direct integration of battery energy storage systems in distributed power generation
TRANSCRIPT
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IEEE TRANSACTIONS ON ENERGY CONVERSION, VOL. 26, NO. 2, JUNE 2011 677
Direct Integration of Battery Energy Storage Systemsin Distributed Power Generation
S. D. Gamini Jayasinghe, Student Member, IEEE, D. Mahinda Vilathgamuwa, Senior Member, IEEE,and Udaya K. Madawala, Senior Member, IEEE
AbstractIn this paper, a wind energy conversion system inter-faced to the grid using a dual inverter is proposed. One of the twoinverters in the dual inverter is connected to the rectified outputof the wind generator while the other is directly connected to abattery energy storage system (BESS). This approach eliminatesthe need for an additional dcdc converter and thus reduces powerlosses, cost, and complexity. The main issue with this scheme isuncorrelated dynamic changes in dc-link voltages that results inunevenly distributed space vectors. A detailed analysis on the ef-fects of these variations is presented in this paper. Furthermore,a modified modulation technique is proposed to produce undis-torted currents even in the presence of unevenly distributed anddynamically changing space vectors. An analysis on the batterycharging/discharging process and maximum power point track-ing of the wind turbine generator is also presented. Simulationand experimental results are presented to verify the efficacy of theproposed modulation technique and battery charging/dischargingprocess.
Index TermsDual inverter, energy storage, non-integer voltageratio, wind energy.
I. INTRODUCTION
WITH the depletion of existing fossil fuel deposits, re-
newable resources such as solar, wind, and biomass
are emerging as alternative energy sources. However, the prob-
abilistic nature of these sources makes their grid integrationand reliability improvement difficult. Recently, microgrids have
been proposed to overcome this difficulty [1]. In order to make
such systems dispatchable, renewable sources should supply the
demand, at least for a limited period, irrespective of the fluc-
tuations present in the primary source. Certain fluctuations can
also be expected in the power demand. These fluctuations, irre-
spective of the origin, are the main reasons for instability and
instantaneous power imbalance of microgrids [2], [3]. The most
practical and effective manner in which these fluctuations can
be suppressed is by using an energy storage system [4][6].
Among all feasible energy storage technologies, battery sys-
tems can be regarded as the most developed and widely usedenergy storage device [7], [8]. The other technologies such as
Manuscript received August 19, 2010; revised November 30, 2010; acceptedJanuary 17, 2011. Date of publication April 7, 2011; date of current versionMay 18, 2011. Paper no. TEC-00314-2010.
S. D. G. Jayasinghe and D. M. Vilathgamuwa are with the School of Electri-cal and Electronic Engineering, Nanyang Technological University, Singapore639798 (e-mail: [email protected]; [email protected]).
U. K. Madawala is with the Department of Electrical and computer En-gineering, University of Auckland, Auckland 1142, New Zealand (e-mail:[email protected]).
Color versions of one or more of the figures in this paper are available onlineat http://ieeexplore.ieee.org.
Digital Object Identifier 10.1109/TEC.2011.2122262
flywheels, superconducting magnetic energy storage, and super-
capacitors are still in the development stage and require further
investigations [9], [10]. As a result, power quality enhancement
using battery energy storage systems (BESS) is actively pur-
sued in the field of distributed generation as evident from the
literature [11][21].
When it comes to system integration, the simplest way of
adding a BESS is the direct connection to the dc link of the grid-
side inverter [11][14]. Even though this connection is simple,
it suffers from several drawbacks such as uncontrolled voltage,
fixed current distribution governed by the internal resistance of
the battery bank, and lack of control over the power flow. Effects
of these issues can somewhat be reduced if an intermediate dc
dc converter is placed between the battery and the dc link. This
interfacing dcdc converter increases the system cost and power
losses. In addition to that, the low-pass filter, comprising of an
inductor and a capacitor, degrades the dynamic response. A 3-
level bidirectional dcdc converter has been proposed in [15] to
reduce voltage stresses on switching devices and to improve the
dynamic response with a reduced filter inductance. But it needs
four switches and a flying capacitor. Therefore, the interfacing
dcdc converter increases the system cost, power losses, and
complexity, even if an optimized design is used.A direct integration method, which is free from the aforemen-
tioned drawbacks and beneficial to both industry and academia,
is yet to be reported. This paper, therefore, presents a new direct
integration scheme for BESS with the use of grid-side inverter.
It utilizes the popular dual inverter topology, as shown in Fig. 1,
where two 2-level inverters are cascaded through a coupling
transformer. The two inverters are named as the main inverter
and the auxiliary inverter in line with their modes of opera-
tion. A battery bank is directly connected to the dc link of the
auxiliary inverter without an interfacing dcdc converter. Un-
like in the aforementioned simple direct connection topology,
the proposed system facilitates full controllability over charg-ing/discharging currents and voltage of the battery.
The main inverter operates at the fundamental frequency pro-
ducing square wave outputs. Harmonics of the square wave out-
put are compensated by the high-speed auxiliary inverter. This
particular frequency splitting arrangement can reduce switch-
ing losses as well as device ratings of the main inverter [34],
[35]. Another advantage of the proposed system is its ability to
produce up to 13 voltage levels in the phase voltage waveform
whereas the traditional 2-level inverter can produce only five
levels.
Redundancy and fault tolerance operation can be seen as
additional features of the proposed system where the faulty
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Fig. 1. Proposed grid-side inverter with a BESS interface.
inverter can simply be disconnected by short circuiting corre-
sponding terminals of the transformer. In such situations, the
healthy inverter continues to be operational, but with less volt-
age levels [33]. Moreover, the 2-level inverter technology is wellmatured and standard modules are readily available in the mar-
ket. Therefore, the proposed system can easily be implemented
using off-the-shelf components.
In the proposed controller, charging/discharging currents of
the battery bank are controlled through the main inverter dc-
link voltage and as such it varies with the available wind power.
Furthermore, the auxiliary inverter dc-link voltage varies with
the state of charge (SoC) of the battery bank. The end result
of these uncorrelated variations is a noninteger dynamically
changing dc-link voltage ratio, which leads to unevenly dis-
tributed space vectors. Conventional modulation methods fail
to produce desired outputs under such situations [36], [37].Therefore, the challenge here is the generation of undistorted
current waveforms even in the presence of unevenly distributed
space vectors.
Extensive research has been done on modulation and control
of the aforementioned dual inverter topology, especially for mo-
tor drive applications [22][28]. They all have considered cases
where fixed-integer dc-link voltage ratios are present. A space
vector modulation (SVM) method with common mode rejection
is presented in [26]. A pulse width modulation (PWM) scheme
for this dual inverter is explained in [27] for 1:1 and 1:2 voltage
ratios. Although a power sharing controller is proposed in [28]
for dynamically varying dc-link voltages, it also assumes iden-
tical dc-link voltage variations thus making the ratio to be 1:1.A hierarchical modulation method is proposed in [29] to handle
dynamic changes in the auxiliary inverter dc-link voltage.
However, the authors have not found previous work address-
ing the issue of non-integer dynamically changing voltage ratio,
for simultaneous variations in both main and auxiliary inverter
dc-link voltages. Therefore, this paper presents an analysis on
the effects of such variations. Furthermore, modified modula-
tion and control techniques are presented to produce undistorted
current and deliver a constant amount of power to the grid even
in the presence of dynamic variations in both main and aux-
iliary inverter dc-link voltages. The viability of the proposed
direct integration method is tested with a wind energy conver-
sion system. Nevertheless, it can be used in the same way for
other renewable energy sources as well.
II. POWER SHARING AND MAXIMUM POWER POINT TRACKING
The output voltage vector of the dual inverter shown in Fig. 1
is equivalent to the addition of the main inverter voltage vector
and the auxiliary inverter voltage vector as in (1). Real powerdelivered to the load can be expressed as the dot product in
(2) [28]. Furthermore, the load power is equivalent to the sum
of the main inverter power and the auxiliary inverter power as
expressed in (3). Equations (4) and (5) show the relationships
between voltage vectors and corresponding switching states.
With the help of these five equations, an expression can be
derived for the power of the auxiliary inverter, in other words
battery power, as in (6). According to (6), it can be deduced that
the battery power PA has a linear relationship with the main
inverter dc-link voltage Vdc when the output power is constant
(i.e., i and vr are constant):
vr = vM + vA (1)
PL =3
2vr i (2)
PL =3
2(vM + vA ) i = PM + PA (3)
vM =2
3Vdc
SaM + SbMe
j (2/3) + ScMej (2/3)
(4)
vA =2
3Vdcx
SaA + SbA e
j (2/3) + ScA ej (2/3)
(5)
PA =3
2(vr vM) i (6)
where vr is the output voltage vector, vM is the main inverter
voltage vector, vA is the auxiliary inverter voltage vector, and i
is the current vector.
In order to verify this relationship, an experiment was carried
out using the setup shown in Fig. 2(a). A gradually increasing
dc voltage was applied to the main inverter while the battery
voltage was kept constant at 25 V. These input voltages are
plotted in Fig. 2(b). The controller was set to maintain constant
power dissipation through the load, and thus, the load current
was constant as shown in Fig. 2(d). Under this constant power
condition, the battery current showed a linear relationship to the
main inverter voltage with a negative slope as in Fig. 2(c). Since
the battery voltage is constant, the battery current is proportionalto the battery power. Therefore, these results confirm that the
battery power can be controlled by controlling the main inverter
dc-link voltage. The same argument can be extended to develop
a maximum power point tracking (MPPT) method for the wind
turbine generator (WTG) as follows.
According to (3), for a given output power PL , the main in-
verter power solely depends on the battery power. Therefore, the
maximum power point of the wind turbine can easily be tracked
by changing the battery power. Furthermore, the aforementioned
analysis reveals that the battery power can be controlled by con-
trolling the main inverter dc-link voltage. The usual practice is
to maintain this voltage at a constant level, with the help of a
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Fig. 2. (a) Experiment setup used to verify the linear relationship betweenmain inverter dc-link voltage and battery power. (b) DC-link voltage variations.(c) Battery current. (d) Load current of the a phase.
Fig. 3. MPPT controller block diagram.
controlled rectifier or a boost rectifier placed between the main
inverter and the WTG. The same controlled rectifier or the boost
rectifier can be used here to vary the main inverter dc-link volt-
age and thus indirectly track the maximum power point of the
WTG. The controller block diagram for this indirect MPPT is
shown in Fig 3. In this controller, the WTG model generates
a power reference based on the measured wind speed. Then, it
is compared with the instantaneous power of the main inverter.
The error is fed into a PI controller that generates a reference
for the main inverter dc-link voltage.
Fig. 4. Space vector diagrams and output voltage waveforms at differentvoltage ratios.
III. EFFECTS OF VARIABLE DC-LINK VOLTAGE RATIO
As explained in the previous section, the main inverter dc-link
voltage needs to be changed to track the maximum power point
of the WTG. This inevitably results in a non-integer dynami-
cally changing dc-link voltage ratio between the main inverter
and the auxiliary inverter. As the voltage ratio varies, space vec-
tors of the combined inverter get distributed unevenly as shown
in Fig. 4. The challenge here is to generate undistorted current
waveforms even in the presence unevenly distributed space vec-
tors. In the proposed system, it is carried out by using a modified
SVM technique. A detailed analysis on the proposed modulation
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method is given in Section IV and the purpose of this section
is to create the necessary background by analyzing effects of
variable voltage ratio.
All the space vector diagrams, shown in Fig. 4, contain seven
main inverter vectors, called main vectors. They are markedwith
large dots. The hexagon formed by these main vector points is
called the main hexagon. Auxiliary inverter vectors, named as
auxiliary vectors, are denoted by attached subhexagons at each
and every main vector point. From Fig. 4(a) to (c), only one
subhexagon is marked to avoid the diagram being too com-
plex. However, scattered dots in these three diagrams corre-
spond to the edges of missing subhexagons. The size of these
subhexagons depends on the battery voltage, which is assumed
to be constant in the following simulations. The circles found
in each space vector diagram represent the path of the refer-
ence voltage vector that remains unchanged for constant power
dispatch.
Fig. 4(a) shows the combined inverter space vector diagram
for the dc-link voltage ratio of 0 (Vdc = 0). At this point, due to
the absence of a power source in the main inverter dc-link, all theseven main vectors coincide at the origin turning the combined
inverter system into a conventional two-level inverter. In this
particular situation, the battery bank should supply the whole
demand or part of it depending on the capacity. Corresponding
inverter output voltage waveform is attached next to the space
vector diagram. When the main inverter dc-link voltage starts to
increase, corresponding main hexagon appears as in Fig. 4(b)
(f). At the ratio of 0.25, subhexagons overlap with each other as
shown in Fig. 4(b) producing four layers of hexagon rings. In
other words, the resultant space vector diagram is equivalent to
that of a 5-level inverter. But due to the uneven distribution of
the hexagons and the low resolution, only few voltage levels canbe seen in the attached waveform. At the ratio of 0.5, vectors get
distributed evenly and three layers of hexagon rings are formed
as shown in Fig. 4(c). Therefore, this particular state represents
a 4-level inverter. Corresponding voltage levels can clearly be
seen in the attached waveform in Fig. 4(c).
At the ratio of 1, the combined inverter resembles a 3-level
inverter (two layers of hexagon rings) with the space vector
pattern shown in Fig. 4(d). Further increase of the main inverter
voltage would expand the space vector diagram as shown in
Fig. 4(e) and (f). At the ratio of 1.5, four layers of hexagons
emerge again resulting in a 5-level inverter. But this time only
outermost vectors are distributed unevenly. Furthermore, the
resolution between voltage levels is high compared to that inFig. 4(b). The space vector diagram at the ratio of 2 is equivalent
to a 4-level inverter as evident from Fig. 4(f). The attached
waveform shows only five levels since the reference circle is
insidethe first layer of hexagon.If thereferencecircle is enlarged
to the next layer, more voltage levels would appear in the output
voltage.
The output voltage waveforms shown in Fig. 4 are in fact
the snapshots taken at six discrete values of the dc-link voltage
ratio. But as explained earlier, the voltage ratio can take any
value between 0 and 2. Therefore, it is important to see how
the output voltage waveform looks like at intermediate values.
Hence, a simulation was carried using the voltage ratio as the
Fig. 5. (a) Inverter output voltage, vas , at different voltage ratios. (b) Funda-mental component ofvas .
Fig. 6. Square wave output of the main inverter and smoothing effect of theauxiliary inverter.
independent variable and the result is shown in Fig. 5(a). At
the ratio of 0, the output voltage waveform is similar to that
in Fig. 4(a). The same scenario can be seen near the ratio of
1.125 as well. In between these two points, a varying waveform
can be seen and it gets optimized at the ratio of 0.5. Beyond
this point, the inverter output voltage waveform gets distortedgradually until the ratio reaches 1. This is due to the decrease
of available voltage levels. However, beyond the ratio of 1,
the waveform again starts to show a continuous improvement
as seen in the latter half of the waveform in Fig. 5(a). With
this result, it can be deduced that the proposed dual inverter
under a noninteger dynamically changing voltage ratio would
produce variable voltage levels similar to that of 2-, 3-, 4-, and
5-level inverters. But with the proposed modulation technique,
it still can synthesize the desired fundamental output voltage
waveform as shown in Fig. 5(b), until the ratio reaches 1.75.
Distortions can occur beyond this point.
IV. MODULATION STRATEGY
As mentioned in Section 1, the main inverter operates in the
six-step mode producing square wave outputs. The auxiliary
inverter is used to compensate harmonic power of the square
wave output and to regulate the real power exchange with the
grid. This combined operation is illustrated in Fig. 6 where the
auxiliary inverter is purposely turned off until 20 ms. During
this period, the only available output is the main inverter square
wave output voltage as shown in the first half of the waveform in
Fig. 6. Harmonic distortion of the output voltage is significant
under this operation. After 20 ms, the auxiliary inverter is turned
on, and consequently, the output voltage becomes smooth with
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Fig. 7. (a) Space vector diagram with the three-axis coordinate system. (b)Shaded triangle with dwell times.
Fig. 8. Block diagram showing the proposed modulation method.
low harmonic distortion as shown by the second half of the
waveform in Fig. 6.
A modified SVM method is proposed for the auxiliary in-verter, and thus, the overall modulation can be considered as a
combination of the six-step mode and SVM. The complexity
of this combined modulation process gets further amplified by
the dynamic variations present in dc-link voltages. To reduce
most of the computational complexities, the three-axis coordi-
nate system shown in Fig. 7(a) is used [30]. In this coordinate
system, each and every vector point is represented by three co-
ordinates that are projections on the axes ofVab , Vbc , and Vca . In
fact, these three axes represent line-to-line voltages of a three-
phase system. If dc-link voltages are fixed, these projections can
be normalized to get discrete values such as 1, 0, and 1. But inthe proposed system, dc-link voltages are not fixed, and hence,
projection can take any value within the operating range. As asolution to this issue, all the calculations are carried out using
actual voltages instead of normalized values, which should be
updated at every switching cycle. A simplified block diagram
of the proposed modulator is shown in Fig. 8.
Since the main inverter operates in the six-step mode, the
main vector selection and gate signal generation units in the
modulator would require only the angle information of the ref-
erence vector, i.e. r . Based on this angle, three normalizedcoordinates of the current main vector, Sab , Sbc , and Sca , are
defined as temporary variables that are then used to calculate
actual projections as expressed in (7). At the same time, three
axis coordinates of the reference voltage vector vr are calculated
TABLE ISWITCHING SIGNAL LOOKUP TABLE
as corresponding line-to-line voltages vab , vbc , and vca . Accord-ing to (1), the difference between the reference vector and the
main vector is the compensation vector that should be supplied
by the auxiliary inverter, and thus, it becomes the reference for
the auxiliary inverter. Projections of this new reference are cal-
culated using (8) and subsequently normalized by (9) to obtain
floor and ceiling values as floor(x) is the greatest integerxandceiling(x) is the smallest integer x. Those floor and ceilingvalues of the normalized reference are then used to locate the
triangle in the subhexagon, for example the shaded triangle in
Fig. 7(a), where the reference vector falls [30], [31]. The ends of
this triangle contain required auxiliary vectors V1 , V2 , and V3 .
But still they are defined using three axis coordinates. In order tomap three axis coordinates into gate signals, the transformation
in (10) and the lookup table in Table I are used:
[Vab Vbc Vca ]T =
Vdc3
[Sab Sbc Sca ]T
(7)
Sab , Sbc , Sca = {1, 0, 1}[vabx vbcx vca x ]
T = (Vab vab ) (Vbc vbc ) (Vca vca )]T
(8)
[vabx vbcx vca x ]T =
3
Vdcx[vabx vbc x vca x ]
T (9)
Ssn = 4x + 2y + z + 3 (10)
where the three axis coordinates are assumed to be in the form
ofVn (x,y,z), n = 1,2,3, and the resulting switching state numberis denoted by Ssn .
Once the three nearest vectors are identified, the next step
is to find corresponding dwell times for each and every vec-
tor. Usually, this part involves multiplications, divisions, and
trigonometric operations that consume significant amount of
processing time. But in the SVM technique adopted in this pa-
per, dwell time calculations are very simple and straightforward.
It is proven in [30] that dwell times are proportional to the dis-tance from the reference vector point to the opposite leg of the
triangle. For example, for the vector V1 in Fig. 7(b), the dwell
time is proportional to the distance d1 from the reference vector
to V2V3 leg of the triangle. In other words, it is proportionalto the difference between vab component (projection on the Vabaxis) of the reference and the corresponding floor value. The
other two dwell times, d2 and d3 , can also be calculated in the
same way. Therefore, to calculate dwell times only subtractions
are needed. This yields fast operation and simple implementa-
tion in hardware level. After finding auxiliary vectors and dwell
times, five-segment switching is used in the auxiliary inverter
as described in [32].
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Fig. 9. Voltage vector additions for different input power conditions at r =60: (a) case 1, (b) case 2, and (c) case 3.
V. ANALYSIS ON BATTERY CHARGING AND DISCHARGING
Charging and discharging process of the battery can be ex-
plained under three different cases where the available wind
power is less than the demand, equal to the demand, and higher
than the demand. In the first case, the battery bank should dis-
charge to supply the deficit and in the third case it should absorbthe surplus of power. However, in the second case, the battery
bank will not be affected. With the help of Figs. 2 and 4, a vague
relationship between these three cases and the dc-link voltage
ratio can be identified as follows.
Case 1: corresponds to 0 < dc-link voltage ratio < 1.Case 2: corresponds to dc-link voltage ratio 1.Case 3: corresponds to 1 < dc-link voltage ratio < 2.
To understand it further, voltage vector additions shown in
Fig. 9 can be used. The vector additions shown in Fig. 9 cor-
respond to r = 600 . At this angle, and its multiples, both the
main vector and the auxiliary vector get aligned making theanalysis easier. When the dc-link voltage ratio is less than 1,
the circular path of the reference voltage vector lies outside the
main hexagon as shown in Fig. 4(b) and (c). Hence, the magni-
tude of the main inverter vector vM is obviously less than that
of the reference vector vr , as shown in Fig. 9(a). As a result,
the auxiliary inverter voltage vector vA has to be used to fill the
gap. Since the same current flows through both inverters, cor-
responding share of power depends only on the magnitude of
the voltage vector. In certain cases, where both inverters should
equally share the output power, the main and auxiliary inverter
vectors are set to be equal [33]. But in the proposed system, the
maximum possible power should be extracted from the main
inverter, and thus, only the balance should be handled by theauxiliary inverter. This automatically happens when the main
inverter is operating at the six-step mode, and hence, no special
attention is required.
When both the circle and main hexagon are at the same mag-
nitude, the main inverter vector itself is sufficient to synthesize
the reference vector as in Fig. 9(b). This roughly corresponds
to the dc-link voltage ratio of 1, as in Fig. 4(d). However, it is
noteworthy to mention that the size of the reference circle, and
hence the dc-link voltage ratio, where the main hexagon meets
the circle, can change with the power demand. When the dc-link
voltage ratio is greater than 1, the main hexagon exceeds the ref-
erence circle as in Fig. 4(e) and (f). In this case, the direction
Fig. 10. (a) Wind speed. (b) Main inverter dc-link voltage Vd c and auxiliaryinverter dc-link voltage Vd cx . (c) Wind power Pw and dispatch power Pd . (d)Battery current Ib . (e) Inverter output current ias . (f) Inverter output voltagebefore filtering vas . (g) Inverter output voltage after filtering, vas ,f .
of the auxiliary inverter vector becomes negative as shown inFig. 9(c). This indicates that part of the available wind power
flows into the battery bank.
According to the abovementioned analysis, it can be deduced
that as long as the circle lies outside themain hexagon the battery
current is positive (discharge). When the reference circle and the
main hexagon are equal in size, the battery current tends to be
zero, which indicates that the available wind power is barely
sufficient to supply the demand. Further increase of the main
inverter dc-link voltage makes the main hexagon to exceed the
voltage reference circle and changes the direction of the battery
current. In other words, the battery bank absorbs part of the
available wind power.
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TABLE IISYSTEM PARAMETERS OF THE SIMULATION SETUP
VI. SIMULATION RESULTS
The proposed concept of ESS interfacing with the grid side
inverter has been tested in a MATLAB/SIMULINK-PLECS
digital simulation platform. The wind speed profile shown in
Fig. 10(a) is used in the simulation, which in turn produces
a dc-link voltage variation at the main inverter as shown in
Fig. 10(b). Corresponding wind power variation Pw and dis-patch power Pd are shown in Fig. 10(c). From this graph, it can
be concluded that the proposed system has the ability to supply
the demand amidst fluctuations present in the input power. The
surplus or deficit of power is supplied or absorbed by the battery
with a current profile as shown in Fig. 10(d). The output cur-
rent and voltage of the inverter are shown in Fig. 10(e) and (f),
respectively. Although the inverter output voltage shows some
fluctuations, once it is passed through a low-pass filter, a smooth
waveform can be observed as shown in Fig. 10(g). The system
parameters of the simulation setup are given in Table II.
VII. EXPERIMENTAL RESULTS
The schematic diagram and photographs of the laboratory
prototype are shown in Fig. 11(a) and (b), respectively. A pro-
grammable ac source is used to emulate the WTG and its output
was rectified using a bridge rectifier. The ac source was pro-
grammed in a way that the rectifier output voltage, in other
words the main inverter dc-link voltage, varies as shown in the
red graph (Vdc ) of Fig. 11(c). During the experiment, the bat-
tery voltage remained at 25 V as shown by the green line (Vdcx )
in Fig. 11(c). The two inverters were coupled through an RL
load and their parameters are given in Table III. The controller
was set to maintain constant power dissipation through the load
as shown in Fig. 11(d) by the graph marked with PL . The in-put power and battery power variations are plotted in the same
figure and are marked as PM and PA , respectively. The corre-
sponding battery current variation is shown in Fig. 11(e). The
shape of this graph is similar to that of the battery power dia-
gram since the battery voltage remains constant. Furthermore,
when the main inverter voltage is lower than the battery voltage,
the battery current is positive and it is negative when the main
inverter voltage exceeds the battery voltage. An enlarged view
of the inverter output current is shown in Fig. 11(f). An en-
larged view of the inverter output voltage is given in Fig. 11(g)
to show the multilevel operation of the proposed dual inverter
system.
Fig. 11. (a)Schematic of theexperimentalsetup. (b)Photographsof theexper-imental setup. (c) DC-link voltages, Vd c and Vd cx . (d)Maininverter power PM ,battery power PA , and output power PL . (e) Battery current Id cx. (f) Enlarged
view of the output current. (g) Enlarged view of the inverter output voltage.
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TABLE IIISYSTEM PARAMETERS OF THE EXPERIMENTAL SETUP
VIII. CONCLUSION
Additional switches and converters required to integrate en-
ergy storage devices into distributed power systems can be
avoided if the grid-side inverter itself can be used as the in-
terface. Accordingly, a modified topology of the popular dual
inverter system has been proposed to connect a battery bank
directly to the auxiliary inverter dc link. The challenge with
this topology is the uncorrelated and dynamic changes present
in dc-link voltages, which results in unevenly distributed spacevectors. A detailed analysis on the effects of such variations is
presented in this paper. Furthermore, a modified SVM method is
proposed to produce desired current waveforms even in the pres-
ence of unevenly distributed space vectors. The battery charg-
ing/discharging process with the proposed control method is
presented in this paper. Experimental and simulation results
are presented to verify the efficacy of the proposed modulation
method and battery charging/discharging process.
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S. D. Gamini Jayasinghe (S10) received the B.Sc.degree in electronics and telecommunication engi-neering fromthe University of Moratuwa, Moratuwa,
Sri Lanka, in 2003. In 2004, he joined the DialogUoM Mobile Communications Research Laboratory.He is currently working toward the Ph.D. degree inthe School of Electrical and Electronic Engineering,Nanyang Technological University, Singapore.
D. Mahinda Vilathgamuwa (S90M93SM99)received the B.Sc. and Ph.D. degrees in electri-cal engineering from the University of Moratuwa,Moratuwa, Sri Lanka, and Cambridge University,Cambridge, U. K., in 1985 and 1993, respectively.
In 1993, he joined the School of Electrical andElectronic Engineering,NanyangTechnological Uni-versity, Singapore, as a Lecturer where he is currentlyan Associate Professor. His current research interestsinclude power electronic converters, electrical drives,and power quality.
Dr. Vilathgamuwa is the Chairman of IEEE Section, Singapore, and a mem-ber of the Power Electronics Technical Committee for the Industrial ElectronicsSociety.
Udaya K. Madawala (M94SM06) received theB.Sc. (Hons.) degree in electrical engineering fromtheUniversityof Moratuwa, Moratuwa, SriLanka, in1987, and the Ph.D. degree in power electronics fromthe University of Auckland, Auckland, New Zealand,in 1993.
In 1997, he joined the Department of Electricaland Computer Engineering, University of Auckland,where he is currently a Senior Lecturer. His researchinterests include motor/generator design and control,power electronics, renewable energy, and super ca-
pacitor applications.Dr. Madawala is an active IEEE volunteer, and serves as an Associate Editor
and a member of the Power Electronics Technical Committee for the IEEEIndustrial Electronics Society.