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Design of an almost continuously controlled three-phase static VAR compensator for power factor
correction purposes
Abdulkareem Mokif Obais* and Jagadeesh Pasupuleti
Department of Electrical Power Engineering, Universiti Tenaga Nasional, Malaysia.
Accepted 31 October, 2011
In this paper, a three-phase four-wire automatic power factor correction system is designed and tested. This system employs three-phase Wye-connected thyristor switched-capacitor banks to generate a controllable static VAR. Each capacitor bank is constructed of five binary weighted thyristor switched-capacitors. This arrangement leads to a capacitor bank capable of generating stepping reactive power having thirty one equidistant non-zero levels. The controlling circuit of each capacitor bank is designed such that maximum absolute deviation from linear response is 1/62 of its rating. Each capacitor is controlled by a single thyristor shunted by a reverse diode. The system is capable of correcting lagging power factor up to unity or adjusting it according to user desire. Each capacitor is connected to a series reactor for protecting the solid state combination from inrush current occurring at the first instant of compensator plug in to power system network. The proposed system is characterized by negligible no load operating losses, no generation of harmonics, energy saving, and reduction of transmission losses. The system is designed and implemented on PSpice which is a computer program very close in performance to real hardware and broadly adopted by manufacturing companies. Key words: Capacitor bank, power factor correction, power quality, static VAR.
INTRODUCTION Power factor improvement leads to a big reduction of apparent power drawn from the ac source which in turn saves energy and minimizes the transmission losses (Mehrdad, 2005; Dai et al., 2007; Lupin et al., 2007). It generally employs means that control reactive power in power system network (Gyugy et al., 1978). The process is usually denoted by reactive power compensation which is a productive technology employed for improving power systems performance. This technology serves customers and power system networks. Power quality is an insisting challenge in ac power systems, whereas reactive power compensation techniques offer striking solutions on the *Corresponding author. E-mail [email protected].
route of its achievement. Reactive power control solves or attenuates many power system problems such as poor voltage regulation, line currents unbalance, poor power factor, and reduced efficiency. There are so many techniques approaching reactive power control, but the static VAR compensators are the most reliable ones, since they present high flexibility in design methodology and exhibit reasonable response amongst fast varying environments (Miller, 1982). Static VAR compensators are either series or shunt compensators. Series compensators deal with modification of distribution or transmission parameters of the ac system, while shunt compensators decide the load equivalent impedance (Miller, 1982; Teleke et al., 2008). Both types of compensators can be used to control the reactive power for power factor correction purposes in ac power systems.
220 Sci. Res. Essays Synchronous condensers and manually switched capacitors or inductors can be used for power factor correction purposes, but. static VAR compensators using thyristor switched- capacitors and thyristor controlled reactors are superior to them, since they are characterized by fast response and high design flexibility (Teleke et al., 2008). Fixed capacitor-thyristor controlled reactor (FC-TCR) compensators are widely used for power factor correction purposes. They offer the feasibility of continuous reactive power control, but they exhibit full load operating losses at relaxation time, since the TCR is operating at its full capacity in order to absorb the reactive power generated by the fixed capacitor (Chen et al., 1999). In addition they release large amounts of harmonic current components which increase transmission losses and disturb the power system network voltage profile (Best and La Parra, 1996). The TCR is a source of harmonics, where the third harmonic for instance is about 13% of the TCR rating (Chen et al., 1999). This reveals the need for harmonics filters which add more complexity and more operating and transmission losses (Lee and Wu, 2000). Static VAR compensators using switched-capacitor banks offer stepping responses in reactive power generation mode and their losses are proportional to the reactive power demands (Nandi et al., 1997). FC-TCR and switched capacitor banks static VAR compensators are usually referred to as conventional static VAR compensators which are basically characterized by the employment of naturally commutated solid-state switching devices having high voltage and current ratings.
Employment of converters with an appropriate pulse width modulation control technique, permits the implementation of static VAR compensators capable of generating or absorbing reactive power with fast time response (Walker, 1986; Stahlkopf and Wilhelm, 1997). The recent developments in power electronics devices offer high amount of flexibility in static VAR compensators design for power factor correction and voltage control purposes. The new generations of these devices are characterized by fast responses, wide frequency spectrums, wide safe operating areas, low switching losses, low ON and OFF times, and easy commutation (Rashid, 2001; Bimal, 2006). Basing on the above facts and the recent analytical computations, Flexible AC Transmission Systems (FACTS) appear as a new concept in power transmission systems (Idris et al., 2010).
These new technologies make it easy to present static VAR compensators having fast response and capable of increasing the amount of apparent power through a transmission line in the neighborhood of its thermal capacity, without exceeding its stability limits. These new technologies are limited to low voltage applications, since they are employing fast solid-state switching devices having relatively low voltage and current ratings (Rashid,
2001; Bimal, 2006).
Here in this paper, a reliable switched-capacitors technique is adopted for three-phase automatic power factor correction purposes. The technique is based on designing a switched-capacitor bank exhibiting almost linear response versus reactive power demand. This technique solves the linearity problem of static VAR generation and offers the feasibility of operation at high voltage and current ratings, since it employs solid state switching devices having high ratings. In addition, the proposed technique is harmonic free, thus no harmonic filters are required. THE CAPACITOR BANK CONFIGURATION The proposed capacitor bank is composed of five binary weighted capacitors as shown in Figure 1a. This configuration offers 31 non-zero levels of possible capacitive reactive current as shown in Figure 1b. Each capacitor is controlled by a single thyristor shunted by a reverse diode. The thyristor handles the positive half cycle of the capacitor current and the diode deals with the negative half cycle. Reactors LS1 to LS5 are current limiters. THE PROPOSED SINGLE-PHASE SYSTEM The single-phase power factor correction system block diagram is shown in Figure 2. The capacitor bank triggering circuit is excited by two signals. The first signal is KiL, where K is the attenuation factor of the current transformer (C.T) circuitry and iL is the instantaneous load current. The second signal is K*v, where K* is the attenuation factor of the voltage transformer (V.T) circuitry and v is the instantaneous phase voltage.
The load voltage and current can be given by:
tVv m sin (1)
)sin( tIi mL (2)
Where Vm is the load voltage amplitude in volts, Im is the load current amplitude in amperes, φ is load current power factor angle in radians, and t is time in seconds. The first zero-crossing detector in Figure 2 converts K*v to a rectangular waveform V1 which is then differentiated and half-wave rectified by the first RC differentiator/rectifier, forming V2. The latter is a train of pulses used to trigger the sample and hold circuit at ωt = nπ, where n is a positive odd integer. The analogue differentiator converts K*v to the analogue signal V3
Obais and Pasupuleti 221
C
1
2
2C
1
2
8C
1
2
4C
1
2
16C
1
2
T1 DT1
12
T2 DT2
12
T3 DT3
12
T4 DT4
12
T5 DT5
12
V
LS1
1
2
LS2
1
2
LS3
1
2
LS4
1
2
LS5
1
2
Line
Neutral
(a)
I
2I
6I
4I
10I
8I
14I
12I
18I
16I
22I
20I
26I
24I
30I
28I
32I
10II
2I
4I
8I
6I
14I
12I
18I
16I
22I
20I
26I
24I
30I
28I
Capacitive reactive current demand
Capacitor bank current
32I
Maximum error=I/2
Stepping response
31I
Linear response
I=VwC
31I
(b)
Figure 1. Capacitor bank, (a) configuration, (b) expected reactive current response.
which is then zero-crossing detected, forming the waveform V4. The latter is processed similar to V1, forming V5. These waveforms are shown in Figure 3.
The current signal KiL is sampled by the sample and hold circuit at ωt= nπ, where n is a positive odd integer, yielding an analogue signal proportional directly to the
222 Sci. Res. Essays
VT1
VT3
VT2
VT5
VT4
8-bit ADC
DB5
DB6
DB7
DB2
DB3
DB4
DB0
DB1
CNVRT
INU1A
74A
C08
1 23
U2B
74A
C08
4 56
U3C
74A
C08
9
10
8
U4B
74A
C08
4 56
U4C
74A
C08
9
10
8
Amplifier
C.T
V.T
Driving circuit
Vi
Sample/hold
circuit
Analogue
differentiatorRC differentiator
/rectifier(1)
Zero-crossing
detector(2)
C
1
2
2C
1
2
8C
1
2
4C
1
2
16C
1
2
T1D1
12 T2
D2
12 T3
D3
12 T4
D4
12 T5
D5
12
LS1
1
2
LS2
1
2
LS3
1
2
LS4
1
2
LS5
1
2
R
2
1
L
1
2
N
L
V
Inductive load
RC differentiator
/rectifier(2)
K*v
Capacitor bank triggering circuit
KiL
Capacitor bank
KiL
V1
V2
V3V4
V5
iL
iC
iT
Zero-crossing
detector(1)
Figure 2. The proposed single phase power factor correction system block diagram.
reactive current component of the load current as follows:
sinsin m
nt
mL KItKIKi
(3)
The latter signal is amplified and clamped upward by 0.15625 volts producing the analogue voltage Vi which is proportional to the reactive current demand. Vi is the analogue input of the 8-bit analogue-to-digital converter (8-bit ADC). For unity power factor correction and at full compensator rating, Vi will have a magnitude of 10 volts. The 8-bit ADC starts conversion at ωt = (2n-1)π/2, where n is a positive odd integer. The five most significant digits
(DB7, DB6, DB5, DB4, and DB3) of the 8-bit ADC are employed for controlling the capacitor bank switching devices (T5, T4, T3, T2, and T1) respectively. The instantaneous capacitor bank current iC is determined by the logic status of the 8-bit ADC as follows:
3
5
14
5
25
5
46
5
87
5
16DBDBDBDBDBCVi mC (4)
Where, C is the basic capacitance of the capacitor bank. For DB7, DB6, DB5, DB4, and DB3, logic zero refers to zero volts, while logic one refers to +5 volts. Note that when Vi is zero, all the digital outputs of the 8-bit ADC are
Obais and Pasupuleti 223
2
2
3
2
5
2
7 2 3 40
Time
0s 20ms 40ms
V(U11:OUT)
-4.0V
0V
4.0V
Time
0s 20ms 40ms
V(VS2)
0V
2.5V
5.0V
Time
0s 20ms 40ms
V(D5:2)
-5.0V
0V
5.0V
3V
5V
4V
2
2
3
2
5
2
7 2 3 40
Time
0s 20ms 40ms
V(VS)
-4.0V
0V
4.0V
Time
0s 20ms 40ms
V(VS1)
0V
2.5V
5.0V
Time
0s 20ms 40ms
V(D6:2)
-5.0V
0V
5.0V
vK *
2V
1V
Time t, Time t,
Figure 3. The single-phase basic voltage waveforms.
logic zero. When Vi is 10 volts, all the digital outputs are logic one.
Table 1 shows the capacitor bank switching status as Vi
varies from zero to 10 volts. The driving circuit includes five sub-circuits; each one of them deals with one of the thyristor (T1 to T5). Choosing appropriate switching instants will protect the switching devices from inrush currents. The appropriate switching of thyristor occurs at ωt = (2n+1)π/2, where n is a positive odd integer. At these instants dv/dt is zero and each of the capacitors (C, 2C, 4C, 8C, and 16C) is charged to -Vm through its corresponding diode and limiting reactor. Note that when this compensator is started, each of the above capacitors charges through its individual diode and limiting reactor to -Vm. No inrush current will associate the charging and switching mechanisms.
THE PROPOSED THREE-PHASE POWER FACTOR CORRECTION SYSTEM
The power circuit of three-phase power factor correction system is shown in Figure 4. It is simply composed of
three identical capacitor banks connected in star form. iCA,
iCB, and iCC are the instantaneous compensator
phase currents, while vA, vB, and vC are the power system instantaneous phase voltages. The three phase instantaneous load currents are iLA,
iLB, and iLC, while the
three phase instantaneous line currents are iA, iB, and iC.
Each capacitor bank will respond according to Figure 1b. The block diagram of the proposed three-phase four-
wire power factor correction system is shown in Figure 5. It comprises three identical voltage transformers and three identical current transformers. Here are three identical triggering circuits; each one of them deals with a single capacitor bank. Phase A triggering circuit is excited by the analogue signals KiLA and K*vA, phase B triggering circuit is excited by the analogue signals KiLB and K*vB, and phase C triggering circuit is excited by the analogue signals KiLC and K*vC. If the compensator is operated by a balanced three-phase supply, then the controlling signals can be given by
tVKvK mA sin** (5)
224 Sci. Res. Essays
Table 1. The capacitor bank status as Vi varies from 0 to 10 V.
Vi (Volts) C1 Status C2 Status C3 Status C4 Status C5 Status
0 OFF OFF OFF OFF OFF
0.3125 ON OFF OFF OFF OFF
0.625 OFF ON OFF OFF OFF
0.9375 ON ON OFF OFF OFF
1.25 OFF OFF ON OFF OFF
1.5625 ON OFF ON OFF OFF
1.875 OFF ON ON OFF OFF
2.1875 ON ON ON OFF OFF
2.5 OFF OFF OFF ON OFF
2.8125 ON OFF OFF ON OFF
3.125 OFF ON OFF ON OFF
3.4375 ON ON OFF ON OFF
3.75 OFF OFF ON ON OFF
4.0625 ON OFF ON ON OFF
4.375 OFF ON ON ON OFF
4.6875 ON ON ON ON OFF
5 OFF OFF OFF OFF ON
5.3125 ON OFF OFF OFF ON
5.625 OFF ON OFF OFF ON
5.9375 ON ON OFF OFF ON
6.25 OFF OFF ON OFF ON
6.5625 ON OFF ON OFF ON
6.875 OFF ON ON OFF ON
7.1875 ON ON ON OFF ON
7.5 OFF OFF OFF ON ON
7.8125 ON OFF OFF ON ON
8.125 OFF ON OFF ON ON
8.4375 ON ON OFF ON ON
8.75 OFF OFF ON ON ON
9.0625 ON OFF ON ON ON
9.375 OFF ON ON ON ON
9.6875 ON ON ON ON ON
3/2sin** tVKvK mB (6)
3/4sin** tVKvK mC (7)
AmLALA tKIKi sin (8)
BmLBLB tKIKi 3/2sin (9)
CmLCLC tKIKi 3/4sin (10)
Where ImLA, ImLB, and ImLC are the load phase currents
amplitudes, while φA, φB, and φC are their power factor angles. These three-phase controlling signals are processed in the same manner adopted in the single phase power factor correction system. The capacitor bank of each phase will respond according to the criterion of Table 1.
SYSTEMS CIRCUITS DESIGN The single-phase and three-phase automatic power factor correction systems are designed and implemented using the computer program PSpice. Datasheets of electronic parts and aiding literatures are considered during design process (Rashid, 2001; Bimal, 2006).
Obais and Pasupuleti 225
N
La
1
2
Ra
Lc
1
2
Rc
Lb
1
2
Rb
C
1
2
2C
1
2
8C
1
2
4C
1
2
16C
1
2
T1D1
12 T2
D2
12 T3
D3
12
T4D4
12 T5 D5
12
LS1
1
2
LS2
1
2
LS3
1
2
LS4
1
2
LS5
1
2
2C
1
2
C1
2
8C
1
2
4C
1
2
16C
1
2
T6
D6
1
2
T7
D7
1
2
T8
D8
1
2
T9
D9
1
2
T10
D10
1
2
LS
6 1
2
LS
7 1
2
LS
8 1
2
LS
9 1
2
LS
10 1
2
C
1
2
8C
1
2
2C
1
2
4C
1
2
16C 1
2
T11
D11
1
2
T12
D12
1
2
T13
D13
1
2
T14
D14
1
2
T15
D15
1
2
LS
11
1
2
LS
12
1
2
LS
13
1
2
LS
14
1
2
LS
15
1
2
N
Ai
Bi
Ci
Av
Bv
Cv
N
CAiLBi
CCi LAi LCiCBi
Three phase loadCompensator power circuit
Figure 4. The power circuit of the three-phase power factor correction system.
Figures 6 and 7 show the circuit diagrams of the single-phase and the three-phase automatic power factor correction systems respectively. The simulation results will be extracted from running these systems on PSpice. RESULTS The basic capacitance C was chosen to be 50 µF for both single-phase and three-phase systems. The power system network has a frequency of 50 Hz and a phase voltage of 240 volts (r.m.s value). Consequently, the single-phase reactive current rating is 165 A (peak value). Figure 8 shows PSpice tests for the single-phase system.
The first test corresponds to the case at which the load
impedance (ZL) was o3725.1 . The power factor for
this load is 0.8 lagging. The reactive component of the load current was 163A (peak value) which was within the compensator rating. Consequently the compensator generated a capacitive reactive current completely cancelled the load current reactive component yielding a real total current (iT) as shown in Figure 8a. The second
test corresponds to an inductive load of o5325.1 .
The reactive component for that load was 217.6A (peak value) which exceeded the system rating by 52.6A (peak value). Therefore the power factor for that load was only improved as shown in Figure 8b. Figure 9 shows tests corresponding to the three-phase system. DISCUSSION Figure 9a concerns a balanced three-phase inductive
226 Sci. Res. Essays
RC
differentiator
/rectifier(1)
iCB
iCC
Phase A capacitor bank
Three phase load
iCA
C.T
VGT3
VGT2
VGT1
VGT5
VGT4
RC
differentiator
/rectifier(1)
Phase B capacitor bank
VGT8
VGT9
VGT10
VGT6
VGT7
KiLC
KiLB
KiLA
VT9
VT10
VT7
VT8
VT6
D6
D7
8-bit ADC
D3
D4
D5
D1
D2
CNVRT
IN
D0
U5D
74AC0812
1311
U6B
74AC084
56
U6C
74AC089
108
U7B
74AC084
56
U7C
74AC089
108
Amplifier
Phase B driving circuit
Sample/hold
circuit
Analogue
differentiator
Zero-crossing
detector(2)
RC
differentiator
/rectifier(2)
Phase B triggering circuit
Zero-crossing
detector(1)
K*VA
ViB
ViA
K*VC
K*VB
ViC
VB
VA
V.T
N
VC
V1A
RC
differentiator
/rectifier(1)
Phase C capacitor bank
C.T
VGT15
VGT12
VGT13
VGT14
VGT11
V.T
VT15
VT13
VT14
VT11
VT12
8-bit ADC
D5
D6
D7
D2
D3
D4
D0
D1
CNVRT
IN
U7D
74AC0812
1311
V1B
U8B
74AC084
56
U8C
74AC089
108
U9B
74AC084
56
U9C
74AC089
108
Amplifier
Phase C driving circuit
Sample/hold
circuit
Analogue
differentiator
VT1
Zero-crossing
detector(2)
VT3
VT2
VT4
8-bit ADC
VT5
V1C
Phase C triggering circuit
RC
differentiator
/rectifier(2)
D5
D6
D7
D3
D4
Zero-crossing
detector(1)
D0
D1
D2
CNVRT
IN
U1A
74AC081
23
U2B
74AC084
56
U3C
74AC089
108
U4B
74AC084
56
U5C
74AC089
108
Amplifier
V.T
Phase A driving circuit
Sample/hold
circuit
Analogue
differentiator
Zero-crossing
detector(2)
V2C
V2B
V2A
V3C
V3B
V3AV4A
RC
differentiator
/rectifier(2)
Phase A triggering circuit
Zero-crossing
detector(1)
V4C
V4B
V5B
V5A
V5C
iA
iB
iC
C.T
iLB
iLA
iLC
Figure 5. The proposed three-phase power factor correction system scheme.
Figure 6. The circuit diagram of the single-phase power factor correction system.
load operating at a 0.8 lagging power factor and exhibiting balanced reactive current components of 163A (peak value). The compensator corrected the power factor to unity for the three-phase load, since the reactive current demands were within its rating. Figure 9b concerns a balanced three-phase inductive load exhibiting balanced reactive current components exceeding the compensator rating, therefore the system was not capable to completely cancel the three-phase reactive current components, but certainly had improved the power factor. Figure 9c shows the response of the
three-phase system to a three-phase load balanced in magnitude, but unbalanced in phase. Finally, the compensator was completely relaxed while it was dealing with a balanced three-phase real load as shown in Figure 9d. Conclusion The proposed single-phase and three-phase automatic power factor correction systems have certain reactive
228 Sci. Res. Essays
U2
0
OP
-18
4/A
D
+3
-2
V+
7
V-
4
OU
T6
0
VG
T3
VG
T4
C1
100n
12
D8
BA
W6
2
R3
2220
21
0
T3
50RIA120
KiC
C4
12nF
1 2V1C
Analogue differentiator
Zero-crossing detector(2)
V2C
R1
0470
21
R2
2k
21
T11 driving circuit
RC differentiator(1)
ViC
RC differentiator(2)
0
0
Amplifier
0
VG
T2
R1
63
1k
21
T12 driving circuit
0
0 R6
50
21
VT
12
VG
T4
DT
1
HFA25TB60
3 1
Zero-crossing detector(1)
+5V
U7
9
A4
N4
7A
-5V
+10V
DT
2
HFA25TB60
3 1
C1
1
1u
12
DT
3
HFA25TB60
3 1
0R
11
1
220
21
R2
22k
21
U6
4A
74
AC
T0
8
123
R1
26
5k
21
DT
4
HFA25TB60
3 1
V4B
DT
5
HFA25TB60
3 1
R1
41
22k
21
0
0
V5B
U1
1B
74
AC
T0
4
34
U4
9B
74
AC
T0
8
456
D3
BA
W6
2
R1
56
4.7
k
21
0
R2
46
.2k
21
Q12
Q2
N3
90
4
U4
8
AD
C8
bre
ak
DB
716
DB
615
DB
514
DB
413
DB
312
DB
211
DB
110
DB
09
AGND8
IN1
CN
VR
T2
STA
T3
OV
ER
4
RE
F5
+10V
R3
5
10k
21
Binary thyristor switched-capacitor bank
0
-10V
+5V
R5
1k
21
Q27Q
2N
22
22
A
U1
9
OP
-18
4/A
D
+3
-2
V+
7
V-
4
OU
T6
U1
AS
D5
00
0
IN4
OU
T1
VC
3
SUB2
R1
71
1k
21
iB
KiB
U1
5A
D8
04
2a
/AD
+3
-2
V+
7
V-
4
OU
T6
iLB
V2B
V1B
+10V
VG
T12
Analogue differentiator
Zero-crossing detector(2)
ViB
T6 driving circuit
VT
11
iCB
RC differentiator(1)
+10V
U7
8
A4
N4
7A
RC differentiator(2)
-10V
U6
LT1
11
2/L
T+
3
-2
V+
8
V-
4
OU
T1
Amplifier
0
T7 driving circuit
0
U2
4A
74
AC
T0
41
2
R1
10
220
21R
12
55k
21
Phase B power circuit
VT
7
VG
T1
V4A
U7
4
A4
N4
7A
R1
40
22k
21
0
R1
55
4.7
k
21
C1
6
100n
1 2
0R
10
6
220
21
R5
6560
21
Q11
Q2
N3
90
4
R1
21
5k
21
0
R1
36
22k
21
+5V
0
Q26Q
2N
22
22
A
C2
5
100n
1 2
D2
BA
W6
2
R8
8560
21
R1
51
4.7
k
21
R1
70
1k
21
0
Q7
Q2
N3
90
4
R7
65k
21
U6
1A
D8
04
2a
/AD
+3
-2
V+
7
V-
4
OU
T6
0
T13 driving circuit
0
R7
75k
21
VT
13
Q22Q
2N
22
22
A
U8
0
A4
N4
7A
V5A
0
0
R1
66
1k
21
0
+5V
C1
3
100n
1 2
R1
12
220
21
VG
T7
R4
2560
21
R1
27
5k
21
R5
32k
21
+10V
0
R1
42
22k
21
VT
6
U2
7
AD
80
42
a/A
D
+3
-2
V+
7
V-
4
OU
T6
R1
57
2k
21
VT
5
U7
3
A4
N4
7A
+5V
U2
9A
74
AC
T0
81 2
3
Q13
Q2
N3
90
4
0
-5V
0R
10
5
220
21
+10V
U2
8A
D8
04
2a
/AD
+3
-2
V+
7
V-
4
OU
T6
R7
22k
21
R6
72k
21
R1
20
5k
21
Q28Q
2N
22
22
A
-10V
U4
3
OP
-18
4/A
D
+3
-2
V+
7
V-
4
OU
T6
U3
6A
D8
04
2a
/AD
+3
-2
V+
7
V-
4
OU
T6
R1
35
22k
21
R1
50
4.7
k
21
R1
72
1k
21
Q6
Q2
N3
90
4
Phase C triggering circuit
0 R4
41k
21
+10V
+10V
VG
T13
R3
982k
21
U3
4
AD
80
42
a/A
D
+3
-2
V+
7
V-
4
OU
T6
K*vA
R5
4128k
21
Q21Q
2N
22
22
A
-5V
+5V
0
0
U4
4
AD
80
42
a/A
D
+3
-2
V+
7
V-
4
OU
T6
R6
22k
21
R1
65
1k
21
-5V
+5V
0
U5
2
AD
80
42
a/A
D
+3
-2
V+
7
V-
4
OU
T6
+5V
T8 driving circuit
-5V
VT
8
U6
0
AD
80
42
a/A
D
+3
-2
V+
7
V-
4
OU
T6
U7
5
A4
N4
7A
+5V
0R
10
7
220
21
-5V
U6
7
AD
80
42
a/A
D
+3
-2
V+
7
V-
4
OU
T6
R1
22
5k
21
-5V
+5V
R1
37
22k
21
S
V5
Implementation = vA
0
R4
85k
21
R1
52
2k
21
Q8
Q2
N3
90
4
0
+10V
R6
35k
21
Q23Q
2N
22
22
A
0
T14 driving circuit
LS
15
20uF
1 2
R1
67
1k
21
VG
T8
+10V
VT
14
U3
3
AD
80
42
a/A
D
+3
-2
V+
7
V-
4
OU
T6
C42
800u
F
12
+5V
VG
T15
-5V
U4
2
AD
80
42
a/A
D
+3
-2
V+
7
V-
4
OU
T6
U8
1
A4
N4
7A
+5V
-5V
U5
1
AD
80
42
a/A
D
+3
-2
V+
7
V-
4
OU
T6
-5V
+5V
U5
9
AD
80
42
a/A
D
+3
-2
V+
7
V-
4
OU
T6
0
T9
2N1804
+5V
-5V
U6
6
AD
80
42
a/A
D
+3
-2
V+
7
V-
4
OU
T6
K*vC
R1
13
220
21
+5V
0
-5V
R4
75k
21
0
R1
28
5k
21
+10V
0
U4
9A
74
AC
T0
8
123
R6
15k
21
R1
72k
21
0
T9 driving circuitL
S10
20uF
1 2
LS
11
5uF
1 2
R1
43
22k
21
R1
58
1k
21
VT
9
C38
50u
F
12
C37
800u
F
12
+10V
VG
T10
U7
6
A4
N4
7A
T11
CS19-12
I
Q14
Q2
N3
90
4
VG
T11
LS
12
5uF
1 2
R1
88k
21 -1
0V
0
LS
13
10uF
1 2
U4
0B
74
AC
T0
84 5
6
K*vB
LS
14
20uF
1 2
R1
08
220
21
C39
100u
F
12
0
R1
23
5k
21
C40
200u
F
12
U4
0D
74
AC
T0
8
13
12
11
VT
14
VT
13
R1
52k
21
C41
400u
F
12
U4
LT1
11
2/L
T
+3
-2
V+
8
V-
4
OU
T1
LS
6
5uF
1 2
VT
12
VT
11
R1
38
22k
21
Q29Q
2N
22
22
A
R1
53
1k
21
T12
CS19-12
C33
50u
F
12
+10V
T6
CS19-12
Q9
Q2
N3
90
4
VG
T6
LS
7
5uF
1 2
R1
68k
21 -1
0V
LS
8
10uF
1 2
U4
0A
74
AC
T0
81 2
3
LS
9
20uF
1 2
C34
100u
F
12
C35
200u
F
12
VT
8
VT
9
S
V6
Implementation = vB
C36
400u
F
12
U3
LT1
11
2/L
T
+3
-2
V+
8
V-
4
OU
T1
VT
6
VT
7
Q24Q
2N
22
22
A
T7
CS19-12
iA
T10
2N1804
Phase C driving circuit
Phase C power circuit
S
V7
Implementation = vC
iLC
iC
iCC
iLA
+5V
U1
1D
74
AC
T0
4
98
RV
T4
2k
21
RV
T1
99k
21
0
R9
4
1.8
k
21
R9
5200
21
0
0
0
+5V
C1
9
100n
1 2
0
R6
9560
21
R7
35k
21
U4
5A
D8
04
2a
/AD
+3
-2
V+
7
V-
4
OU
T6
00
0
+5V
C2
2
100n
1 2
R7
8560
21
U5
5A
D8
04
2a
/AD
+3
-2
V+
7
V-
4
OU
T6
0
0
U2
1
AD
80
42
a/A
D
+3
-2
V+
7
V-
4
OU
T6
-5V
+5V
Sample/Hold circuit
U1
2
AD
80
42
a/A
D
+3
-2
V+
7
V-
4
OU
T6
+5V
-5V
0
R8
15k
21
Load impedance
DB7A
DB4A
DB5A
DB6A
DB3A
Logic circuit
Output circuit
8-bit ADC
Pricision comparators
Voltage transformer
Current transformer
AC supply
KiA
RC
T1
0.0
1
21
LA
1
2.3
65
mH
1 2
RA
1
1
21
Phase A triggering circuit
T14
2N1804
D4
BA
W6
2
0
U5
AD
80
42
a/A
D
+3
-2
V+
7
V-
4
OU
T6
-5V
+5V
Phase B triggering circuit
0
R9
15k
21
0
T5 driving circuit
VT
5
U7
2
A4
N4
7A
T4
2N1804
0R
10
4
220
21R
11
95k
21
R1
34
22k
21
V3A
R1
49
1k
21
Q5
Q2
N3
90
4
R5
22k
210
VG
T13
VG
T14
Q20Q
2N
22
22
A
C5
100n
12
U2
6
AD
80
42
a/A
D
+3
-2
V+
7
V-
4
OU
T6
0
T13
50RIA120
+5V
R1
64
1k
21
0
-5V
+10V
R6
82k
21
R1
2470
21
+10V
VG
T5
R6
62k
21-1
0V
0
R2
0
1k
21
U3
9
OP
-18
4/A
D
+3
-2
V+
7
V-
4
OU
T6
R1
73
1k
21
VG
T12
C7
500n
12
R2
8150
21
0 R4
11k
21
VG
T14
DT
11
HFA25TB60
3 1
R3
882k
21
+10V
0
0
D7
BA
W6
2
DT
12
HFA25TB60
3 1
DT
13
HFA25TB60
3 1
R5
1128k
21
R3
1220
21
0
C2
12nF
1 2
U6
4C
74
AC
T0
8
109
8
R5
72k
21
R1
2k
21
DT
14
HFA25TB60
3 1
DT
15
HFA25TB60
3 1
U4
9D
74
AC
T0
8
13
12
11
0
0
00
U5
4A
DC
8b
rea
k
DB
716
DB
615
DB
514
DB
413
DB
312
DB
211
DB
110
DB
09
AGND8
IN1
CN
VR
T2
STA
T3
OV
ER
4
RE
F5
R4
50
21
Zero-crossing detector(1)
+5V
0
-5V
+5V
R9
1k
21
VG
T9
C3
100n
12
VG
T8
C1
0
1u
12
U1
CS
D5
00
0
IN12
OU
T9
VC
11
SUB2
R1
92k
21
0
T8
50RIA120
V4A
U1
7A
D8
04
2a
/AD
+3
-2
V+
7
V-
4
OU
T6
V5A
R1
1470
21
0
U1
1A
74
AC
T0
4
12
-10V
+10V
0
R2
16
.2k
21
VG
T7
U1
0L
T1
11
2/L
T+
3
-2
V+
8
V-
4
OU
T1
R1
68
1k
21
+10V
Binary thyristor switched-capacitor bank
R3
4
10k
21
U2
4C
74
AC
T0
45
6
-10V
VG
T11
VG
T9
DT
6
HFA25TB60
3 1
0
+10V
V4C
DT
7
HFA25TB60
3 1
U1
8
OP
-18
4/A
D
+3
-2
V+
7
V-
4
OU
T6
DT
8
HFA25TB60
3 1
C1
8
100n
1 2
U6
4B
74
AC
T0
8
456
KiA
R5
9560
21
V1A
DT
9
HFA25TB60
3 1
Zero-crossing detector(2)
V2A
0
DT
10
HFA25TB60
3 1
T1 driving circuit
Analogue differentiator
+5V
C2
7
100n
1 2
RC differentiator(1)
ViA
R9
0560
21
U4
9C
74
AC
T0
8
109
8
Phase A driving circuit
RC differentiator(2)
Amplifier
0
R8
65k
21
T2 driving circuit
0
U5
3 AD
C8
bre
ak
DB
716
DB
615
DB
514
DB
413
DB
312
DB
211
DB
110
DB
09
AGND8
IN1
CN
VR
T2
STA
T3
OV
ER
4
RE
F5
U6
3A
D8
04
2a
/AD
+3
-2
V+
7
V-
4
OU
T6
VT
2
Phase A power circuit
0
R8
75k
21
U6
9
A4
N4
7A
+5V
0
R7
1k
21
0
0
V5C
R1
01
220
21
U1
BS
D5
00
0
IN5
OU
T8
VC
6
SUB2
+5V
0
C1
5
100n
1 2
R1
16
5k
21
U1
6A
D8
04
2a
/AD
+3
-2
V+
7
V-
4
OU
T6
R1
31
22k
21
R4
5560
21
0
D1
BA
W6
2
+10V
R1
46
4.7
k
21
-10V
VT
15
U8
LT1
11
2/L
T+
3
-2
V+
8
V-
4
OU
T1
U2
9C
74
AC
T0
810 9
8
Q2
Q2
N3
90
4
U2
4B
74
AC
T0
43
4
U3
1A
D8
04
2a
/AD
+3
-2
V+
7
V-
4
OU
T6
VG
T6
V4B
U3
8A
D8
04
2a
/AD
+3
-2
V+
7
V-
4
OU
T6
Q17Q
2N
22
22
A
0
C1
7
100n
1 2
R1
61
1k
21
R5
8560
21
+10V
+10V
VG
T2
+5V
0
K*vC
VT
1
C2
6
100n
1 2
0R
89
560
21
T5
2N1804
U6
8
A4
N4
7A
0
R8
45k
21
0R
10
0
220
21
U6
2A
D8
04
2a
/AD
+3
-2
V+
7
V-
4
OU
T6
R1
15
5k
21
0
R1
30
22k
21
R8
55k
21
R1
45
4.7
k
21
+5V
V5B
0
0
Q1
Q2
N3
90
4
U1
1F
74
AC
T0
4
13
12
+5V
C1
4
100n
1 2
RV
T6
2k
21
R4
3560
21
0
RV
T3
99k
21
Q16Q
2N
22
22
A
R9
8
1.8
k
21
VT
10
R9
9200
21
R1
60
1k
21
U2
9B
74
AC
T0
84 5
6
0
U3
0A
D8
04
2a
/AD
+3
-2
V+
7
V-
4
OU
T6
0
T3 driving circuit
0
0
VT
3
U7
0
A4
N4
7A
U3
7A
D8
04
2a
/AD
+3
-2
V+
7
V-
4
OU
T6
0
+5V
C2
1
100n
1 2
R7
1560
21
0R
10
2
220
21
+10V
R1
17
5k
21
R7
55k
21
K*vB
U4
7A
D8
04
2a
/AD
+3
-2
V+
7
V-
4
OU
T6
R1
32
22k
21
0
R1
47
2k
21
0
Q3
Q2
N3
90
4
0
0
+5V
C2
4
100n
1 2
R8
0560
21
Q18Q
2N
22
22
A
+5V
U5
7A
D8
04
2a
/AD
+3
-2
V+
7
V-
4
OU
T6
R1
62
1k
21
U1
1E
74
AC
T0
4
11
10
0
+10V
VG
T3
RV
T5
2k
21
0
U3
2
AD
80
42
a/A
D
+3
-2
V+
7
V-
4
OU
T6
0
RV
T2
99k
21
U2
3
AD
80
42
a/A
D
+3
-2
V+
7
V-
4
OU
T6
-5V
+5V
R9
6
1.8
k
21
-5V
+5V
U4
1
AD
80
42
a/A
D
+3
-2
V+
7
V-
4
OU
T6
R9
7200
21
Sample/Hold circuit
-5V
+5V
U1
4
AD
80
42
a/A
D
+3
-2
V+
7
V-
4
OU
T6
U5
0
AD
80
42
a/A
D
+3
-2
V+
7
V-
4
OU
T6
+5V
-5V
0
+5V
0
0
0
-5V
R8
35k
21
+5V
0
-10VV
4
10V
0
C2
0
100n
1 2
iCA
Load impedance
0 V1
10V
R7
0560
21
DB7C
DB4C
DB5C
DB6C
+10V
V2
5V
R7
45k
21
DB3C
0
+5V
U4
6A
D8
04
2a
/AD
+3
-2
V+
7
V-
4
OU
T6
Logic circuit
-5V
0
Output circuit
V3
5V
8-bit ADC
Pricision comparators
0
Voltage transformer
0
U5
8
AD
80
42
a/A
D
+3
-2
V+
7
V-
4
OU
T6
Current transformer
AC supply
+5V
0
KiC
RC
T3
0.0
1
21
C2
3
100n
1 2
+5V
R7
9560
21
-5V
LC
1
2.3
65
mH
1 2
U6
5
AD
80
42
a/A
D
+3
-2
V+
7
V-
4
OU
T6
U5
6A
D8
04
2a
/AD
+3
-2
V+
7
V-
4
OU
T6
RC
1
1
21
+5V
0
-5V
R4
65k
21
Phase B driving circuit
0
D6
BA
W6
2
0
+10V
U2
2
AD
80
42
a/A
D
+3
-2
V+
7
V-
4
OU
T6
0
R6
05k
21
0
+5V
U9
AD
80
42
a/A
D
+3
-2
V+
7
V-
4
OU
T6
R4
92k
21
-5V
Sample/Hold circuit
0
T4 driving circuit
0
-5V
+5V
U1
3
AD
80
42
a/A
D
+3
-2
V+
7
V-
4
OU
T6
LS
5
20uF
1 2
U2
5
AD
80
42
a/A
D
+3
-2
V+
7
V-
4
OU
T6
0
+5V
+5V
T15
2N1804
R9
35k
21
0
-5V
-5V
VT
4
+10V
0
0
R8
25k
21
C32
800u
F
12
R6
52k
21
R6
42k
21
T15 driving circuit
VG
T5
U7
1
A4
N4
7A
Load impedance
-10V
VT
15
U8
2
A4
N4
7A
DB6B
DB7B
U3
5
OP
-18
4/A
D
+3
-2
V+
7
V-
4
OU
T6
DB4B
DB5B
DB3B
0 R4
01k
21
0R
11
4
220
21
R3
782k
21
Logic circuit
R1
29
5k
21
Output circuit
R5
0128k
21
8-bit ADC
Pricision comparators
R1
44
22k
21
Voltage transformer
0
KiB
V3C
Current transformer
AC supply
0
R1
59
1k
21
RC
T2
0.0
1
21
R5
52k
21
Q15
Q2
N3
90
4
LB
1
2.3
65
mH
1 2
K*vA
RB
1
1
21
R1
03
220
21
Q30Q
2N
22
22
A
0
R1
18
5k
21
D5
BA
W6
2
U4
0C
74
AC
T0
8
109
8
R1
74
1k
21
0
U7
AD
80
42
a/A
D
+3
-2
V+
7
V-
4
OU
T6
R1
32k
21
+10V
VG
T15
+5V
LS
1
5uF
1 2
0
-5V
R2
6
1k
21
0
R9
25k
21
R1
33
22k
21
C9
500n
12
R1
48
1k
21
R3
0150
21
C28
50u
F
12
0
0
0
+10V
D9
BA
W6
2
T1
CS19-12
T10 driving circuit
VT
10
Q4
Q2
N3
90
4
R3
3220
21
U7
7
A4
N4
7A
C6
12nF
1 2
VG
T1
LS
2
5uF
1 2
0
R3
2k
21
R1
09
220
21
R1
48k
21
R1
24
5k
21
0
R1
39
22k
21
0
0-1
0V
LS
3
10uF
1 2
Fig. 7 The circuit diagram of the three-phase automatic power factor correction system.
0 R8
50
21
R1
54
1k
21
V3B
U2
9D
74
AC
T0
813
12
11
Q10
Q2
N3
90
4
Zero-crossing detector(1)
LS
4
20uF
1 2
-5V
+5V
C1
2
1u
12
Q25Q
2N
22
22
A
C29
100u
F
12
C30
200u
F
12
R2
52k
21
R1
69
1k
21
V4C
VT
3
0
V5C
VT
4
C31
400u
F
12
VG
T10
U1
1C
74
AC
T0
4
56
+10V
U2
LT1
11
2/L
T
+3
-2
V+
8
V-
4
OU
T1
0
0
R2
76
.2k
21
R2
3
1k
21
VT
1
VT
2
+10V
C8
500n
12
Q19Q
2N
22
22
A
Binary thyristor switched-capacitor bank
R3
6
10k
21
R2
9150
21
T2
CS19-12
-10V
0
Figure 7. The circuit diagram of the three-phase power factor correction system.
Obais and Pasupuleti 229
(a)
Time
20ms 30ms 40ms 50ms 60ms
V(C1:1) -I(v5) -I(R) -I(RVT5)
-400
0
400
iC
iLiT
v o
LZ 3725.1
v (
Volt t
), i
L,
i C,
i T(A
mp
.)
Time(b)
Time
20ms 30ms 40ms 50ms 60ms
V(C1:1) -I(v5) -I(R) -I(RVT5)
-400
0
400
iC
iL
iT
v
v (
Volt t
), i
L,
i C,
i T(A
mp
.) o
LZ 5325.1
Time
Figure 8. (a) Unity power factor correction, (b) power factor improvement.
Av Bv Cv
LAiLBi LCi
CAiCBi CCi
AiBi
Ci
a Time
Time
20ms 30ms 40ms 50ms
V(V11:PVS) V(LB1:2) V(C41:1)
-400V
0V
400V
Time
20ms 30ms 40ms 50ms
-I(LB1) -I(LA1) -I(LC1)
-400A
0A
400A
Time
20ms 30ms 40ms 50ms
-I(R175) -I(R176) -I(R177)
-200A
0A
200A
Time
20ms 30ms 40ms 50ms
I(R179) I(R178) I(R180)
-400A
0A
400A
voltagesphase ac
currentsline Load
currents
rCompensato
currents linesupply ac
Av Bv Cv
LAiLBi
LCi
CAiCBi CCi
Ai Bi Ci
b Time
Time
20ms 30ms 40ms 50ms
V(R178:2) V(R179:2) V(C41:1)
-400V
0V
400V
Time
20ms 30ms 40ms 50ms
-I(R177) -I(R176) -I(R175)
-200A
0A
200A
Time
20ms 30ms 40ms 50ms
-I(LA1) -I(LB1) -I(LC1)
-400A
0A
400A
Time
20ms 30ms 40ms 50ms
I(R179) I(R178) I(R180)
-200A
0A
200A
voltagesphase ac
currentsline Load
currentsrCompensato
currents linesupply ac
Av BvCv
LAiLBi
LCi
CAiCBi CCi
Ai Bi Ci
c Time
voltagesphase ac
currentsline Load
currents
rCompensato
currents linesupply ac
Time
20ms 30ms 40ms 50ms
V(R178:2) V(R179:2) V(C41:1)
-400V
0V
400V
Time
20ms 30ms 40ms 50ms
-I(LC1) -I(LB1) -I(LA1)
-400A
0A
400A
Time
20ms 30ms 40ms 50ms
-I(R175) -I(R176) -I(R177)
-200A
0A
200A
Time
20ms 30ms 40ms 50ms
I(R178) I(R179) I(R180)
-400A
0A
400A
Av BvCv
LAi LBiLCi
CAiCBi
CCi
AiBi
Ci
d Time
voltagesphase ac
currentsline Load
currentsrCompensato
currents linesupply ac
Time
20ms 30ms 40ms 50ms
V(LA1:2) V(C33:1) V(RVT3:2)
-400V
0V
400V
Time
20ms 30ms 40ms 50ms
-I(LA1) -I(LB1) -I(LC1)
-400A
0A
400A
Time
20ms 30ms 40ms 50ms
-I(R176) -I(R175) -I(R177)
-400A
-200A
0A
200A
400A
Time
20ms 30ms 40ms 50ms
I(R178) I(R180) I(R179)
-400A
0A
400A
Figure 9. Performance of the three-phase compensator during (a) a balanced full load
of 0.8 lagging power factor, (b) a balanced full load of 0.6 lagging power factor, (c) a full load balanced in magnitude and unbalanced in phase, (d) a balanced full resistive load.
230 Sci. Res. Essays current or reactive power ratings. When the detected reactive power absorbed by the load is greater than the compensator rating, the power factor will not be corrected to unity, but certainly will be improved and the apparent power supplied by the ac supply will be reduced. These systems respond almost linearly throughout their pre-assigned areas of operation. They achieve better power quality by reducing the apparent power drawn from the ac supply and minimizing the power transmission losses. In addition, no harmonics disturbing the power system network are released, and hence no filtering is required. The responses of both systems are settled down within the power system network fundamental cycle. There is a feasibility of utilizing this technique for designing systems with high voltage and current ratings. Since this technique is not dealt with accomplishing balanced three-phase currents, the future work will be extended to design an integrated system capable of achieving both power factor correction and load balancing. REFERENCES Best RA, La Parra HZ (1996). Transient response of a static Var shunt
compensator. IEEE t Power Elect., 11(3): 489-494. Bimal KB (2006). Power electronics and motor drives. Elsevier Inc. Chen JH, Lee WJ, Chen MS (1999). Using a static Var compensator to
balance a distribution system. IEEE Ind. Appl., 35(2): 298-304. Dai D, Li S, Ma X, Tse CK (2007). Slow-scale instability of single-stage
power-factor correction power supplies. IEEE T Circuits Syst., 54(8):
1724-1735.
Gyugy L, Otto RA, Putman TH (1978). Principles and applications of
static, thyristor-controlled shunt compensators. IEEE t Power Appl. Syst., PAS-97: 1935-1945.
Idris RM, Khairuddin A, Mustafa MW, Kalam A (2010). Optimal allocation of multi-type FACTS devices using Bees Algorithm for ATC enhancement in deregulated power system, int. rev. Elect. Eng., 5(2):
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balancing for unbalanced three-phase four wire system by a
combined system of an SVC and a series active filter. IEE p-Elect Pow Appl., 147(6): 563-571.
Lupin JM, Chenevard L, Peronnet J (2007). Energy efficiency
improvement through optimization of the power factor correction. In: Proceed. 19
th Int. Conf. Elect. Distr. Held Vienna, pp. 1-4.
Mehrdad M (2005). Saving through power quality. In: Proceeding of the
Twenty-Seventh Industrial Energy Technology Conference held at New Orleans, pp. 1-6.
Miller TJ (1982). Reactive power Control in Electric Systems. John Willey
& Sons. Nandi S, Biswas P, Nandakumar V, Hegde R (1997). Two novel
schemes suitable for static switching of three-phase delta-connected
capacitor banks with minimum surge current. IEEE t Ind. Appl., 33(5): 1348-1354.
Rashid M (2001). Power electronics handbook. Academic Press.
Stahlkopf KE, Wilhelm MR (1997). Tighter controls for busier systems. IEEE Spectrum., 34(4): 48-52.