# A High Voltage Ratio and Low Ripple Interleaved DC-DC Converter for Fuel Cell Applications

Authors: Long-Yi Chang; Kuei-Hsiang Chao; Tsang-Chih Chang
Journal: The Scientific World Journal
 (2012)

---

## Abstract

This paper proposes a high voltage ratio and low ripple interleaved boost DC-DC converter, which can be used to reduce the output voltage ripple. This converter transfers the low DC voltage of fuel cell to high DC voltage in DC link. The structure of the converter is parallel with two voltage-doubler boost converters by interleaving their output voltages to reduce the voltage ripple ratio. Besides, it can lower the current stress for the switches and inductors in the system. First, the PSIM software was used to establish a proton exchange membrane fuel cell and a converter circuit model. The simulated and measured results of the fuel cell output characteristic curve are made to verify the correctness of the established simulation model. In addition, some experimental results are made to validate the effectiveness in improving output voltage ripple of the proposed high voltage ratio interleaved boost DC-DC converters.


---

## Body

## 1. Introduction

Owing to worldwide energy crisis and awareness of environmental protection in recent years, to seek for substitute energy has become an important issue. Among many substitute energies, solar energy, wind energy, hydroelectric power, biomass energy, and fuel cells are green energies with potential development. As for fuel cells, there tend to have been more and more researches and applications recently. The fuel cell is a clean energy without pollution. Its energy, derived from reversed reaction of electrolyzed water, produces dynamic power. Only water is produced after the reaction; hence, there is hardly any environmental pollution. Fuel cells as a source of power are usually applied to electric hybrid automobiles, distributed electric generation system, and portable and stationary power. Among them proton exchange membrane fuel cells (PEMFCs) are the most commonly used because of the following merits: (1) lower temperature during operation, accordingly leading to rapid turning on and off and rapid reaction to the load change; (2) lower operation pressure, thus with higher safety; (3) easily set in mode system; and (4) lower emission ratio and higher conversion ratio [1–4].Although the proton exchange membrane fuel cell has the advantages mentioned above, due to its own activation loss, ohmic loss, and concentration loss, the output voltage is lowered as a result of load increase. Namely, the fuel cell lowers the output voltage but raises the output current gradually as the output power rises under the added load. Thus, it is a low-voltage high-current output equipment. If we can transfer the low voltage produced by the fuel cell to high voltage, sending it to DC link, there will be a wider range of application [5–13]. In order to upgrade the fuel cell voltage output to the necessary electricity level and avoid the unsteady voltage caused by load change, it is necessary to adjust the fuel cell energy by means of power electronic technique, thus keeping steady the output voltage.Based on this, presented in this paper is a high voltage ratio interleaved DC-DC converter parallelly connected and further interleaved by means of two sets of voltage-doubler boost converters. So besides the advantages of high voltage ratio converter, also because of the effect of parallel connection, the current is dispersed into four routes, thus lowering the current stress of the switch and inductance. In this way it can withstand the high current output while there is a high load. Through the parallel connection of two sets of converters and controlling their interleaved voltage, it is possible to lower the output voltage ripple ratio. Figure1 is the structure of the high voltage interleaved DC-DC converter presented in this paper. The fuel cell provides electricity for the dual interleaved voltage doubler of high voltage ratio converter. Electronic load is used to test the amount of load (light or heavy load); also microcontroller PIC 18F8720 manufactured by Microchip company is used for closed loop control. Because two voltage-doubler boost converters are parallelly connected to interleave the output voltage, the output voltage ripple can be significantly reduced.Figure 1
The system of the presented dual interleaved voltage doubler of high voltage ratio converter.


## 2. Fuel Cells

There is a great variety of fuel cells; also there are different ways to classify them. The common approach is to classify them according to the various qualities of the electrolyte. Thus, they can be divided into the following six kinds:(1)
proton exchange membrane fuel cell, PEMFC,(2)
alkaline fuel cell, AFC,(3)
phosphoric acid fuel cell, PAFC,(4)
molten carbonate fuel cell, MCFC,(5)
solid oxide fuel cell, SOFC,(6)
direct methanol fuel cell, DMFC.Among them, the proton exchange membrane fuel cell is the best choice when we choose fuel cells for the source of the applied power because of the following reasons: (1) lower operation temperature, thus it can be rapidly turned on and off; (2) lower operation pressure, hence greater safety; (3) it can be easily set into mode system; (4) lower emission ratio and higher conversion ratio.


### 2.1. Mold Building of Fuel Cells

As for fuel cells, this paper adopts the NEXA proton exchange membrane fuel cell produced by Ballard Company. The specifications of this proton exchange fuel cell are shown in Table1 [14].Table 1
Specifications of the Ballard NEXA proton exchange membrane fuel cell [14].
Power
Rated power
1200 W
Operating voltage range
22–50VDC
Voltage at rated power
26 V
Current at rated power
46 A
Startup time
2 minutes
Emissions
Noise
72 dBA
Water
870 mL/hr
Physical
Dimensions
56
×
25
×
33 cm
Mass
13 kg
Fuel
Purity
99.99% H2 (vol)
Pressure
0.7–17.2 bar
Consumption
<18.5 SLPMIn building up the proton exchange membrane fuel cell math model, currently there are many simple precise model parameters and calculation formulae being presented and developed [15, 16]. In this paper we refer to the electrochemistry formulae already presented to build up the math model of the proton exchange membrane fuel cell, also within the range of the load current operation simulate the characteristic curve of the output voltage and power rate of the fuel cell [15, 16].The math model of the proton exchange membrane fuel cell is shown in(1)Vstack=NVFC,VFC=ENernst-Vact-Vohmic-Vcon.
Therein, Vstack is the stack output voltage; N the number of cells forming the stack; VFC  the output voltage of the fuel cell; ENernst the output voltage produced by every piece of fuel cell in thermodynamics; Vact the activation loss; Vohmic the ohmic loss; Vcon the concentration loss.And the thermodynamic output voltage of every piece of fuel cell can be shown as follows.(2)ENernst=1.229-0.85×10-3(T-298.15)+4.31×10-5T[ln(PH2)+12ln(Po2)].
Therein, T is the cell temperature (in Kelvin); PH2 is the partial pressures of hydrogen; PO2 is the partial pressures of oxygen.As for activation loss voltage, it can be shown this way:(3)Vact=-[ξ1+ξ2×T+ξ3×T×ln(CO2)+ξ4×T×ln(IFC)].
Therein, ξ1,ξ2,ξ3,ξ4 is the parametric coefficient for each cell model; CO2 the concentration degree of oxygen in the catalytic interface of the cathode; IFC the fuel cell current.And the respective coefficients of the activation loss are(4)ξ2=0.00286+0.0002×ln(A)+4.3×10-5×ln(CH2),CO2=PO2[5.08×106×e(-498/T)].
Therein, A is the cell active area, CH2 is the liquid phase concentration of hydrogen.As for ohmic loss voltage, it can be shown as follows:(5)Vohmic=IFC×(RM+RC).
Therein, RM is the resistance coefficient of the membrane, RC is the resistance coefficient constant to protons transfer through the membrane.The resistance coefficient of the membrane therein is(6)RM=ρM×LA.
Therein, ρM is the specific resistivity of the membrane to the electron flow, L is the thickness of the membrane.The resistance coefficient of the membrane can be shown to be(7)ρM={181.6×[{(IFCA)2.5}1+0.03×(IFCA)+0.062×(T303)2×(IFCA)2.5]}/{[λ-0.634-3×(IFCA)×e[4.18×(T-303)/T]]}.
Therein, λ is the adjustment parameter, the range of which is between 14 and 23.Concentration loss formula is shown to be(8)Vcon=-B×ln(1-jjmax).
Therein, B is the constant variable depending on the cell type and its working status; J is the current density of the cell; jmax is the maximum current density.Therein, the current density of the cell is(9)j=IFCA.
Therefore, the equivalent circuit of the fuel cell can be worked up as in Figure 2.Figure 2
The equivalent circuit of the fuel cell.If we take the dynamic response of the fuel cell into consideration, when two different substances come into contact or the load current flows from one end to the other, accumulation of charge is produced on the contact area. In the fuel cell, the layer of change between the electrode and electrolyte (or compact contact face) will accumulate electric charge and energy, whose action is similar to capacitance. So when the load current changes, there will be charge and discharge phenomena happening on the charge layer. Meanwhile, activation loss voltage and concentration loss voltage will be under the influence of transient response, causing delay. But ohmic loss voltage will not be influenced or delayed. We can take this into consideration to let first-order lag exist in activation loss voltage and concentration loss voltage. Thus, its dynamic response equation can be shown to be [15, 16]
(10)VFC=ENernst-Vohmic-Vc,dVcdt=IFCC-Vcτ,τ=C×Ra.
Therein, τ is the time constant; C is the equivalent capacitance of the system; Vc is the dynamic voltage of the fuel cell; Ra is the equivalent resistance.The analysis shown above can be used to build up the mathematical model of the proton exchange membrane fuel cell so as to carry on the simulation analysis of the system.


### 2.2. The Simulation of the Fuel Cell

In this paper PSIM simulation software is used to build up the simulated model of the proton exchange membrane fuel cell. Its composition module is shown in Figure3, in which the upper right increased k value is 42, representing the stack amount of the single cell in the cell stack. The simulated circuit of the equivalent capacitance dynamic action is shown in Figure 4.Figure 3
The fuel cell model built up by means of PSIM software.Figure 4
The simulated circuit of capacitance equivalent dynamic action built up by means of PSIM software.The DLL in Figure3 is the dynamic link library of PSIM simulation software. Through software Microsoft Visual C++ 6.0, the necessary DLL file for linking can be set up. By means of Microsoft Visual C++ 6.0, we can make use of programs to write the mathematical formulas in them, saving the trouble of building up numerous inner circuit figures.After building up fuel cell model, we have its load current operated within fixed rate and value. The hydrogen and oxygen pressures are, respectively, set up at 1 bar. The characteristic curve of the simulated fuel cell output voltage and power rate is shown in Figure5. The upper part of Figure 5 is the curve of the current and voltage of the fuel cell, while the lower part is the power rate curve. Compared with Figure 6, the actual measuring output curve of Ballard Co. NEXA fuel cell, we can find both of the curves of the output characteristics are closely similar. Only because the curve of Figure 6 is formed by connecting from point to point, it follows that there is slight difference between them.Figure 5
The curve of the fuel cell output by means of PSIM software simulation.Figure 6
The curve of the actual measuring output of Ballard Co. NEXA fuel cell [14].


## 2.1. Mold Building of Fuel Cells

As for fuel cells, this paper adopts the NEXA proton exchange membrane fuel cell produced by Ballard Company. The specifications of this proton exchange fuel cell are shown in Table1 [14].Table 1
Specifications of the Ballard NEXA proton exchange membrane fuel cell [14].
Power
Rated power
1200 W
Operating voltage range
22–50VDC
Voltage at rated power
26 V
Current at rated power
46 A
Startup time
2 minutes
Emissions
Noise
72 dBA
Water
870 mL/hr
Physical
Dimensions
56
×
25
×
33 cm
Mass
13 kg
Fuel
Purity
99.99% H2 (vol)
Pressure
0.7–17.2 bar
Consumption
<18.5 SLPMIn building up the proton exchange membrane fuel cell math model, currently there are many simple precise model parameters and calculation formulae being presented and developed [15, 16]. In this paper we refer to the electrochemistry formulae already presented to build up the math model of the proton exchange membrane fuel cell, also within the range of the load current operation simulate the characteristic curve of the output voltage and power rate of the fuel cell [15, 16].The math model of the proton exchange membrane fuel cell is shown in(1)Vstack=NVFC,VFC=ENernst-Vact-Vohmic-Vcon.
Therein, Vstack is the stack output voltage; N the number of cells forming the stack; VFC  the output voltage of the fuel cell; ENernst the output voltage produced by every piece of fuel cell in thermodynamics; Vact the activation loss; Vohmic the ohmic loss; Vcon the concentration loss.And the thermodynamic output voltage of every piece of fuel cell can be shown as follows.(2)ENernst=1.229-0.85×10-3(T-298.15)+4.31×10-5T[ln(PH2)+12ln(Po2)].
Therein, T is the cell temperature (in Kelvin); PH2 is the partial pressures of hydrogen; PO2 is the partial pressures of oxygen.As for activation loss voltage, it can be shown this way:(3)Vact=-[ξ1+ξ2×T+ξ3×T×ln(CO2)+ξ4×T×ln(IFC)].
Therein, ξ1,ξ2,ξ3,ξ4 is the parametric coefficient for each cell model; CO2 the concentration degree of oxygen in the catalytic interface of the cathode; IFC the fuel cell current.And the respective coefficients of the activation loss are(4)ξ2=0.00286+0.0002×ln(A)+4.3×10-5×ln(CH2),CO2=PO2[5.08×106×e(-498/T)].
Therein, A is the cell active area, CH2 is the liquid phase concentration of hydrogen.As for ohmic loss voltage, it can be shown as follows:(5)Vohmic=IFC×(RM+RC).
Therein, RM is the resistance coefficient of the membrane, RC is the resistance coefficient constant to protons transfer through the membrane.The resistance coefficient of the membrane therein is(6)RM=ρM×LA.
Therein, ρM is the specific resistivity of the membrane to the electron flow, L is the thickness of the membrane.The resistance coefficient of the membrane can be shown to be(7)ρM={181.6×[{(IFCA)2.5}1+0.03×(IFCA)+0.062×(T303)2×(IFCA)2.5]}/{[λ-0.634-3×(IFCA)×e[4.18×(T-303)/T]]}.
Therein, λ is the adjustment parameter, the range of which is between 14 and 23.Concentration loss formula is shown to be(8)Vcon=-B×ln(1-jjmax).
Therein, B is the constant variable depending on the cell type and its working status; J is the current density of the cell; jmax is the maximum current density.Therein, the current density of the cell is(9)j=IFCA.
Therefore, the equivalent circuit of the fuel cell can be worked up as in Figure 2.Figure 2
The equivalent circuit of the fuel cell.If we take the dynamic response of the fuel cell into consideration, when two different substances come into contact or the load current flows from one end to the other, accumulation of charge is produced on the contact area. In the fuel cell, the layer of change between the electrode and electrolyte (or compact contact face) will accumulate electric charge and energy, whose action is similar to capacitance. So when the load current changes, there will be charge and discharge phenomena happening on the charge layer. Meanwhile, activation loss voltage and concentration loss voltage will be under the influence of transient response, causing delay. But ohmic loss voltage will not be influenced or delayed. We can take this into consideration to let first-order lag exist in activation loss voltage and concentration loss voltage. Thus, its dynamic response equation can be shown to be [15, 16]
(10)VFC=ENernst-Vohmic-Vc,dVcdt=IFCC-Vcτ,τ=C×Ra.
Therein, τ is the time constant; C is the equivalent capacitance of the system; Vc is the dynamic voltage of the fuel cell; Ra is the equivalent resistance.The analysis shown above can be used to build up the mathematical model of the proton exchange membrane fuel cell so as to carry on the simulation analysis of the system.


## 2.2. The Simulation of the Fuel Cell

In this paper PSIM simulation software is used to build up the simulated model of the proton exchange membrane fuel cell. Its composition module is shown in Figure3, in which the upper right increased k value is 42, representing the stack amount of the single cell in the cell stack. The simulated circuit of the equivalent capacitance dynamic action is shown in Figure 4.Figure 3
The fuel cell model built up by means of PSIM software.Figure 4
The simulated circuit of capacitance equivalent dynamic action built up by means of PSIM software.The DLL in Figure3 is the dynamic link library of PSIM simulation software. Through software Microsoft Visual C++ 6.0, the necessary DLL file for linking can be set up. By means of Microsoft Visual C++ 6.0, we can make use of programs to write the mathematical formulas in them, saving the trouble of building up numerous inner circuit figures.After building up fuel cell model, we have its load current operated within fixed rate and value. The hydrogen and oxygen pressures are, respectively, set up at 1 bar. The characteristic curve of the simulated fuel cell output voltage and power rate is shown in Figure5. The upper part of Figure 5 is the curve of the current and voltage of the fuel cell, while the lower part is the power rate curve. Compared with Figure 6, the actual measuring output curve of Ballard Co. NEXA fuel cell, we can find both of the curves of the output characteristics are closely similar. Only because the curve of Figure 6 is formed by connecting from point to point, it follows that there is slight difference between them.Figure 5
The curve of the fuel cell output by means of PSIM software simulation.Figure 6
The curve of the actual measuring output of Ballard Co. NEXA fuel cell [14].


## 3. Single Set of Voltage-Doubler Boost Converter

Shown in Figure7 is the circuit structure of single set voltage-doubler boost converter [17, 18]. It is made up of interleaved boost converters with a clamp capacitor C1. The circuit structure is simple and it can reach the same high voltage ratio with lower duty cycle. Therefore, it can reduce the conduction loss of the switch, to further upgrade the efficiency of the whole converter. The work theorem of the whole circuit can be divided into four operation modes, of which the equivalent circuits are, respectively, shown in Figures 8(a)–8(d).Figure 7
Circuit structure of voltage-doubler boost converter.The four switch modes of voltage-doubler boost converter in the duty cycle: (a) model 1, (b) model 2, (c) model 3, and (d) model 4.
(a)
(b)
(c)
(d)The equivalent circuits of mode 1 and mode 3 are exhibited in Figures8(a) and 8(c). In this situation, switches S1 and S2 are turned on. Input voltage Vi stays between inductance L1 and L2, making the inductance current increase linearly, and begins to deposit energy, and the load current is provided by capacitor Co. The change of the inductance current iL1 and iL2 can be shown in
(11)Vi=L1diL1dt=L2diL2dt.Figure8(b) is the equivalent circuit in mode 2, in which switch S1 is turned off while S2 is turned on. The inductance current in forward direction conducts diode D1. In the meantime inductance L1 voltage releases energy to clamp capacitor C1, charging capacitor C1, while inductance L2 goes on depositing energy. The change of the inductance current iL1 can be shown in
(12)diL1dt=Vi-VC1L1.The equivalent circuit of mode 4 is exhibited in Figure8(d), in which switch S1 is turned on and switch S2 is turned off. The inductance current in forward direction conducts diode D2. Then inductance L2 and clamp capacitor C1 simultaneously release energy to output capacitor Co and load. The change of inductance current iL2 can be shown in
(13)diL2dt=Vi+VC1-VOL2.Through the analysis of the four modes mentioned above, onlyVC1 capacitor voltage is an unknown variable. According to circuit structure and KVL theorem, inductance L1, L2 and the voltage of diode D1 plus clamp capacitor voltage VC1 should be zero, and in steady state the average voltage of inductance L1 and L2 is zero. Therefore, it is known that the average voltage of D1 is identical with clamp capacitor voltage VC1. The waveform of D1 voltage is exhibited in Figure 9, so the clamp capacitor voltage VC1 can be shown in
(14)VC1=VD1,avg=VO2.Figure 9
Voltage waveform of diodeD1 under each mode.After getting the clamp capacitor voltage, we work out (11)–(13) according to volt-second balance theorem and get (15). Then we carry in (14) to work out (16). Therefore, we can infer that the voltage increase of the converter is shown in (17), in which T is the switching cycle, D is the duty cycle and f is the switching frequency:
(15)Vi-VC1L1×(1-D)T+ViL1DT=0,(16)Vi-(VO/2)L1×(1-D)T+ViL1DT=0,(17)VO=2Vi1-D.From (17) it is known that voltage-doubler boost converter can reach the same high voltage ratio with a shorter duty cycle. Moreover on account of the added clamp capacitor, the voltage of the switch can be reduced to only half of the output voltage. This can be known from the switch voltage of (18) while operating under mode 2 and mode 4:
(18)Vds1,max=VC1=VO2,Vds2,max=VC1=VO2.The output and input power can be shown, respectively, in(19)PO=VO2R,(20)Pi=ViIi=Vi×(IL1+IL2).
From (20), assuming L=L1=L2, it follows
(21)Pi=ViIi=Vi×2IL.
If there is no power loss of the converter, then Po=Pi with the following result
(22)Vi×2IL=VO2R=(2Vi/(1-D))2R=4Vi2(1-D)2R,IL=2Vi(1-D)2R,IL1=IL2=IL.The waveform of inductance currents is exhibited in Figure10, in which though iL1 and iL2 waveforms are in complementary relation, its maximum and minimum inductance current are the same. Hence based on IL1, the related formulae of the maximum and minimum inductance current are, respectively, shown in
(23)IL1,max=IL1+ΔiL12=2Vi(1-D)2R+ViDT2L1,IL1,min=IL1-ΔiL12=2Vi(1-D)2R-ViDT2L1.Figure 10
The waveform of the change of inductance current.The condition on which the converter can be operated in continuous current mode is thatiL1,min and iL2,min should at least be greater than zero. So the boundary condition of continuous and discontinuous inductance current is
(24)IL1,min=0=2Vi(1-D)2R-ViDT2L1.
So we get
(25)L1,min=D(1-D)2R4f.Because the maximum and the minimum induction currents of inductanceL1 and L2 are the same, the minimum induction rates derived from L1 and L2 are identical. Hence, if the converter is to be operated in the continuous current mode, inductance L1 and L2 must at least be greater than or equal to L1,min.From the mathematic functionD(1-D)2 of (25), it can be observed if D value is at 1/3, the mathematic function D(1-D)2 will have the maximum value, which also means the maximum D value created by (25) is 1/3. Hence in designing inductance, when D as 1/3 is substituted into (25), and let the inductance value derived from calculation be multiplied by surplus value 1.25, it can be assured that the inductance current can really work in the continuous current mode.The load impedances of so-called light load and heavy load in this paper, are respectively, 2,020 Ω and 450 Ω. So at switching frequency 15 kHz, heavy load duty cycle about 0.85 when it is substituted into (25), the result is that in order to let the current continue under light load, the least inductance should be 6.23 mH, while under heavy load it should be 179 μH. In this paper 260 μH is the option to make it possible to be in continuous current conduction mode under heavy load.The change of output capacitor current is shown in theiCo of Figure 11. From Figure 11 we know the amount of capacitor electric charge change as
(26)|ΔQ|=VODTRO=COΔVO.
Then its voltage ripple ratio may be expressed as follows:
(27)ΔVOVO=DTROCO.Figure 11
The switch signal, inductance, and capacity waveforms under each operation mode.So the result is(28)CO=DROf(ΔVO/VO).Therefore in the converter, we can decide the size of the capacitor according to the amount of voltage ripple ratio. From (28) it is observed that the output capacity and duty cycle are in linear relation. It means the designed output capacity must be greater than the required capacity with the maximum duty cycle. In this paper voltage ripple ratio is set at 5%. When it is substituted into (28), the output capacity is 2.5 μF. So 150 μF is selected to make the voltage ripple ratio lower than 5%.By means of the above-described operation mode of the converter, the switch control signal in the circuit, inductance and capacity current waveform can be exhibited in Figure11, and its input voltage ripple and current ripple can be shown in
(29)ΔIi=(VO/2-ViLn-ViLn)(1-D)T=VO-4Vi2Ln(1-D)T;Ln∈{L1,L2},(30)ΔVCo=IODT.From (29) it is known that the voltage-doubler boost converter has the advantage of lower input current but the amount of its output voltage ripple is the same as the traditional high voltage converter. Hence in this paper we set forth an ameliorated interleaved voltage-doubler boost converter. By means of the original voltage-doubler boost converter parallelly connected, making output voltage interleaved, so as to reduce output voltage ripple, the flaw of greater output voltage is further ameliorated.


## 4. The Presented Dual Interleaved Voltage Doubler of High Voltage Ratio Converter

The circuit structure of the dual interleaved voltage doubler of high voltage ratio converter presented in this paper is shown in Figure12. By means of parallelly connected original voltage-doubler boost converter to have the two sets of upper and lower voltage mutually interleaved, we can lower its output voltage ripple by controlling one set of their switch control signals to make its output voltage ripple offset that of the other set. In controlling both the upper and the lower sets of switches S1,S2 and S3,S4 to make S1,S2 and S3,S4 switch control phase discrepancy 180° lead to voltage ripple phase displacement, the function of lowering voltage ripple is thus achieved. And because the interleaved switches of these two sets of voltage-doubler boost converters make the input current circuit divide into four routes, thus further lowering the current stress of the inductance and switch, it is possible to withstand the high current of the output of the fuel cell under heavy load. Also it is controlled by microcontroller PIC18F8720. In this way the output voltage can be kept steady at a fixed value.Figure 12
The circuit structure of dual interleaved voltage doubler of high voltage ratio converter.Figure13 shows the control signal, inductance current, and output voltage ripple waveforms in the circuit. From Figure 13 are observed the output voltage ripples of the two converters VO1 and VO2. Through the phase displacement of the switch control signal, the phase displacement of two sets of voltage ripples is brought about, thus resulting in the effect of lowering the output voltage ripple.Figure 13
The ripple waveforms of switch control signal, inductance current, and output voltage under each operation mode.


## 5. Experimental Results

In order to prove the feasibility of the dual interleaved voltage doubler of high voltage ratio converter set forth in this paper, a test will be carried on under two different loads. The fuel cell produces output voltage about 26 to 43 V, to be upgraded to 300 V, and the electronic load is, respectively, adjusted at 2,020 Ω (about output power 43 W) and 450 Ω (about output power 200 W) under test.Figure14 is the waveforms of the switch signal control in dual interleaved voltage doubler of high voltage ratio converter. Switches S1,S3 and S2,S4 have respective control phase discrepancy 180°. Figures 15 and 16 show the waveforms of switch signal, the waveforms of fuel cell output voltage and output voltage of converter, respectively, under output power 43 W and 200 W. From the figures it is observed that under different loads, by controlling the duty cycle of the switch signal, the output voltage of converter can be kept steady at 300 V.Figure 14
The switch signal waveforms of dual interleaved voltage doubler of high voltage ratio converter.Figure 15
The switch signal and input/output voltage waveforms under output power 43 W.Figure 16
The switch signal and input/output voltage waveforms under output power 200 W.Figures17 and 18 are the waveforms of switch signal and inductance current iL1 and iL2 under respective output power 43 W and 200 W. From the figures it is observed that with the gradual increase of loads, the inductance currents iL1 and iL2 are also on the increase to enable it to work in continuous current mode under higher output power.Figure 17
The switch signal,iL1 and iL2 inductance current waveforms under output power 43 W.Figure 18
The switch signal,iL1 and iL2 inductance current waveforms under output power 200 W.Figures19 and 20 are the respective output voltage ripple waveforms of single set voltage-doubler boost converter and the presented dual interleaved voltage-doubler of high voltage ratio converter. From Figures 19 and 20 it is observed that through comparison we find there is improvement in output voltage ripple waveform. In Figure 19 the peak-to-peak voltage of the single set voltage doubler boost converter is about 15.8 V, while that of the presented dual interleaved voltage doubler of high voltage ratio converter in Figure 20 is about 9.5 V. Their respective voltage ripple ratios are 5.27% and 3.17%.Figure 19
The output voltage ripple waveform of single voltage-doubler boost converter under output power 43 W.Figure 20
The output voltage ripple waveform of the presented dual interleaved voltage-doubler of high voltage ratio converter under output power 43 W.Figures21 and 22 are the respective output voltage ripple waveforms of single set voltage doubler boost converter and the presented dual interleaved voltage doubler of high voltage ratio converter. From Figures 21 and 22 it is observed that through comparison we find there is improvement in output voltage ripple waveform. In Figure 21 the peak-to-peak voltage of the single set voltage-doubler boost converter is about 36 V, while that of the presented dual interleaved voltage doubler of high voltage ratio converter in Figure 22 is about 26.25 V. Their respective voltage ripple ratios are 12% and 8.75%. Thus it is proved that the dual interleaved voltage doubler of high voltage ratio converter can improve the flaw of higher voltage ripple ratio of the original single set voltage-doubler boost converter.Figure 21
The output voltage ripple waveform of single voltage-doubler boost converter under output power 200 W.Figure 22
The output voltage ripple waveform of the presented dual interleaved voltage doubler of high voltage ratio converter under output power 200 W.


## 6. Conclusion

This paper sets forth an ameliorated dual interleaved voltage doubler of high voltage ratio converter to improve the problem of output ripple voltage of single set voltage-doubler boost converter. With two parallelly connected voltage-doubler boost converters to interleave the output voltage ripple, we further lower the output voltage ripple. Not only does it maintain the advantages of voltage-doubler boost converter, but also, owing to the interleaved single set converter with two separate current routes and the two sets of switches of the double voltage booster once again in parallel connection leading to four separate current routes, it is thus possible to further lower the current stress of the switch and inductance. Through test and experiment, this paper proves and confirms the feasibility of the presented dual interleaved converter.



---

*Source: 896508-2012-12-23.xml*