Soft Switched Coupled Inductor based High Step Up Converter for Distributed Energy Resources Shelas Sathyan, Student member IEEE, H M Suryawanshi, Senior member IEEE, and A B Shitole Electrical Engineering Department Visvesvaraya National Institute of Technology, Nagpur, India 440010 Email: shelassathyan@yahoo.co.in, hms 1963@rediffmail.com, amardeep.shitole@gmail.com Abstract—In this paper coupled inductor based high step up converter for dc micro grid is proposed. Switched capacitor based improved voltage extension cell is utilized to obtain high voltage gain. By using extended and improved voltage doubler cell, the voltage stress on the main switch and output diode are reduced. So active switches of low RDS(on) can be used and thus overall efficiency of the system is improved. Active clamp technique is incorporated to limit the voltage excursion on main switch and also to obtain zero voltage switching for both main and auxiliary switches which further improve the efficiency and power density. Design and analysis of the proposed converter is carried out and the result are verified by using PSIM Simulation package. Finally, a 500 W experimental prototype is build to verify the theoretical and simulation results. keywords- Coupled Inductor; DC-DC converter; High step up; Zero voltage switching; Active clamp. I. I NTRODUCTION Increasing demand of the electrical energy and the concern of environmental pollution leads to the development of renewable energy based power generation system. Distributed generation systems using renewable and non renewable sources are found to be a better alternative for traditional power generation system [1]. Renewable energy sources like solar photovoltaic, wind, wave and tidal energy systems are highly intermitted in nature and its continuous and steady power generation depend on various factors like environmental conditions, geographical area and time (month) of operation etc. Thus reliable and efficient utilization of these sources require power electronics interfaces [2], [3]. Low voltage dc sources like solar PV and fuel cells require to be connected in series and parallel to obtain sufficient power and voltage level. This will increase the overall system cost. Mismatches due to shading and unhealthy modules reduces the available power and voltage level. It is found that parallel connection of solar PV modules are less sensitive to current mismatches. Since current mismatch causes higher impact on energy yield, parallel connection of solar modules or modular or multi string structure are preferred over a large series strings of PV modules due to less mismatch losses and better tracking of maximum power [4], [5]. So for better utilization of these sources we require individual and dedicated power converters and these converters has to step up the energy sources output voltage to the required utility voltage level. Conventional boost converter can not provide high voltage gain due to its increased conduction losses and voltage stress at high duty ratio operation [6]. Transformer isolated converter k,((( can easily obtain high step up . But the stress on the switches, weight, leakage energy problem and the power density are limiting factors. In [7] non isolated converter using voltage multiplier cell is introduced. But to obtain high conversion ratio multiple such cell has to be used. coupled inductor based converters are an alternative solution for high step up applications. Voltage stress due to leakage inductance in coupled inductor based converter can reduced by using active or passive clamp technique. Voltage extension cell can be utilized to improve the voltage conversion ratio and thus reduce the turn’s ratio of the coupled inductor. In [8], passive clamp coupled inductor converter is introduced for high step up application. But this converter suffer from high voltage stress on output diode. A switched capacitor based coupled inductor converter is introduced in [9]. Here switched capacitor cell charges in parallel and discharges in series to obtain high step up. To get higher power density, converters has to operate at high switching frequency where switching losses dominate the conduction losses. So soft switched converters are preferred over passive clamp converters. In [10] active clamp soft switched coupled inductor converter is presented. But the converters output diode voltage stress are higher. A soft switched extended voltage doubler circuit is presented in [11]. This converter has higher voltage conversion ratio and the voltage stress on output diode is equal to output voltage of the converter. In this paper improved switched capacitor based coupled inductor converter is proposed. Proposed converter has higher voltage gain and less voltage stress on the active switches and output diode. So switches of low RDS(on) can be utilized and thus improve the efficiency. By adding active clamp circuit the voltage stress on the main switch is reduced and zero voltage switching of both main and auxiliary switches are obtained. II. PROPOSED CONVERTER AND OPERATIONAL PRINCIPLE The proposed converter is shown in Fig.1. It consists of a coupled inductor and improved voltage extension cell. Voltage extension cell consisting of two switched capacitors C1 and C2 which charges in parallel and discharges in series as given in [9]. The diodes D1 and D2 forms the charging path for the switched capacitors . Active clamp circuit consists of clamp capacitor Cc and auxiliary switch SAU X . Output diode Do is similar to the output diode of a normal boost converter. The coupled inductor is replaced by its equivalent transformer model with magnetizing inductance Lm and effective leakage inductance Lk referred to primary. N1 and N2 represents number of turns of primary windings and secondary windings Fig.1 Proposed converter of the coupled inductor respectively. Turn’s ratio of the coupled 2 inductor is given by N, where N = N N1 . All switches and other elements are considered to be ideal except leakage inductance of coupled inductor and output capacitance of MOSFETs. Capacitance Cr includes parallel combination of output capacitance of MOSFET switches and winding capacitance of coupled inductor. III. I NTRODUCTION There are eight operating modes in one switching cycle of the proposed converter. Key wave form of the converter is given in Fig.2. In the key wave forms, Vg1 and Vg-aux are the gate signals for main and auxiliary switches. ILK , ILm , Is1 , and Icc are current through leakage inductance, magnetizing inductance, main MOSFET switch and clamp capacitor respectively. The currents through output diode and charging diodes of switched capacitors are given by IDo , ID1 and ID2 respectively. The eight operating modes of the converter are given in Fig.3. Mode 1 (t0 − t1 ): In this mode, the main switch S1 is conducting and the auxiliary switch is turned off. Magnetizing current iLm and leakage current iLk are increases linearly. The output diode Do is reversed biased. The switched capacitors C1 and C2 charges in parallel through the secondary winding of the coupled inductor and diodes D1 and D2 respectively. Load is supplied by output capacitor C0 . Current through magnetizing inductance and leakage inductance are given by iLm (t) = iLm (t0 ) + iin (t) = iLk (t) = iLk (t0 ) + kVin (t − t0 ) Lm (1 − k)Vin (t − t0 ) Lk (1) (2) Vin − Vc1N(t) (t − t0 ) Lk where k is the coupling coefficient. And k is given by (3) 1 Cr (Lm +Lk ) and Z1 = Lm +Lk . Cr Since Cr is very small ,this rise in voltage can be approximated as linear increase. Mode 3 (t2 − t3 ): At t2 , Vds (t) = Vcr (t) becomes equal to Vin +Vcc . Since Cc is much larger than Cr almost all charging currents now flow through the body diode of the auxiliary switch SAUX thus limit voltage excursion on main switch. Leakage inductance and clamp capacitor forms a resonant circuit and the resonant current through Cc is given by VLk (t) sin(ω2 (t−t2 )) Z2 (6) Lm +Lk and Z2 = . Voltage across Cc where ω2 = √ 1 Cc (Lm +Lk ) the magnetizing inductance is given by Lm (4) Lm + LK Mode 2 (t1 − t2 ): At time t1 , main switch S1 is turned off. The leakage inductor current and magnetizing current start to charge parasitic capacitor Cr of the main switch. Voltage across Cr increases from 0V to Vin +Vcc . Voltage across main switch is given by k= Vds (t) = Vcr (t) = Vin (1 − cos ω1 (t − t1 )) + iLk (t1 )Z1 sin(ω1 (t − t1 )) where ω1 = √ iCc (t) = iLk (t) = iLk (t2 )cos(ω2 (t−t2 ))+ which can also be expressed as iLk (t) = iLk (t0 ) + Fig.2 Key waveforms of proposed converter (5) VLm ≈ −VCc Lm Lm + Lk (7) So iLm start to decrease . This mode ends at t3 when the voltage across output diode Do become equal to zero and start to conduct. Mode 4 (t3 − t4 ): At t3 , output diode Do start to conduct. Input voltage Vin , magnetizing inductance Lm , switching capacitors C1 and C2 discharge its energy to the load in series. Leakage inductance Lk continue to resonate with clamp capacitor Cc . In order to get ZVS for auxiliary switch, it Fig. 1. (a) Mode 1 (to - t1 ) (b) Mode 2 (t1 - t2 ) (c) Mode 3 (t2 - t3 ) (d) Mode 4 (t3 - t4 ) (e) Mode 5 (t4 - t5 ) (f) Mode 6 (t5 - t6 ) (g) Mode 7 (t6 - t7 ) (h) Mode 8 (t7 - t8 ) Different modes of operation of proposed converter. should be turned on before clamp capacitor current reverse its direction. Mode 5 (t4 − t5 ): At t4 , gate signal is applied to auxiliary switch. Prior to the application of gate signal, body diode of the switch was in conduction. So Auxiliary switch (SAU X ) turned on with ZVS. Input voltage Vin , magnetizing inductance Lm , switching capacitors C1 and C2 continue to discharge its energy to the load through output diode Do . Resonant current iLk (t) reverse its direction and flow through the auxiliary switch as shown in Fig.3. Mode 6 (t5 − t6 ): This mode start at t5 ,when the auxiliary switch is turned off. Now leakage inductance Lk and parasitic capacitance of Cr forms new resonance circuit and start to discharge the parasitic capacitance voltage Vcr (t). Since Cr is small, the voltage across main switch decreases rapidly. This modes end at t6 , when the parasitic capacitance voltage becomes to zero. In order to achieve ZVS for main switch S1 , energy stored in leakage inductance at this mode should be greater than the energy stored in parasitic capacitor as given in [12] and [13]. So condition for ZVS of the main switch can TABLE I. be expressed as Lk = 2 (t5 ) Cr Vcr 2 iLk (t5 ) Parameters (8) Power Mode 7 (t6 − t7 ): This modes start at t6 , when the parasitic capacitor is fully discharged. Body diode of the main switch S1 start to conduct the current iLk . To achieve ZVS for main switch, Gate pulse Vg1 should applied during this mode. Mode 8 (t7 − t8 ): At time t7 , main switch turns on with ZVS. Leakage inductor current and magnetizing current increases linearly. Output diode current start to decrease. This mode end at t8 , when the output diode currents equal to zero and reverse bias. Here after switched capacitors c1 and c2 start to charge in parallel through secondary of the coupled inductor and cycle repeats. IV. PARAMETERS OF THE PROPOSED CONVERTER Values 500 W Turns Ratio 1:2 Vin 48 V Vo 400 V fs 100 KHz Lm 132μH Lk 2.5μH Cc 3μF C1 , C 2 4.7μF Co 200μF Cr 1.5 nF STEADY STATE ANALYSIS In order to simplify the analysis, coupling coefficient of the coupled inductor is considered to one. ie, no leakage inductance. Only mode 1 and mode 5 are considered for the analysis. Voltage across the capacitors are considered to be constant over one switching cycle. During mode 1, main switch is turned on. Voltage across the magnetizing inductance is given by on = Vin (9) VLm and reflected voltage across secondary is given by on = N.Vin Vsec and (10) Fig.4 Volatge gain comparison of proposed converter Vc1 = Vc2 = N.Vin (11) During the switch turned off duration (Mode 5), voltage across Lm is given by Vin + Vc1 + Vc2 − Vo (12) 1+N By volt-second balance of magnetizing inductance, voltage gain of the proposed converter is obtained as of f VLm = Vo 1 + 2N − N D = Vin 1−D (13) Which is higher than that of the converters proposed in [10] and [11]. Voltage stress on the clamp capacitor is given by D.Vin (14) 1−D Where D is the duty ratio of the converter. Voltage stress on the output diode is less than the output voltage and is given by (1 + N )Vo VDo = (15) 1 + 2N − N D Voltage stress of the main switch is clamped to Vcc + Vin . Which is given by Vin Vds = (16) 1−D Actual voltage gain of the converter will be slightly less than that of the derived one. It is due to the the fact that presence of leakage inductance causes duty cycle loss which slightly reduces the actual voltage gain. Since coupling coefficient of Vcc = the converter is taken as unity for the steady state analysis, effects due to this duty cycle loss is not considered for the derivation of voltage gain. Comparison of voltage gain of proposed converter with respect to that of [11] is shown in Fig.4 for different duty ratio and turn’s ratio. V. SIMULATION AND EXPERIMENTAL RESULTS To verify and to analysis the effectiveness of the proposed converter, A 500 W prototype is designed and simulation of the converter is done in PSIM simulation package. Later experimental prototype of the converter is build and results are verified. Different parameters of the proposed converters are given in Table.1. In Fig.5, simulation results of magnetizing current (iLm ) and leakage currents (iLk ) are given. Where Vg1 and Vg−aux represents the gate signal for main and auxiliary switch respectively. In Fig.6, Simulation result of drain to source voltage of the main switch S1 and current through the switch are shown. The voltage of the main switch is clamped to a voltage below 125 V at full load condition. Zero voltage turn on of the switch is also shown in Fig.6. To get ZVS for the main switch, there should be a time delay between turn off instant of the auxiliary switch and turn on instant of the main switch. The optimum time delay (td ) between turned off of the auxiliary switch and turned on of the main switch is given by √ π Lr Cr td = (17) 2 Fig.5 Simulation result of magnetizing current and leakge inductor current Fig.8 Auxiliary switch voltage, auxiliary switch current and switched capacitor (C1 ) current. Fig.6 Simulation result of volatge across switch S1 and current through S1 Fig.9 Output voltage, Switched capacitor volatge (Vc1 ) and clamp capacitor (Vcc ) voltage. Fig.7 Clamp capacitor current iCc , Diode D1 current iD1 , and output diode current iDo Fig.10 Experimental wave form of volatge across switch S1 with out active clamp, Scale (100V/Div and 5μs/Div) In Fig.7, current through the clamp capacitor (iCc ), diode D1 , and output diode Do at full load is given. Proposed converter is also achieved zero voltage switching for auxiliary switch. In Fig.8, voltage across auxiliary switch and current through the switch are shown. Zero voltage turn on of the auxiliary switch can achieve, if the delay between turn off of the main switch S1 and turn on of the auxiliary switch is adjusted properly. This delay is also taken as td . In Fig.9, Simulation result of output voltage of the converter is shown along with clamp capacitor voltage (Vcc ) and switched capacitor voltage (VC2 ). The ripple in output voltage is less than 1% of the output voltage. A 500 W experimental prototype is tested to verify the design. Parameters for the experimental prototypes are given in table 1. In proposed converter, coupled inductor is different Fig.11 Experimental wave form of volatge across switch S1 , Scale (50V/Div and 2.5μs/Div) Fig.12 Experimental wave form of current through switch S1 . ( Scale 20A/Div and 2.5μs/Div) Fig.14 Converter efficiency as a function of output power VI. Fig.13 Experimental wave form of volatge across switch S1 and current through the switch. ( Scale:50V/Div, 20A/ Div ) from flyback inductor. Here coupled inductor transfer energy to the output during both turn on and turn off period of the main switch. So unlike flyback converter, it does not require large air gap to store energy. This help to choose coupled inductor of small size. For the proposed converter, Arnold Micrometals’s sendust core of part number MS-184125-2 is selected as coupled inductor. Main and auxiliary MOSFET switches are IRFP4227pbF. The clamp capacitor has to carry high impulse current. Polypropylene capacitors are selected for this purpose. Output filter capacitor and switched capacitors are electrolytic type. Leakage inductance of the converter is found to be 2.5μH. To measure exact leakage inductance using π model of two winding transformer, the method given in [14] is utilized. Parasitic capacitance of the MOSFET is taken as Coss ef f and is equal to 360 pF. Control circuit is developed in low cost C2000 Piccolo LaunchPad from Texas instruments. In Fig.10, experimental wave form of the voltage across the main switch (S1 ) without active clamp circuit is given . In this case, voltage spike due to the leakage inductor increases the stress on the switch and also induces EMI. We require switches of higher voltage rating to sustain this spike. In Fig.11 drain to source voltage of the main switch with active clamp is shown. Active clamp circuit effectively clamp the voltage excursion on the switch. So switches of low voltage rating can be used. This improve the efficiency since low voltage rated switch has low Rds(on) . Main switch current iS1 is shown in Fig.12. Zero voltage turn on of main switch S1 is shown in Fig.13. Measured maximum efficiency of the converter is 95.92%. In Fig.14, efficency of the proposed converter for different power level is given. Efficiency of the proposed converter remains in the range of 95% for most of the load condition. C ONCLUSION In this paper coupled inductor based high step up active clamp converter is proposed for low voltage renewable and non renewable energy sources. In order to validate the design, simulation and experimental result of the converter is given. Improved and extended voltage doubler cell is utilized to increase the voltage gain of the converter. This reduces the output diode stress compared to the conventional boost and other coupled inductor converters. The voltage stress on the active switches is eliminated by using active clamp technique. 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Basso, “How to deal with leakage elements in flyback converters,” Motorola Semiconductor Application Note, 2005. Shelas Sathyan received B.Tech degree in electrical and electronics engineering from Government College of Engineering Kannur, Kerala, India in 2009 and M.Tech degree in Power electronics and Drives from Visvesvaraya National Institute of Technology Nagpur, India in 2012. Currently he is working towards PhD degree in electrical engineering at Visvesvaraya National Institute of Technology Nagpur, India. His research interest includes DC-DC converters for renewable energy sources and power factor correction. H. M. Suryawanshi (SM’06) was born in Nagpur, India, on January 1, 1963. He received the B.E. degree in electrical engineering from Walchand College of Engineering, Sangli, India, in 1988, the M.E. degree in electrical engineering from the Indian Institute of Science, Bangalore, India, in 1994, and the Ph.D. degree from Nagpur University, Nagpur, in 1999. He is currently a Professor with the Department of Electrical Engineering, Visvesvaraya National Institute of Technology, Nagpur. He is currently an associate editor of IEEE TRANSACTIONS ON INDUSTRIAL ELECTRONICS. His research interests include the field of power electronics, emphasizing developmental work in the area of resonant converters, power factor correctors, active power filters, FACTS devices, multilevel converters, and electric drives. Dr. Suryawanshi is fellow of IE(I) and IETE (India). View publication stats A.B. Shitole received B.E degree in electrical engineering from Government College of Engineering Karad, Maharashtra, India in 2008 and M.Tech degree in Power Systems from College of Engineering Pune,India in 2012. Currently he is working towards PhD degree in electrical engineering at Visvesvaraya National Institute of Technology Nagpur, India. His research interest includes control of power converters, multilevel inverters and renewable energy integration.