of faulty induction motor with current controller.
V. EXPERIMENTAL RESULTS
A three-phase experimental setup has been built to verify
the accuracy of the proposed system. In this setup the power
circuit is rated at 30 A, 415 V input/output line to line
voltages and 750 V dc bus. Various linear and nonlinear
current references, representing different load characteristics,
are emulated experimentally.
A Digital Signal Processor (DSP), Field Programmable Gate
Array (FPGA) digital hardware system has been designed
to implement load emulation experimentally. In order to get
flexible I/O interface and data acquisition, this system has three
analog to digital converters and a Xilinx XC3S200 FPGA.
Three AD7864-AS2 analog to digital converters are interfaced
to sensor unit for data acquisition of voltage and currents.
Texas Instruments TMS320VC33 DSP is used as a processor
to simulate the load model and generate the current references
with a 75 MHz clock. FPGA act as a pulse width modulator
and control the power switches of the converter using 20 MHz
clock reference.
A. Induction Motor with stator inter-turn fault
Fig. 7 shows experimental emulated results of a faulty
motor’s load model a-phase start up current. The upper trace
shows the output voltage vsa of source VSI. The fundamental
frequency of the source VSI is 50 Hz. The middle trace shows
reference currents isa ref , isb ref , isc ref of faulty induction
motor model. The lowest trace shows tracking performance
of source VSI a-phase reference current isa ref and measured
current isa. Fig. 8 shows experimental results of faulty IM load
model for VSI in constant v/f control mode. The upper trace
shows the unbalanced variable frequency current references
and the lower trace shows the reference and the measured
currents in a-phase. These results verify the simulation results
of Fig. 6 and demonstrate that this control system can be used
to test the inverters even for the faulty motor load models.
323
0 0.05
-200
0
200
0 0.1 0.2
-10
0
10
0 0.1 0.2
-10
0
10
(i)
(ii)
(iii)
isa,sb,sc ref
isa refisa
vsa
VA
A
Time (s)
Fig. 7. Experimental results: emulation of faulty induction motor with sourceVSI.
0 0.5 1
-6
-4
-2
0
2
4
6
0 0.1 0.2 0.3 0.4 0.5
-5
0
5
(i)
(ii)
isa ref
isa ref
isb refisc ref
isa
AA
Time (s)
Fig. 8. Experimental results: faulty IM for v/f control source VSI.
B. Severely unbalanced load
This section deals with the emulation of electrical loads
drawing unbalanced currents such that the sum of the phase
currents is not zero. The emulation of such loads needs a
four-leg inverter. Fig. 9 shows experimental results of four-
leg emulator for two phase load current references. Reference
phase currents are isa = 8 A, isb = 8 A, (peak to peak) and
isc = 0. The upper trace of Fig. 9 shows the emulator phase
currents and the lower trace shows neutral current controlled
by the fourth leg of emulator. The peak to peak neutral current
in is 8 A.
C. Unbalanced leading/lagging power factor load
Fig. 10 shows experimental results of four-leg emulator,
emulating unbalanced leading power factor load current ref-
erences. For experimentation the reference currents are isa =
10 A, isb = 8 A, and isc = 6 A (peak to peak). Figure shows
the a-phase current with a leading power factor of 0.7. Theupper trace also shows the resultant neutral current controlled
by the fourth leg of emulator and the lower trace shows the
tracking performance of a-phase current.
0 0.05 0.1-10
0
10
0 0.05 0.1-10
0
10
0 0.05 0.1-10
-5
0
5
10
0 0.05 0.1-10
-5
0
5
10
(i)
(iii)
(ii)
(iv)
in
isa
isb
isc
AA
AA
Time (s)
Fig. 9. Experimental results: four-leg emulator for two phase currentreferences (isc = 0).
0 0.05 0.1
-50
0
50
0
-10
0
10
(i)
(ii)
isa ref
isa
isavsain
AV,A
Time (s)
Fig. 10. Experimental results: four-leg emulator for leading power factorload.
0 0.05 0.1
-50
0
50
0 0.05 0.1-50
0
50
(i)
(ii)
isa vsain
errorsignal(isa ref − isa)
AV,A
Time (s)
Fig. 11. Experimental results: lagging power factor load emulation.
The upper trace of Fig. 11 shows experimental results of
a-phase current for a lagging power factor of 0.2. The current
references are chosen as isa = 10 A, isb = 8 A, and isc = 6
A (peak to peak). The lower trace shows the tracking error
324
0 0.05 0.1-20
-10
0
10
20
0 0.05 0.1-20
-10
0
10
20
0 0.05 0.1
-20-100
1020
0 0.05 0.1-30-20-100
102030
(i)
(ii)
(iii)
(iv)
isa
isb
isc
in
AA
AA
Time (s)
Fig. 12. Experimental results: four-leg emulator for nonlinear unbalancedload.
between reference and measured a-phase source currents.
D. Unbalanced nonlinear load
Fig. 12 shows the experimental waveforms of four-leg
emulator for three single phase diode bridge rectifiers with
neutral connected and unbalanced load model. Figure shows
unbalanced current references isa = 16 A, isb = 20 A, and
isc = 22 A (peak). The lowest trace shows the fourth leg
current in. From the results, it can be observed that the
controller constantly trace the reference currents of nonlinear
unbalanced active loads. The tracking performance of the
controller remains same even during the periods when the
reference remains zero.
VI. POWER REGENERATION
The regenerative converter serves as the utility end of the
emulator. This feature permits the load emulator system to
return the power taken by the emulated “load” back to the
utility. It does this by maintaining closed-loop control of the
common dc bus voltage, as shown in Fig. 13. The regenerative
converter essentially controls the dc bus voltage to be equal
to a reference, Vdc ref . Fig. 13 shows the control scheme for
the regenerative converter. The compensation and the power
exchange is based on instantaneous p-q-r power theory [23],
[24]. Therefore, in addition to the bidirectional active power
exchange the regenerative converter can also can be used for
general power quality conditioning such as a multifunctional
compensator.
In the p-q-r theory, the instantaneous active power exists
only along the p-axis. The instantaneous powers along the qand r axes are imaginary or reactive powers and are denoted
as qq and qr, respectively. The relation between instantaneous
power and instantaneous load currents in the p-q-r reference
frame is given as:
pqq
qr
=
epip−epirepiq
(21)
+
pcc3-phasesource
transformer e(a,b,c)
Regen.
converter
3-phase
Powerreference
gate pulsescurrent
controllerPWM
modulator
abc to 0αβ0αβ to pqr
pqr to 0αβ0αβ to abc ic
ic ref
Pref load
Vdc link
Vdc ref
idc
PI
Pdclink
Cdc
Fig. 13. The dc bus voltage regulation control system.
where, ep and [ip iq ir] are the Point of Common Coupling
voltage and converter currents in p-q-r reference frame, re-
spectively.
The power reference Pref load for the converter is set based
on the power calculated from the emulated load model. The
term Pref load is then added to the reference active power
Pdclink which is required to regulate the dc bus voltage. The
relation between dc link voltage, dc bus capacitor and the dc
bus power is given as:
Vdc =Pc dc loss + Pdclink
Cdc · ∆Vdc · fripple
(22)
In this expression, ∆Vdc is the permissible ripple on dc link
voltage and fripple is the minimum ripple frequency. For a
specified dc link voltage and with the given permissible ripple
and minimum ripple frequency, the dc link capacitance re-
quired is directly proportional to the p-axis active power drawnby the converter. The numerator of the above expression is the
total instantaneous p-axis power drawn by the compensator.
The term Pc dc loss is the average active power required to
meet the losses in the converter. The term Pdclink is the
average active power corresponding to the power exchange
across the dc bus.
The converter reference currents for the PWM current
controller are calculated in p-q-r reference frame from the
combined reference power by using reverse transformations
as mentioned in [25]. The output of the current controller is
then given to the PWM modulator to get the desired gating
pulses for the converter. In the dc bus regulation loop the actual
dc bus voltage is measured and compared with the reference
Vdc ref . A PI controller is used to compensate the error [26].
Fig. 14, 15 shows the experimental results of bidirectional
active power exchange. Fig. 14 shows the transient ac grid
voltages ea, eb, ec and currents isa, isb, isc seen from the
regenerative converter PCC. The regenerative converter ini-
tially acts as a normal compensator for reactive power and
harmonics; then the emulator is switched on intermediately.
This results in the loading of the common dc bus. At this
325
25V/div 4A/div
50V/div
ea
eb
ec
isa
isb
isc
vdc
(i)
(ii)
(iii)
(iv)
Fig. 14. Experimental results: positive active power transfer by regenerativeconverter.
(iv)
(iii)
(ii)
(i)
Fig. 15. Experimental results: negative active power transfer by regenerativeconverter.
instance, the emulator inverter draws the active power from
the dc bus and transfers it to the ac grid. The regenerative
converter tries to maintain the dc bus voltage by drawing the
active power from the ac grid through an isolation transformer.
Fig. 15 shows the steady state waveform of the voltages
and currents of the regenerative converter. Here the emulator
inverter draws active power from the ac grid and transfers it to
the dc bus. The dc bus would rise if the regenerative converter
is not switched on. The regenerative converter regulates the
common dc bus while transferring the additional average active
power from the dc bus to its ac grid, performing regenerative
power transfer. The 180 degree out of phase line currents with
reference to utility voltages are seen from the Fig. 15. This
demonstrates the negative active power transferred from the
common dc bus.
VII. CONCLUSIONS
This paper has focused on the emulation of unbalanced four
wire loads that are very common in a low voltage distribution
system. Moreover, the regenerative technique employed to
supply the power absorbed by the emulator VSI back to
the grid enables the emulation of high power loads. The
results show the emulation of a variety of loads such as the
faulty induction motor, severely unbalanced loads and neutral
connected unbalanced diode rectifier loads. The performance
of the emulator in drawing currents close to the desired
currents has been shown through experimental results. The
smooth waveforms of the output current are the result of the
good design of the LCL filter.
The capacity of the emulator is limited by the power rating
and bandwidth of the system. A minimum real-time step of 20
µs has been achieved using this platform. This time resolution
is sufficient to simulate the dynamic behavior of most power
electronics control systems and electrical load models.
ACKNOWLEDGMENT
The author∗ is thankful to the Power electronics and power
systems (PEPS) group of IIT-Bombay, India and Sardar Patel
Institute of Technology, Andheri-W, Mumbai for providing the
necessary facilities for carrying out this work.
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