Printer Friendly

Pulse mask controlled HFAC resonant converter for high efficiency industrial induction heating with less harmonic distortion/ Conversores ressonantes de corrente alternada de alta frequencia controlados por mascara de pulso para aquecimento indutivo industrial de alta eficiencia com baixa distorcao harmonica.


Induction heating (IH) is a non-contact heating process. It uses the high frequency electricity to heat materials that are electrically conductive. Since it is non-contact, the heating process does not contaminate the material being heated. It is also very efficient compared to the other heating methods, since the heat is actually generated inside the workpiece (Acero et al., 2008; Lucia, Acero, Carretero, & Burdio, 2013). This can be contrasted with the other heating methods where heat is generated with a flame or heating element, which is then applied to the workpiece. Clean and fast heat supplied to the workpiece meets the increased requirements with regard to environmental protection (Ahmed & Nakaoka, 2006; Acero et al., 2008). In IH process, the surroundings are not exposed to any thermal and atmospheric pollution. The advantage of this process is producing the heat inside the work piece without the need for any external heat source. For these reasons, induction heating lends itself to some unique applications in industry. Induction heating has been successfully applied to domestic applications due to the advantages of high heating, safety and efficiency (Byun, Choi, Roh, & Hahn, 2000; Meng, Cheng, & Chen, 2011).

High frequency IH system requires specially designed power converters. A large number of inverter topologies have been developed for different applications with the power levels ranging from hundreds of watts to several megawatts for the domestic and industrial applications (Lucia, Burdio, Barra^n, Acero, & Carretero, 2011). There is voltage and current fed high frequency AC (HFAC) inverters to transfer high power to the load. Different inverter topologies such as half bridge, full bridge, and single switch have been proposed for IH applications (Lucia, Burdio, Millan, Acero & Barragan, 2010; Park, Lee, & Hyun, 2007; Booma & Ramareddy, 2013). The choice of topology is mainly based on the cost and performance for specific application.

High quality heating depends on the control of power supplied to the load. On the other hand, the main desired feature of the IH power supply is the cost and efficiency. Half bridge series resonant inverter (SRI) fed by voltage source represents the cost effective solution; however, power control has to be done through the control of variable DC voltage. A bridge rectifier with DC link capacitor has been used conventionally for the variation in DC voltage (Saha, Kurl, Ahmed, Omori, & Nakaoka, 2008). This had problems in size; cost and quality of the supply current. Utility current will have more harmonic distortion. Different power control and regulation strategies have been proposed such as pulse width modulation (PWM), pulse frequency modulation and phase shift control. These power control schemes may cause high magnitude of switching losses, because it is not always possible to turn on or off the switching devices at zero voltage or zero current instants (Lucia, Burdio, Millan, Acero, & Puyal, 2009; Carretero, Lucia, Acero, & Burdio, 2011; Pham, Fujita, Ozaki, & Uchida, 2011). Power control by variable frequency operation (Sarnago, Lucia, Mediano & Burdio, 2013a) has several disadvantages including high electromagnetic interference, poor utilization of the components and complex filtering of output voltage ripple. Fixed frequency control techniques (Sarnago Sarnago, Lucia, Mediano & Burdio, 2013b; Lucia et al., 2013) can overcome the above problems.

The aim of the paper is to propose a fixed frequency pulse mask control technique for HFAC converter for IH system to improve the output power with less harmonic distortion. In this paper, a HFAC converter for IH system with single-phase diode rectifier, a single-phase half bridge inverter with MOSFET as power switches and series IH load is described.

The voltage fed half bridge SRI is considered, since it is the most used topology due to its simplicity and less cost. Induction coil and the workpiece is modeled as series connection of inductor ([L.sub.eq]) and resistor ([R.sub.eq]), based on its analogy with respect to the transformer. Power control is done using the pulse mask scheme.

In the pulse mask scheme, the inverter operation is maintained at resonance, so that the losses are decreased. In conventional methods, with the increased output power, switching losses are increased. Under pulse mask scheme, switching losses are lower and fixed; the total output power of the inverter is increased. This improves the efficiency of the IH generators for wide power variation. It also overcomes the drawbacks of the conventional control modes. Generally, HFAC converters inject harmonics into the utility (Lucia, Carretero, Palacios, Valeau, & Burdio, 2011). The diode bridge rectifier with the input side T filter is considered in this work. It causes lesser harmonic distortion. With the proposed circuit and control scheme, an improvement in output power and lesser total harmonic distortion (THD) at high frequency working conditions can be achieved. The proposed control technique achieves the linear variation in output power, which makes the control algorithm simpler.

Description of HFAC converter and IH system

Figure 1 shows the main block diagram of HFAC power conversion circuit for IH load. The HFAC conversion circuit diagram using half bridge SRI is shown in Figure 2. The single-phase AC supply is given to the uncontrolled rectifier circuit. T filter is used between AC supply and rectifier to reduce THD.



The T filter consists of two inductors [L.sub.T1] and [L.sub.T2] and the capacitor ([C.sub.f]). The rectifier converts AC supply into DC. After the rectifier, DC link capacitor ([C.sub.dc]) is connected in parallel, to filter out the ripple contents available in the DC supply. Then DC is given to the half bridge SRI which consists of two MOSFET switches [Q.sub.1], [Q.sub.2], two anti-parallel diodes [D.sub.1], [D.sub.2] and two resonant capacitors ([C.sub.r/2]) to produce HFAC supply. IH load connected with the inverter receives the supply from the inverter.

Modeling of IH load

IH load consists of a work coil and workpiece as shown in Figure 3(a). Basically, IH load is a transformer representation of the electromagnetic induction action between the work coil (primary) and the load (secondary). It is difficult to measure the transformer parameters. Therefore, it is better to represent the IH load using a simplified series [R.sub.eq][L.sub.eq] model. The transformer representation of the load model is shown in Figure 3(b). Where [L.sub.1] is the inductance of the work coil, [L.sub.2] is the inductance of the work piece, M is the mutual inductance between the primary and the secondary and [R.sub.2] is the resistance of the work piece. The equivalent circuit of the load is shown in Figure 4. The equivalent values of the IH system [R.sub.eq] and [L.sub.eq] are changed by the geometry, load materials, temperature and excitation frequency. These parameter variations make the output power control harder (Lucia et al., 2011). For this reason, a complete analysis for the equivalent parameters of the IH system is provided here. Loop 1 and 2 in Figure 3(b) yield the following voltage equations 1 and 2.

[V.sub.L1] = j[[omega].sub.S][L.sub.1][I.sub.L1] + jM[[omega].sub.s][I.sub.L2] (1)

0 = j[[omega].sub.S]M[I.sub.L1] + ([R.sub.2] + j[[omega].sub.S][L.sub.2])[I.sub.L2] (2)


[I.sub.L1] is the current in the first loop;

[V.sub.L1] is the applied voltage in the loop 1 and;

[[omega].sub.s] is the angular switching frequency.



The load current [I.sub.L2] is obtained from Equation 2 as follows:

[I.sub.L2] = [-j[[omega].sub.s]M[I.sub.L1]/[R.sub.2] + j[[omega].sub.s][L.sub.2] (3)

The equations 1 and 3 give the following equations 4, 5, 6, 7, 8 and 9:

[V.sub.L1] = j[[omega].sub.s][L.sub.1][I.sub.L1] + jM[[omega].sub.s][-j[omega]sM[I.sub.L1]/[R.sub.2] + j[[omega].sub.s][L.sub.2]] (4)

[[V.sub.L1-]/[I.sub.L1]] = [j[[omega].sub.S][L.sub.1]([R.sub.2] + j [[omega].sub.S][L.sub.2]) + jM[[omega].sub.S](-j[[omega].sub.S]M)]/([R.sub.2] + j[[omega].sub.S][L.sub.2]) (5)


[R.sub.eq] = [[omega].sup.2.sub.S][M.sup.2][R.sub.2]/[R.sup.2.sub.2] + [[omega].sup.2.sub.S][L.sup.2.sub.2]


[L.sub.eq] = [L.sub.1] - [[[omega].sup.2.sub.S][L.sub.2][M.sup.2]/[R.sup.2.sub.2] + [[omega].sup.2.sub.S][L.sup.2.sub.2] (9)

The mutual coupling co-efficient (K) and the time constant of the load ([tau]) is given in equations 10 and 11.

K = M/[square root of [L.sub.1][L.sub.2]] (10)

[tau] = [L.sub.2]/[R.sub.2] (11)

From equation 9, the following equation 12 is obtained.

[M.sup.2] = [R.sub.eq]([R.sup.2.sub.2] + [[omega].sup.2.sub.S][L.sup.2.sub.2])/[R.sub.2][[omega].sup.2.sub.S] (12)

Solving 9 and 12 yields the following equations 13, 14 and 15.


[L.sub.2][R.sub.eq] = [R.sub.2] ([L.sub.1] - [L.sub.eq]) (14)

[tau] = [[L.sub.1] - [L.sub.eq]]/[R.sub.eq] (15)

It can be seen from equation 15 that [tau] can be estimated by using [R.sub.eq], [L.sub.eq] and [L.sub.1] From equation 14, equation 16 is obtained as:

[R.sub.2] = [L.sub.2][R.sub.eq]/[[L.sub.1] - [R.sub.eq]] (16)

Solving 9 and 16 yields the following equations 17, 18, 19 and 20:


[R.sup.2.sub.eq] + [[omega].sup.2.sub.S][([L.sub.1] - [L.sub.eq]).sup.2] = [[omega].sup.2.sub.S][M.sup.2]([L.sub.1] - [L.sub.eq])/[L.sub.2] (18)

[M.sup.2]/[L.sub.1][L.sub.2] = [R.sup.2.sub.eq] + [[omega].sup.2.sub.S][([L.sub.1] - [L.sub.eq]).sup.2]/[[omega].sup.2.sub.S]([L.sub.1])([L.sub.1] - [L.sub.eq]) (19)

[??] K = [square root of ([R.sup.2.sub.eq] + [[omega].sup.2.sub.S][([L.sub.1] - [L.sub.eq]).sup.2]/[[omega].sup.2.sub.S][L.sub.1]([L.sub.1] - [L.sub.eq]))]


[[omega].sub.S] = 2 [pi][f.sub.S];

fs is the switching frequency.

The above analysis is used for the design of the circuit parameters. The half bridge SRI is operated at a switching frequency higher than the resonant frequency to achieve ZVS condition. To reduce the switching losses during turn-off, a lossless snubber network ([C.sub.s]) is added (Lucia et al., 2011; Sarnago, Mediano, & Lucia, 2012). This operation mode ensures zero switching losses.

Design of IH load parameters

The design of IH load parameters for the rated power of 500 W is described in this section. The angular resonant frequency ([[omega].sub.r]) of the series resonant circuit is given by equation 21:

[[omega].sub.r] = 1/[square root of [L.sub.eq][C.sub.r]] (21)


[C.sub.r] is the resonant capacitance used to obtain the series resonant condition. The normalized angular switching frequency ([[omega].sub.n]) is expressed as equation 22:

[[omega].sub.n] = [[[omega].sub.s]/[[omega].sub.r]] (22)

The quality factor (QL) of the IH coil is given by equation 23:

[Q.sub.L] = [[omega].sub.r][L.sub.eq]/[R.sub.eq] = 1/[[omega].sub.r][R.sub.eq][C.sub.r] (23)

The output power ([P.sub.o]) of the half bridge inverter fed by a [D.sub.C] voltage ([V.sub.d]) is given by the following equation 24:

[P.sub.o] = 2[V.sup.2.sub.d]/[[pi].sup.2][R.sub.eq](1 + [Q.sup.2.sub.L][([[omega].sub.n] - [1/[[omega].sub.n]]).sup.2] (24)

For the output power [P.sub.o], the [R.sub.eq] of the IH load is given by the equation 25:

[R.sub.eq] = [V.sup.2.sub.eff]/[P.sub.O][Cos.sup.2][theta] (25)

By using the quality factor ([Q.sub.L]) of the resonant circuit, [L.sub.eq] of the heating coil is given by equation 26:

[L.sub.eq] = [Q.sub.L][R.sub.eq]/[[omega].sub.r] (26)

By the definition of the resonant frequency, the resonant capacitor ([C.sub.r]) can be calculated using the following equation 27:

[C.sub.r] = 1/[[omega].sup.2.sub.r][L.sub.eq] (27)

To reduce turn-off losses, a lossless small snubber capacitor ([C.sub.s]) is used with the inverter switch. Using the above equations, calculations of load parameters are made and they are listed in Table 1.

Pulse mask control strategy

Power control is an important goal to be achieved in an IH load to maintain the required temperature. The heating of the work piece can be controlled by controlling the input power to the working coil of the IH load. Conventionally, this is achieved by the control of the voltage fed SRI using pulse width modulation (PWM) technique. The output power [P.sub.o] of the half bridge voltage fed inverter, given by the equation 24, under resonant condition can be written as equation 28:

[P.sub.o] = 2[V.sup.2.sub.d][Cos.sup.2][phi]/[[pi].sup.2][R.sub.eq] (28)

In the conventional PWM based power control, the output power is controlled through PWM duty cycle ([D.sub.PWM]). [D.sub.PWM] is given by the following equation 29:

[D.sub.PWM] = [T.sub.ON]/T (29)


[T.sub.ON] is the turn-on time of the switch and;

T is the total time for one cycle, as shown in Figure 5.


The desired output power ([P.sub.desired]) can be obtained by variation in [D.sub.PWM], as given below as equation 30:

[P.sub.desired] = [P.sub.o][D.sub.PWM] (30)

The [D.sub.PWM] is the control variable for continuous power regulation in PWM method. Hard switching and soft switching transition of the MOSFET switches are shown in Figure 5. During hard switching, both the voltage and current values are not zero, which leads to higher switching losses. However, during the soft switching transition, either the switch voltage or the current becomes zero. In the conventional method, [D.sub.PWM] is varied by varying [T.sub.ON]. The variation in [T.sub.ON] causes hard switching due to violation in ZVS operation, which leads to higher turn-on/off losses and reduced output power.

To minimize the turn off losses, a pulse mask control is proposed in this paper. In the proposed method, for a control cycle [T.sub.c], the inverter transmits power to the load in [T.sub.M] time and it stops working in the remaining ([T.sub.c] - [T.sub.M]) time as shown in Figure 6. The generation of high frequency pulse masked control pulses are presented in Figure 6. Key waveforms under the proposed scheme are presented in Figure 7. Power is injected into the IH load in [T.sub.M] period due to continuous gate pulses. During the period [T.sub.c] - [T.sub.M], zero power is injected into the load due to the masking of pulses. The switches of the SRI are operated above the resonant frequency in order to achieve the ZVS at the turnoff instant. The principle of this scheme is to control the output power [P.sub.o] without changing the turn-on/turn-off instants. Since the switching instants are not changed, the pulse mask scheme offers zero turn-on/off losses. The other advantage of this method is its linear dependency on the output power [P.sub.o]. Gate signals for the switches [Q.sub.1] and [Q.sub.2] are presented in Figure 7 (a). Figure 7(b) shows the wave forms for the output voltage ([V.sub.o]) and output current ([I.sub.o]) in the pulse mask scheme. The output voltage is a discontinous one, while the output current Io is an oscillating one due the high inductance of the IH load. In this paper, the pulse masking modulation index ([D.sub.M]) is considered as control variable. The pulse-masking index [D.sub.M] is given by the following equations 31 and 32:

[D.sub.PDM] = [T.sub.M]/[T.sub.c] (31)

[P.sub.desired] = [P.sub.o][D.sub.M] (32)



The desired power is adjusted by controlling the [D.sub.M]. The variation of [D.sub.M] does not change the switching instant of the MOSFET. Consequently, ZVS at turn-off instant is maintained, which reduces in switching losses. For the complete range of load variation, ZVS condition is not disturbed in the pulse mask control scheme. This improves the output power in the proposed scheme compared to the conventional PWM method.

Results and discussions

Schematic of the voltage fed half bridge SRI is developed for time domain simulation using Matlab simulation tool. Simulation of the proposed converter circuit is carried out for an IH load of 0.5 kW operating at the frequency of 25 kHz. The design specifications and the circuit parameters of the proposed HFAC circuit using the commercial MOSFET and diode modules are listed in Table I. The utility side input voltage of 50 Hz frequency is shown in Figure 8 (a). The DC link voltage and the gate pulses for inverter switch [Q.sub.1] at 50 and 10% [D.sub.M] are shown in Figure 8(b, c and d), respectively. Pulse masked 25 kHz high frequency gate pulses produced by the proposed scheme are of discontinuous manner. The output voltage ([V.sub.o]), output current ([I.sub.o]) of the inverter at the pulse masking modulation index of 50 and 10% are shown in Figure 9 (a, b, c and d), respectively. Since the waveforms are of high frequency, the expanded view of the [V.sub.o] and [I.sub.o] are shown in Figure 9 (e and f), respectively. Due to the variation in [D.sub.M], the average value of voltage [V.sub.o] and [I.sub.o] varies and causes the variation in the output power. The voltage across the power switch [MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII] and current through the switch [MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII] at the [D.sub.M] of 50 and 10% are shown in Figure 9 (g and h), respectively. These waveforms were obtained using simulation. It can be observed from the waveforms that during current rising and falling instants, the switch voltage is zero. These waveforms prove the soft switching operation of the proposed modulation topology. With both the modulation index [D.sub.M], ZVS condition is maintained during turning on/off instants.


To validate the pulse mask scheme in SRI, a prototype model rated for 500 W was fabricated. The schematic diagram for the hardware implementation of the power circuit and the control circuit are shown in Figure 10. The power circuit has a diode bridge rectifier, a half bridge SRI and an IH load. Uncontrolled rectifier was constructed using IN5408 diode switches. A half bridge SRI using four power switches was employed for DC-HFAC conversion. MOSFET of IRF840 switches are used since they can withstand maximum voltage of 500 V and current of 8 A. A copper coil of 8 mm thickness was used to build the work coil with an outer diameter of 110 mm. An iron piece of 100-80-45 mm size has been chosen as workpiece.


The control circuit has PIC16F877A embedded controller, IR2110 driver and (+5V) - (+12V) power supply circuit. Pulse mask control pulses were produced with the embedded controller PIC16F877A. The layout of the hardware prototype is shown in Figure 11 (a). With 100% [D.sub.M], the output 25 kHz frequency signal and the 50 Hz AC signal are presented in Figure 11(b).


The switching pulses for [Q.sub.1] and [Q.sub.2] were produced using microcontroller. For the amplification of the output pulses from the micro controller, IR2110 driver circuit was used. The amplified pulses from the driver are applied to the switches, and they are presented in Figure 11 (c). [V.sub.o] and [I.sub.o] corresponding to [D.sub.M] of 10% are shown in Figure 11 (d) and Figure 12 (a), respectively. The output voltage is of discontinuous manner with the peak amplitude of 47 V and frequency of 25 kHz. The output current was of oscillating nature due to the inductive nature of the load. The peak amplitude of the oscillation was 5.4A with 25 kHz frequency. These experimental results closely agree with the theoretical and simulation results. The voltage across the power switch [Q.sub.1] ([V.sub.Q1]) and current through the switch [Q.sub.1] ([I.sub.Q1]) is presented in Figure 12 (b).

It can be observed from the waveforms that during the turning off transition the switch voltage and current are nearly zero. These waveforms indicate the soft switching operation of the proposed modulation topology. Due to the soft switching operation, the total losses that take place in the inverter switches were reduced, as shown in Figure 13 (a). Total losses were calculated with the difference between input and output power. In the proposed scheme, the switching losses were decreased due to ZVS condition. This leads to increased output power in the pulse mask scheme. The output power variation with the variation in the input power in the conventional and the proposed methods is shown in Figure 13 (b). For the same input power, the output power obtained in the proposed scheme is higher. The proposed control scheme can be easily implemented using the low cost PIC16F877A controller.


The FFT of the utility current with the proposed conversion circuit with and without T filter obtained in the simulation is presented in Figure 14 (a and b), respectively. The presence of input side T filter reduces THD from 27.03 to 2.68%. Thus, the developed pulse masked controlled HFAC voltage fed SRI for IH application had lesser THD and higher output power than the conventional one.





In this paper, constant frequency Pulse mask controlled HFAC power conversion circuit for IH load has been designed, simulated and implemented. The pulse mask control strategy for the HFAC power converter provides ZVS condition for wide-operating range. This converter has advantages, as improved output power with reduced switching losses, linear power variation and low total harmonic distortion. The proposed converter was successfully implemented in hardware using the low cost embedded controller. The hardware results are in good agreement with the simulation results. Further studies should be performed by using phase locked loop based controller for tracking the changes in the load parameters.

Doi: 10.4025/actascitechnol.v28i2.25005


Acero, J., Burdio, J. M., Bagan, L. A., Navarro, D., Alonso, R., Garcia, J. R., ... Garde, I. (2008). The domestic induction heating appliance: An overview of recent research. Proceeding of Applied Power Electronics Conference and Exposition, conference, 651-657.

Ahmed, N. A., & Nakaoka, M. (2006). Boost-half-bridge edge resonant soft switching PWM high-frequency inverter for consumer induction heating appliances. IEE Proceedings of Electric Power Applications, 153(6), 932-938.

Booma, N., & Ramareddy, S. (2013). Design and simulation of energy efficient fixed frequency pulse controlled power converter for induction melting application. Advanced Materials Research, 768(1), 404-410.

Byun, J. K., Choi, K., Roh, H. S., & Hahn, S. Y. (2000). Optimal design procedure for a practical induction heating cooker. IEEE Transactions on Magnetics, 36(4), 1390-1393.

Carretero, C., Lucia, O., Acero, J., & Burdio, J. M. (2011). Phase-shift control of dual half-bridge inverter feeding coupled loads for induction heating purposes. Electronics Letters, 47(11), 670-671.

Lucia, O., Acero, J., Carretero, C., & Burdio, J. M. (2013). Induction heating appliances: towards more flexible cooking surfaces. IEEE Industrial Electronics Magazine, 7(3), 35-47.

Lucia, O., Barragan, L. A., Burdio, J. M., Jimenez, O., Navarro, D., & Urriza, I. (2011). A versatile power electronics test-bench architecture applied to domestic induction heating. IEEE Transactions on Industrial Electronics, 58(3), 998-1007.

Lucia, O., Burdio, J. M., Barragan, L. A., Acero, J., & Carretero, C. (2011). Series resonant multi-inverter with discontinuous-mode control for improved light-load operation. IEEE Tranactions on Industrial Electronics, 58(11), 5163-5171.

Lucia, O., Burdio, J. M., Millan, I., Acero, J., & Barragan, L. A. (2010). Efficiency oriented design of ZVS half-bridge series resonant inverter with variable frequency duty cycle control. IEEE Transactions on Power Electronics, 25(7), 1671-1674.

Lucia, O., Burdio, J. M., Millan, I., Acero, J., & Puyal, D. (2009). Load-adaptive control algorithm of half-bridge series resonant inverter for domestic induction heating. IEEE Transactions on Industrial Electronics, 56(8), 3106-3116.

Lucia, O., Carretero, C., Palacios, D., Valeau, D., & Burdio, J. M. (2011). Configurable snubber network for efficiency optimization of resonant converters applied to multi-load induction heating. Electronics Letters, 47(17), 989-991.

Meng, L., Cheng, K. W. E., & Chen, K. W. (2011). Systematic approach to high power and energy-efficient industrial induction cooker system: Circuit design, control strategy, and prototype evaluation. IEEE Transactions on Power Electronics, 26(12), 3754-3365.

Park, N. J., Lee, D. Y., & Hyun, D. S. (2007). A power-control scheme with constant switching frequency in class-D inverter for induction-heating jar application. IEEE Transactions on Industrial Electronics, 54(3), 1252-260.

Pham, H., Fujita, H., Ozaki, K., & Uchida, N. (2011). Phase angle control of high-frequency resonant currents in a multiple inverter system for zone-control induction heating. IEEE Transactions on Power Electronics, 26(11), 3357-3366.

Saha, B., Kurl, K. S., Ahmed, N. A., Omori, H., & Nakaoka, M. (2008). Commercial frequency AC to high frequency AC converter with boost-active clamp bridge single stage ZVS-PWM inverter. IEEE Transactions on Power Electronics, 23(1), 412-419.

Sarnago, H., Lucia, O., Mediano, A., & Burdio, J. M. (2013a). Modulation scheme for improved operation of a RB-IGBT based resonant inverter applied to domestic induction heating applications. IEEE Transactions on Industrial Electronics, 60(5), 2066-2073.

Sarnago, H., Lucia, O., Mediano, A., & Burdio, J. M. (2013b). Class-D/DE dual mode-operation resonant converter for improved-efficiency domestic induction heating system. IEEE Transaction on Power Electronics, 28(3), 1274-1285.

Sarnago, H., Mediano, A., & Lucia, O. (2012). High efficiency AC-AC power electronic converter applied to domestic induction heating. IEEE Transactions on Power Electronics, 27(8), 3676-3684.

Received on September 20, 2014.

Accepted on October 6, 2015.

Nagarajan Booma * and Sathi Ramareddy

Departamento de Engenharia Eletrica e Eletronica, Centro de Investigacao em Colaboracao com a Universidade de Anna, Faculdade de Engenharia de Jerusalem, Pallikkaranai, Pincode 600100, Chennai, Tamil Nadu, India. *Author for correspondence. E-mail:
Table 1. Design specifications.

Quantity                   Symbol           Values

Power (load)            [P.sub.rated]       0.5 kW
Switching frequency       [f.sub.s]         25 kHz
Resonant frequency        [f.sub.r]         20 kHz
Load inductance           [L.sub.eq        0.6 e-3H
IH load resistance        [R.sub.eq        0.4 Ohms
Resonant capacitor        [C.sub.r]        2200 e-6F
Filter inductor          [L.sub.T1]         0.3 mH
Filter inductor          [L.sub.T2]         0.3 mH
Filter capacitor          [C.sub.f]      100 [micro]F
DC link capacitor        [C.sub.dc]       5 [micro]F
COPYRIGHT 2016 Universidade Estadual de Maringa
No portion of this article can be reproduced without the express written permission from the copyright holder.
Copyright 2016 Gale, Cengage Learning. All rights reserved.

Article Details
Printer friendly Cite/link Email Feedback
Title Annotation:texto en ingles
Author:Booma, Nagarajan; Ramareddy, Sathi
Publication:Acta Scientiarum. Technology (UEM)
Date:Apr 1, 2016
Previous Article:Effect of reversal of the flow direction on hydrodynamic characteristics and plants cultivated in constructed wetland systems/Efeito da inversao no...
Next Article:Principal components in the discrimination of outliers: a study in simulation sample data corrected by Pearson's and Yates's chi-square...

Terms of use | Privacy policy | Copyright © 2021 Farlex, Inc. | Feedback | For webmasters