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61
Chapter 4
SOFT SWITCHED PUSH-PULL CONVERTER WITH
OUTPUT VOLTAGE DOUBLER
S.No. Name of the Sub-Title Page No.
4.1 Introduction……………………………………………………… 62
4.2 Single output primary ZVS push-pull Converter………… 62
4.3 Multi-Output Primary ZVS Push-Pull QRC……………….. 82
4.4 Single output Voltage Doubler ZVS-QRC
Push-pull converter …………………………………………… 86
4.5 Multi-output Voltage Doubler ZVS-QRC Push-pull
converter …………………………………………………………. 96
4.6 Current fed push-pull converter……………………………… 104
4.7 Analysis……………………………………………………………. 125
4.8 Cascoded Transformer Connection ………………………... 127
4.9 Conclusion……………………………………………………….. 129
62
4.1 Introduction
Resonance is introduced in the primary switching circuit of the
push-pull converter to reduce the switching losses in hard switched
converters operating at high frequencies. Soft switching push-pull
converters used for powering applications like robotic arm motor, TTL
logic circuits and CMOS circuits are presented in this chapter. Multi-
output and voltage doubler are also introduced with detailed operating
modes and design procedure. The design is validated through simulation
and experimental results.
4.2 Single Output Primary ZVS Push-Pull Converter
Primary ZVS push-pull converter is introduced in this section.
Detailed explanation of circuit operation and design procedure are also
presented.
4.2.1 Principle of Operation
The ZVS push-pull converter is shown in Fig. 4.1(a). Lr1, Lr2, Cr1,
Cr2 are resonant inductors and resonant capacitors respectively. The
filter components are Lf and Cf. The circuit operation is explained in six
modes under ideal conditions. Fig. 4.1(b) shows the waveforms of gate
pulses for switches S1 (Vg1) and S2 (Vg2), resonant capacitor voltages and
inductor currents respectively under ideal conditions [60].
63
(a)
(b)
Fig: 4.1 (a) Primary ZVS push-pull circuit (b) Idealized Waveforms
4.2.2 Modes of Operation
The operation of the converter is explained in the following six
modes. The assumptions made are:
Magnetising inductance is larger than resonant inductor
All semiconductor switches are ideal
64
Analysis is carried out at steady state
Lossless capacitors and inductors
Output filter capacitor value is assumed to be large
Supply and load are maintained constant
A. Mode 1 (t0 ≤ t ≤ t1): (Power Transfer Interval: Td1 = t1 – t0)
Switches S1 and S2 are OFF at time Td1. Diode D2 present in the
secondary of the circuit is forward biased, while D1 is reverse biased.
During this interval, power is transferred from primary to secondary. The
conduction path and the operating region of the interval Td1 is
highlighted in Fig. 4.2(a) and Fig. 4.1(b).
It can be noticed from Fig. 4.1(b) that the resonant capacitor
voltage Vcr1 is charging from 0 to 2Vdc and Vcr2 is discharging from 2Vdc to
0. Resonant inductor current iLr1 is maintaining its charge (constant
current source) and resonant inductor current iLr2 is negatively charging.
The equation governing this mode is consolidated with its initial and final
conditions and is presented in Table 4.1.
B. Mode 2 (t1 ≤ t ≤ t2): (Resonant Transition Interval 1: Td2 = t2 – t1)
When S2 is turned ON, the interval Td2 starts and S1 is in OFF
state. D1 in the secondary circuit is forward biased whereas D2 is reverse
biased. This period is called resonant transition interval 1 since the
resonance of the converter begins in this phase.
65
Resonant inductor Lr1 and resonant capacitor Crl form the resonant
circuit. In this interval, energy from the resonant inductor is transferred
to the resonant capacitor, leading to the overcharging of the capacitor to
a value of 2Vdc + ImZo/2. Conduction path and operating region of the
interval Td2 are shown in Fig. 4.2(b) and 4.1(b).
(a) Mode 1 (b) Mode 2
(c) Mode 3 (d) Mode 4
(e) Mode 5 (f) Mode 6
Fig: 4.2 Equivalent circuits of the ZVS PWM push-pull converter
66
At t = t2, ILrl value reaches zero and the voltage Vcrl reaches its peak
value. Resonant inductor current, iLr1 discharges positively while iLr2
discharges negatively.
C. Mode 3 (t2≤ t ≤ t3): (Resonant Transition Interval 1: Td3 = t3 – t2)
In interval Td3, S1 and S2 conditions are the same as that of mode 2
(S1 is OFF and S2 is ON). Secondary diodes D1 and D2 are forward and
reverse biased respectively. As the resonance is maintained, this interval
is also known as resonant transition interval 1. Fig. 4.2(c) shows the
conduction path for the interval Td3. Fig. 4.1(b) shows the resonant
capacitor voltages Vcr1 discharging from 2Vdc + ImZo/2 to 2Vdc and Vcr2 is
0. Resonant inductor currents are charged in opposite directions and
energy transfer is same as that of the second interval. When voltage
across the resonant capacitor VCr = 2Vdc, resonance between Lr and Cr
ends.
D. Mode 4 (t3≤ t ≤ t4): (Power Transfer Interval: Td4 = t4 – t3)
In the fourth interval Td4, both S1 and S2 are OFF, D1 is forward
biased and D2 is reverse biased in the secondary. This mode also
transfers power similar to mode 1. The conduction path for the interval
Td4 is shown in Fig. 4.2(d). The resonant capacitor voltage Vcr1 discharges
from 2Vdc to 0, Vcr2 charges from 0 to 2Vdc. In this interval, resonant
inductor current iLr1 increases negatively but the resonant inductor
current iLr2 remains constant.
67
Table 4.1 Mode equations
Mode Formula Initial Condition Final condition
Mode 1
( ) ( )
=
,
( )
Vcr2 = 2Vdc ( ) ( ) ( )
Mode 2
( )
( ) ( )
( )
ILrl( ) ( )
( )
( ) ( )
( )
( )
( )
( )
Mode 3
( )
( )
( )
( )
( ) ( )
( )
( )
( ) ( )
( )
(
) (
) ;
; (
) ( )
( )
( )
( )
( ) ( ) ( )
Mode 4
( )
( )
( ) ( )
( ) ( )
68
E. Mode 5 (t4≤ t ≤t5): (Resonant Transition Interval 2: Td5 = t5 – t4)
In interval Td5, S1 is ON and S2 is OFF, D2 is forward biased and D1
is reverse biased in the secondary. This mode is called resonant transition
interval 2. Fig. 4.2(e) shows the conduction path while Fig. 4.1(b) details
the charging of Vcr2 from 2Vdc to (2Vdc + ImZo/2) and Vcr1 = 0. The
resonant inductor current iLr1 decays to zero towards positive and
decays to zero towards negative.
F. Mode 6 (t5≤ t ≤ t6) (Resonant Transition Interval 2: Td6 = t6 – t5)
In interval Td6, S1 is ON and S2 is OFF. The secondary working is
same as that of the previous mode. This mode is also known as resonant
( )
( )
( )
( ) ( )
(
) (
)
Mode 5
( ) ( ( )
)
( )
( )
[
] ( )
( ) ( )
Mode 6
( ) ( )
[
] ( )
( ) ( )
69
transition interval 2. The conduction path and the region of operation are
shown in Fig. 4.2(f). Resonant capacitor voltage Vcr1 is 0 and Vcr2
discharges from 2Vdc + ImZo/2 to 2Vdc as shown in Fig. 4.1(b). Resonant
inductor current, iLr1 charges positively and iLr2 charges negatively.
When the sixth mode ends, a new cycle repeats.
4.2.3 Design
The specifications and the design aspects of the power supply are
discussed in detail in this section.
4.2.3.1 Specifications
Converter Specifications:
Switching frequency (fs) = 50 kHz
Input Voltage (Vdc) = 15 V
= 0.4
Resonant frequency (f0) = 125 kHz
DC Motor Specifications:
Output power (Po) = 5 W
Output Voltage (Vo) = 5V
Output Current (Io) = 1A
Speed = 95rpm
Torque = 0.5Nm
70
4.2.3.2 Converter Design
The design of 5W, 50 kHz ZVS push-pull converter is given below:
Voltage conversion ratio, M
= 0.2898
= 0.39 (max value of M is chosen)
Where, Vsmin and Vsmax are minimum and maximum supply voltages
respectively.
Magnetizing current, ( ) = 1.39 (4.1)
i) Resonant Condition
Condition for ZVS is
;
21.47 = 25 Ω (chosen)
Characteristic impedance, √ (4.2)
Resonant frequency, =
ii) Resonant component calculation
Resonant frequency,
√ (4.3)
Resonant capacitor, = 0.048 = =
Resonant inductor, = 45 = =
Angular resonant frequency,
√ (4.4)
71
iii) Filter inductor and Capacitor design
Cut-off frequency,
Filter capacitor, = 220
Filter inductor, = 4.7
4.2.3.3 Transformer and Inductor Design
Design of transformer and inductors are carried out as per the
design elaborated in section 3.3.1.4 and the results obtained are
tabulated in Table 4.2.
Table 4.2 Transformer and Inductor design details
Parameters Core selected
Transformer design
Np = 12
From Appendix –I : core - EE 20/10/5
,
,
From Appendix –II : SWG = 28 (
), SWG =24 ( )
Resonant Inductor Design
From Appendix –I : core - EE 20/10/5
,
,
From Appendix –II : SWG =19 ( )
Filter Inductor Design
, ,
From Appendix –I : core - EE 20/10/5
From Appendix –II : SWG=24 ( )
4.2.3.4 Motor speed calculation
The motor specifications (section 4.2.3.1) reveal that the motor
develops a torque of 0.5Nm for an input power of 5W.
72
Torque = 0.5 Nm
The motor used in robotic applications has less inertia, negligible iron
and friction losses. For this lossless machine, power input = power
output.
Output power of the converter (Po) = Input power to the motor = 5W
Motor Power output = Torque * Speed in rad/sec
Therefore, Speed = 5 /0.5 = 10 rad/sec = 95.5rpm
The simulation and hardware results of the converter with this
robotic arm motor specification are explained in sections 4.2.4 and
4.2.6.2 respectively.
4.2.4 Open-loop Simulation Results
The simulation was carried out with the designed values and the
circuit diagram of the simulated circuit for a robotic arm application is
shown in Fig. 4.3(a). The resonant waveforms obtained, illustrated in Fig.
4.3(b), are similar to the theoretical waveforms shown in Fig. 4.1(b). The
figure clearly confirms ZVS turn ON for both switches. It is further
observed that the peak resonant capacitor voltage across each switch is
45V and 42V respectively. The output voltage 5V, output current-1A and
speed of 98rpm obtained, is shown in Fig. 4.3(c). Thus the simulation
confirms that the converter is well suited for powering a robotic arm
controlled by a motor of 5W, 0.5Nm, 10rad/sec specifications.
73
(a)
(b) (c)
Fig: 4.3 Primary ZVS Push-pull QRC fed servo motor (a) Simulation
circuit (b) Resonant waveforms (c) Motor inputs and outputs
4.2.5 Closed loop Simulation Results
The closed loop simulations are carried out for electronic PI
controller and Enhanced PID Controller and the results obtained are
discussed in this section for a single output converter.
74
4.2.5.1 Electronic PI Controller
The designed primary ZVS push-pull converter is simulated in
PSIM for the specifications stated in section 4.2.3.1. A PI Controller has
the properties of P and I controllers and is widely used in DC–DC
converter fed servo control applications. The equation which describes PI
controller is,
u(t) = KP e(t) + KPKI ∫e(t) dt (4.5)
Where, u(t) – output signal , e(t) – error input , KP – proportional
constant, KI – integral constant.
Proportional controller is described by the value of its proportional
gain Kp. The integral term of a PI controller varies the output as long as
there is a non-zero error. Therefore such a controller can eliminate even
a small error. An electronic PI controller designed for the primary ZVS
push-pull converter with OP-AMPs is shown in Fig. 4.4(a). The circuit
comprises of a difference amplifier, PI Controller, non–inverting amplifier
and a PWM generator. The design equations are as given below:
For P – Proportional Controller,
output voltage Vo =
Ve (4.6)
For I – Integral Controller,
output voltage Vo =
∫ dt (4.7)
The effect on the load change is depicted in Fig. 4.4(b). From the figure it
is clear that, for the load change applied at 1.5 seconds, the output
75
voltage is regulated and its corresponding change is observed in the
current waveform. Fig. 4.4(c) shows the resonant waveforms, which is
similar to the theoretical waveforms in Fig. 4.1(b).
(a)
(b) (c)
Fig: 4.4 ZVS Push-pull converter using PI Controller (a) Closed loop
simulation circuit (b) Output waveforms (c) Resonant waveforms
4.2.5.2 Enhanced PI Controller (EPI)
Closed loop simulation is carried out with PID, PI, EPID and EPI
controllers to analyse the performance of the controllers. The error,
76
which is the difference between the measured output voltage and the
desired set point, is fed to the PID controller. The controller processes the
error and produces output which further reduces the error. Based on the
nature of the system, the proportional, derivative and integral constants
are chosen. The constants chosen react on the present error, cumulative
errors and rate of change of error, respectively. The controller output is
the weighed sum of all these three actions. The output is variable in
nature, which in turn varies the pulse width of the PWM thus controlling
the switch. The enhanced constants b and c of the Enhanced PID
controller (EPID) helps in improving the performance of the controller by
reducing the peak overshoot and settling time of the output, without
affecting the PI parameters. The value of the enhanced constants varies
between 0 and 1.
Fig. 4.5(a) and (b) reveal the PSIM simulation diagram of the PID
and EPID controlled converter. The closed loop output response of the
EPID controller for 2Ω change (both increase and decrease) is shown in
Fig. 4.5(c) and (d) respectively. From the figures, it is observed that the
voltage is regulated at the rated value for both increase and decrease in
load, and Table 4.3 gives the comparison of various controllers with
respect to peak time, settling time etc. Observations are carried out for a
load variation of ±50% and the resonant waveforms for the same are as
shown in Fig. 4.6(a) and (b).
77
(a) (b)
(c) (d)
Fig: 4.5 Closed loop simulation circuit of ZVS Push-pull converter using (a) PI Controller (b) EPID Controller (c) & (d) Output voltage and current
for ± 20% load variation with EPID controller.
The equations governing the controllers are:
PID Controller, ( ) ∫( ) ( )
EPI Controller, ( ) ∫( )
EPID Controller, ( ) ∫( ) ( )
Efficiency = ( )
( ) (4.8)
Where, P - Controller output, Ysp - desired set point, Y - Measured
output voltage, KD - differential constant, b and c are enhancement
78
constants, ( ) - error input e(t), ( ) &( ) are
the average output and input voltages and currents
respectively.
(a)
(b)
(c)
Fig: 4.6 Voltage and current waveforms for load change within ± 50% with EPID controller (a) Switch-1 (b) Switch-2 (c) Efficiency graph.
It is observed that the shape of the resonant voltage and current
waveforms prevail throughout the ±50% load changes and the peak
voltage and current are in the range of 45V to 50V and 0.8 to 0.9A. The
79
efficiency graphs shown in Fig. 4.6(c) are plotted for an input voltage of
14V, 15V and 16V and the maximum efficiencies (equation 4.8) noted
from the graphs is 84.54%, 85.53% and 86.16% at 5W output power
respectively.
Table 4.3 Time domain analysis
Parameters Controllers
PID EPID EPI PI
Before Load Change
Peak time (tp in msec) 0.370 0.326 0.352 0.353
Peak Overshoot (V) 5.216 5.213l 5.213 5.215
Settling time (ts in sec) 0.223 0.190 0.19 0.190
After load change
Peak Overshoot (V) 5.932 5.932 5.988 5.978
Peak time (tp in msec) 0.049 0.0366 0.039 0.0366
Settling time (ts in sec) 7.96 7.9276 8.17 8.37
A comparison Table 4.3 is tabulated for analysing the closed loop
response of PID, PI, EPID and EPI controllers. From the table it is
obvious that the response of EPID have less peak time, settling time, less
overshoot and faster response. Therefore, it is the best option for
switched mode power supplies with stringent regulation. The enhanced
coefficients introduced improve the dynamic response of the system by
reducing the error at a faster rate.
The standard power supply data sheet for avionics, mobile, ground
systems and other applications are given in Appendix VI and the
important parameters are listed in Table 3.4. The inference from
standard military power supply table 3.4 is load overshoot: 400mV.
While that obtained from EPID controller is 932mV; comparing these
80
values it is clear that the overshoot is large in the EPID controller output
and could be reduced by tuning the EPID constants values.
4.2.6 Experimental implementation
The designed converter is implemented in hardware and the
implementation particulars are detailed below.
4.2.6.1 PWM Generation
The pulses for the switches are generated from DSPIC30f4011. TTL
of 0-5V is used by typical logic systems such as micro controllers. TTL’s
cannot supply enough current to switch a high power MOSFET ON and
OFF. In order to perform high speed switching most MOSFET’s are
activated with pulses of amplitude 12-20V and with a higher current.
Hence, a MOSFET driver is an essential interface between logic system
and MOSFET. The pulses are amplified to a range of 12V to 15V and
isolated before being fed to the switches with the help of an opto-coupler
cum driver IC TLP250 as shown in Fig. 4.7.
Fig: 4.7 Gating Pulse from opto-coupler IC TLP250
81
4.2.6.2 Power circuit Results
Fig. 4.8(a) and (b) show the resonant capacitor voltages (VCr1-pk =
46V, VCr2-pk = 37.8V) with gate pulses of switches S1 and S2. For a rated
supply voltage of 15V and load resistance of 5Ω the output voltage (4.8V)
and output current (1A) of the ZVS push-pull converter obtained is
presented in Fig. 4.9(a) and (b) respectively. The complete hardware set
up of the converter is represented in Fig. 4.9(c).
(a) (b)
Fig: 4.8 (a) Resonant capacitor-1 voltage with gate pulse-1 (b) Resonant capacitor-2 voltage with gate pulse-2
(a) (b) (c)
Fig: 4.9 (a) Output voltage and current (b) Supply voltage and current
(c) Hardware setup
The ripples observed in Fig 4.9(b) are due to the combined effect of
supply voltage ripples at 100Hz (push-pull converter has full wave
82
rectification at output (i.e.) 100Hz) and switching frequency ripples at 50
kHz. This could be eliminated by adding a filter at the input of the
converter.
4.3 Multi-Output Primary ZVS Push-Pull QRC
To increase compactness, the primary resonant converter dealt
above is implemented for multi-output operations. The operation and
design procedure of a 6.2W, 50kHz multi-output primary ZVS push-pull
converter is explained in this section. In order to validate the design
procedure, the simulation and experimental results are presented and
analysed in detail.
4.3.1 Principle of Operation
The multi-output ZVS push-pull converter is shown in Fig. 4.10.
The resonant inductors and resonant capacitors are Lr1, Lr2 and Cr1, Cr2
respectively and filter components are Lf and Cf. Primary resonance is
similar to single output topology; with 6 modes, the ideal operation of the
circuit is same as explained in section 4.2.2.
Fig: 4.10 ZVS multi-output push-pull circuit
83
The waveforms for switch pulses for S1 and S2, resonant capacitor
voltages and resonant inductor currents are same as illustrated in Fig.
4.1(b).
4.3.2 Design
The design procedure is same as explained in section 4.2.3. The design
parameters for primary ZVS multi-output converter are described in this
section.
4.3.2.1 Specifications
Switching frequency (fs) = 50kHz
Output power (Po) = 6.2W
Input Voltage (Vdc) = 15 V
Output Voltage-1(Vo) = 2V
Output Current-1(Io) = 0.6A
Output Voltage-2(Vo) = 10V
Output Current-2(Io) = 0.5A
4.3.2.2 Converter Design
The design parameters required for the multi-output converter is
same as that explained in section 4.2.3.2.
4.3.2.3 Transformer and Inductor Design
The design of the transformer, resonant inductor and filter
inductor are same as explained in section 4.2.3.3 and the results
84
obtained are same as tabulated in Table 4.2, except for the secondary
turns in the transformer (i.e) number of turns in secondary-1 is 7 and
secondary-2 = 14
4.3.3 Open-loop Simulation Results
With the designed values the converter is simulated in PSIM
software and the simulation results are analysed in this section for a
resistive load. The two output voltages obtained 2.1V and 10V at rated
supply (15V) and load condition (7Ω & 20Ω), are as shown in Fig. 4.11(a).
The two resonant capacitors’ peak voltages and currents obtained are
60.10V and 1.93A, 55.29V and 1.46A respectively and are shown in Fig.
4.11(b).
. (a) (b)
Fig: 4.11 (a) Output voltages and currents (b) Resonant waveforms
4.3.4 Experimental Results
Fig. 4.12 and 4.13 show the hardware implemented waveforms of
the designed converter. Fig. 4.12(a) and (b) show the resonant capacitor
85
voltages (VCr1-pk = 19.4V, VCr2-pk = 17.8V) with the gate pulse of both the
switches S1 (39.5%) and S2 (41.3%). The output voltage-1 (1.9V), current1
(638mA), voltage-2 (10.1V) and current-2 (531mA) of the ZVS push-pull
converter are shown in Fig. 4.12(c) and 4.13(a), and the complete
hardware set up of the converter is shown in Fig. 4.13(b). The ripples
observed in output voltage and current (Fig 4.12(c)) are due to the
combined effect of ESR and ESL of the output electrolytic capacitor. This
can be reduced by adding a non-electrolytic capacitor (0.47µF) at the
output of the converter.
(a) (b) (c)
Fig: 4.12 (a) and (b) Resonant capacitor voltages with corresponding gate pulses (c) Output-1 voltage and current.
(a) (b)
Fig: 4.13 (a) Ouput-2 voltage and current (b) Hardware Setup.
86
The converters explained in sections 4.2 and 4.3 deals with the
resonance in the primary circuit alone, while the secondary diodes
experience high surge due to transformer leakage inductance. This issue
is addressed in the next section.
4.4 Single Output Voltage Doubler ZVS-QRC Push-Pull Converter
The primary resonant converters dealt in the above two sections for
single and multi-output converters do not engross energy stored in the
leakage inductance which appear as voltage stress in the secondary
diodes; hence resonance is introduced in the secondary circuit to
reduces the losses in the passive switches. This resonant circuit also
serves the purpose of voltage doubling at the output, thus increasing the
voltage at the output with less component count.
4.4.1 Voltage Doubler Circuit
It is an electronically controlled circuit which charges the capacitor
from input voltage through switches. The advantages of this circuit are -
it is more adaptable to changes, easy to implement, economical and can
obtain an output which is an odd or even multiple of the input voltage.
The basic doubler circuit is shown in Fig. 4.14(a). The advantages are:
It clamps the voltage stress on secondary diodes D1 and D2 to V0.
The rectifier does not need a RC snubber and hence it can obtain a
high efficiency and low noise output voltage.
87
The conduction loss can be minimized by including a rectifier diode of
low voltage rating, which leads to simplified structure.
(a) (b)
Fig: 4.14 (a) Voltage doubler circuit (b) Circuit diagram of the push-pull ZVS-QRC with output voltage doubler.
4.4.2 Principle of Operation
The circuit diagram of the ZVS push-pull QRC with secondary
voltage doubler is as shown in Fig. 4.14(b). The primary circuit working
is similar to the primary ZVS push-pull QRC, as explained in section 4.2,
with an added feature of secondary ZCS in the rectifying diodes (D1 and
D2). The switches (S1 and S2) are switched ON one after the other, so that
the transformer does not saturate but is excited in both the directions,
hence increasing the transformer utilization factor. The magnetizing
inductance is assumed to be large so as to maintain continuous
conduction even at light load conditions. The resonant circuit is formed
with resonant inductors (Lr1 & Lr2) and resonant capacitors (Cr1& Cr2) to
achieve ZVS in the main switches. The theoretical waveform [60] is as
presented in Fig. 4.15.
88
4.4.3 Modes of Operation
The CCM operation of the converter is explained in 6 modes as
illustrated in Fig. 4.16(a) – (f). The assumptions were discussed earlier in
section 4.2.2.
A. Mode 1 (t0 ≤ t ≤ t1): (Power Transfer Interval: Td1 = t1 – t0)
Upper limb: Mode 1 starts with an initial condition of ILr1 = Im/2. During
this interval (Td1), the main switches are in the OFF condition. The
resonant inductor acts as a constant current source with some initial
charge and charges the resonant capacitor voltage from 0 to 2VS. The
diode D2 in the secondary is forward biased while D1 is reverse biased.
Power is transferred from primary to secondary and charges the
secondary resonant capacitor. The filter capacitor supplies the load.
Lower limb: Same as the working of the upper limb in mode 4. The
energy stored in the transformer leakage inductance is discharged to
charge the secondary resonant capacitor.
B. Mode 2 (t1 ≤ t ≤ t2): (Resonant Upper Transition Interval 1: Td2 = t2
– t1)
Upper limb: The initial conditions for this interval (Td2), are Vcr1(0) = 2VS ,
ILr1(0) = Im/2. This mode begins when S2 is turned ON, S1 is OFF and
diodes D1 and D2 are forward biased and reverse biased respectively. The
resonant capacitor is charged by the resonant inductor to (2VS + ImZo/2)
from 2VS for a duration of Td2/2. The overcharged capacitor in turn
89
charges the resonant inductor in the reverse direction for the remaining
Td2/2 duration. This interval is called resonant upper transition interval 1,
as resonance occurs in this mode. This mode ends when the resonant
capacitor voltage reaches 2VS.
Lower limb: Working is same as upper limb in mode 5. The secondary
circuit is the same as in the mode explained before.
Fig: 4.15 Idealised resonant waveforms of primary ZVS push-pull
converter with output voltage doubler
C. Mode 3 (t2≤ t ≤ t3): (Resonant Upper Transition Interval 1: Td3 = t3 – t2)
Upper limb: The initial conditions for this mode are Vcr1(0) = 2VS . During
this interval (Td3), S1 is OFF and S2 is ON, diode D1 is forward biased and
90
diode D2 is reverse biased. The resonant capacitor discharges and Vcr1
decreases from 2Vs to 0. Resonant inductor current, iLr1 increases linearly
from a negative value at t = t2 and reaches -Im/2 at t = t3. Energy transfer
from resonant capacitor to resonant inductor is observed in this mode.
Lower limb: Working is the same as that of upper limb in mode 6. The
energy stored in the capacitance is discharged back to the transformer
secondary and the load.
D. Mode 4 (t3≤ t ≤ t4): (Power Transfer Interval: Td4 = t4 – t3)
Upper limb: The initial conditions for this mode are Vcr1(0)=0 and ILr1(0) =
-Im/2. In this interval (Td4), S1 and S2 are OFF; D1 is forward biased while
D2 is reverse biased. This interval is similar to mode 1 and is known as
power transfer interval. The resonant capacitor voltage Vcr1 is 0 during
this period and the resonant inductor current iLr1 discharges negatively
through the switch diode.
Lower limb: Its working is same as that of upper limb in mode 1. The
energy stored in the transformer leakage inductance is discharged to the
load, charging the secondary resonant capacitor in the negative direction.
E. Mode 5 (t4 ≤ t ≤t5): (Resonant Lower Transition Interval 2: Td5 = t5 –t4)
Upper limb: The initial condition for this mode is ILr1(0) = -(Im/2)cosα. In
this interval (Td5), S1 is turned ON and S2 is OFF, D2 is forward biased
and D1 is reverse biased. Resonant inductor current iLr1 decreases
linearly, reaches 0 and charges positively; hence it is known as resonant
91
lower transition interval 2. As the lower limb resonance ends, mode 5
terminates.
Lower limb: Primary circuit working is similar to that of the upper limb in
mode 2. The secondary circuit works in the same manner as in mode 4.
(a) Mode 1 (b) Mode 2
(c) Mode 3 (d) Mode 4
(e) Mode 5 (f) Mode 6
Fig: 4.16 Modes of operation
92
F. Mode 6 (t5≤ t ≤ t6) (Resonant Lower Transition Interval 2: Td6 = t6 –
t5)
Upper limb: In interval (Td6), switch S1 is turned ON and S2 is OFF, D2 is
forward biased and D1 is reverse biased. Voltage across the resonant
capacitor Vcr1 = 0, resonant inductor is positively charged and its
corresponding current iLr1 increases linearly from a positive value at t = t5
to Im/2 at t = t6.
Lower limb: Working is same as the upper limb of mode 3. The energy
stored in the capacitance is discharged back to the secondary circuit.
The next cycle starts and same operation continues at the end of this
mode.
4.4.4 Design
The specifications and the design aspects of the power supply are
discussed in this section.
4.4.4.1 Specifications
Switching frequency (fs) = 50kHz
Output power (Po) = 1.32W
Input Voltage (Vdc) = 15 V
Output Voltage (Vo) = 3.3V
Output Current (Io) = 400mA
= 0.4
93
4.4.4.2 Converter Design
The design of 1.32W, 50kHz ZVS push-pull converter with
secondary voltage doubler is as given below:
Voltage conversion Ratio, M
= 0.191
= 0.26 (max value of M is chosen)
Magnetizing current, ( ) = 1.26
This design is similar to the design explained in section 4.2.3; the
designed values are: = 0.048 , = 45 , = 220 , = 4.7 .
4.4.4.3 Transformer and Inductor Design
The design of the transformer, resonant inductor and filter
inductor is carried out. The design is same as explained in section
4.2.3.3 and the results obtained for the inductors are same as tabulated
in Table 4.2, while that for the transformer is tabulated in Table 4.4.
Table 4.4 Transformer design
Parameters Core selected
Np = 12Turns
From Appendix –I : core - EE 20/10/5
,
,
From Appendix –II : SWG = 28 ( )
SWG =24 ( )
94
4.4.5 Open-loop Simulation Results
Open loop simulation of the converter shown in Fig. 4.14(b) is
carried out in PSIM. The obtained output voltage (3.3V) and current
(400mA) are shown in Fig. 4.17(a) for rated supply (15V) and load
conditions (8Ω). The peak voltage (78V) across both the resonant
capacitors is as shown in Fig. 4.17(b). It can be observed that it is similar
to that of the theoretical waveform shown in Fig. 4.15. It also confirms
the turn ON ZVS in the active switches. The peak voltage across the
rectifier diodes are VD1 = VD2 = 5V and the rectifier diode peak currents
are iD1 = iD2 = 3A as shown in Fig. 4.17(c). From this, it is observed that
there is no oscillation or voltage spike on the rectifier diodes.
(a) (b) (c)
Fig: 4.17 Simulation waveforms of (a) Output voltage & current (b) Resonant capacitor voltages with gating pulses (c) Diode current &
voltages
4.4.6 Experimental Results
A prototype converter with 1.32W output power (3.3V, 400mA) is
developed to verify the operating principle of the single output ZVS-QRC
95
Push-pull converter with voltage doubler. The different devices used in
the converter are: S1 and S2: IRF840, D1 and D2: Fast recovery schottky
diodes BA159 (Detailed in Appendix-IV), dsPIC30f4011 is used for
generating pulses, Driver cum isolator: TLP 250 (Detailed in Appendix-V).
Fig. 4.18 shows the experimental results for full load condition.
The nominal converter output voltage (VO), current (IO) are as shown in
Fig. 4.18(a) and the gating pulses derived from driver circuit are as
shown in Fig. 4.7. Fig. 4.18(b) & (c) present the resonant capacitor
voltages Vcrl and Vcr2.
(a) (b) (c)
Fig: 4.18 (a) Output voltage & current (b) & (c) Resonant capacitor voltages with gating pulses
From the figure it is observed that the switches S1 and S2 are
turned ON when voltages Vcrl and Vcr2 become zero respectively. Also it is
observed that these waveforms are similar to the theoretical waveforms
shown in Fig. 4.15 and the simulated waveform shown in Fig. 4.17(b).
The rectifier diode currents iD1 and iD2 are also obtained and it is
observed that it does not have any oscillation or voltage spikes. The
96
pulses obtained from the DSPIC30f4011 is isolated and amplified in the
opto-coupler circuit to 12.4V approximately. This pulse triggers the
voltage controlled device (MOSFET IRF840). The resonant capacitor
voltage obtained for switch- 1& 2 are 60V and 62V respectively, while in
simulation it is 78V for both capacitors. This difference in voltage
magnitude between the simulation and hardware results is due to the
fact that the devices and capacitors used in the simulation are ideal. The
switching frequency of the prototype is 50kHz and therefore the size of
the components used is reduced to ¼th the original size.
4.5 Multi-Output Voltage Doubler ZVS-QRC Push-Pull
Converter
This section discusses the multi-output ZVS push-pull converter
with a secondary voltage doubler. This converter further adds the
advantage of compactness and multiple isolated outputs to the single
output converter mentioned in section 4.4, by adding one extra winding
to the secondary of the transformer. Operation of the circuit is explained
in detail and the design procedure is also presented. The closed loop
hardware results obtained are also discussed.
4.5.1 Principle of Operation
Fig. 4.19 shows the designed ZVS multi-output push-pull
converter with secondary voltage doubler. Lr1, Lr2 and Cr1, Cr2, Cr3, Cr4
97
are resonant inductors and resonant capacitors respectively. Lf1, Lf2 and
Cf1, Cf2 are the filter components. Resonance occurs on both sides of the
converter; namely: in primary between (Lr1 & Cr1) and (Lr2 & Cr2), in
secondary-1 between the magnetizing inductance of secondary-1 & Cr3,
and in secondary-2 between magnetizing inductance of secondary-2 &
Cr4.
Fig: 4.19 ZVS multi-output quasi resonance push-pull converter with
output voltage doubler
4.5.2 Modes of Operation
Idealized operation and waveforms of the multi-output circuit is
similar to single output converter explained in section 4.4.3 and is
depicted in Fig. 4.15.
4.5.3 Design
Specifications and the design aspects of the power supply are
discussed in this section.
98
4.5.3.1 Specifications
Switching frequency (fs) = 50kHz
Output power (P0) = 3.6W
Input voltage (Vdc) = 15±15%
Output voltage-1 (V01) = 5V
Output current-1 (I01) = 0.5A
Output voltage-2 (V02) = 3.3V
Output current-2 (I02) = 0.33A
4.5.3.2 Converter Design
Sample design of 3.6W, 50 kHz multi-output ZVS push-pull
converter is listed below: Magnetizing current, Im = I0 (M+1) = 0.745A
i) Resonant Condition
The design is similar to the design details explained in section
4.2.3. Using equation (4.2), the characteristic impedance is calculated as
Z0 = 40.
ii) Resonant component calculation
Using equations (4.3) and (4.4), the resonant components are
calculated as - resonant capacitor Cr = 0.33µF and resonance inductor
Lr = 60µH.
iii) Filter inductor and Capacitor design
It is similar to the design explained in section 4.2.3.2 and the designed
values are: filter capacitor Cf = 220µF and filter inductor Lf = 10µH.
99
4.5.3.3 Transformer and Inductor Design
Design of the transformer and inductors are carried out as per the
design elaborated in section 3.2.1.4 and the results obtained are
tabulated in Table 4.5.
Table 4.5 Transformer and Inductor design details
Parameters Core selected
Transformer design
Np = 8
From Appendix –I : core - EE 20/10/5
,
,
From Appendix –II : SWG =29 ( ), SWG =35
( ), SWG =27 (
) Resonant Inductor Design
E = 235× 10-6 J
a 0.44 mm2
N 14 turns
From Appendix –I : Core – EE 25/9/6 AP = 3120mm4, Ac = 40mm2, Aw = 78mm2
From Appendix –II : SWG = 21 (a= 0.51890 mm2)
Filter Inductor Design
a 0.5234mm2
N 6 turns
From Appendix –I : Core- EE 22/10/5 AP = 1418mm4, Ac = 31mm2, Aw = 47.8mm2
From Appendix –II : SWG = 20 (a= 0.65670 mm2)
4.5.4 Simulation Results
The simulation of the circuit is carried out in PSIM and the
simulated waveforms for the converter are revealed in Fig. 4.20 and Fig.
4.21. The resonant voltages and currents obtained are displayed in Fig.
4.21(a) & (b) while the output voltage and current obtained (5V, 0.5A)
and (3.3V, 0.33A) are exhibited in Fig. 4.20. The secondary diode
currents and voltages are illustrated in Fig. 4.21(c).
100
(a) (b)
Fig: 4.20 Output voltages and currents
4.5.5 Experimental Results
Hardware implementation of multi-output push-pull converter is
carried out for both open loop and closed loop with controller IC UC3825.
The results obtained from the hardware implementation are presented
and discussed in detail.
(a) (b) (c)
Fig: 4.21 (a) Primary resonant waveforms (b) Secondary resonant
waveforms (c) diode waveforms
101
4.5.5.1 PWM Controller
The pulses obtained from opto-coupler circuit have a frequency of
50kHz and a duty ratio of 40%. Peak voltage of the obtained pulses is
found to be 14V. The duty ratio and frequency remains the same as
obtained from IC UC3825. The implementation details and design of the
IC components are same as explained in sections 3.4.1 to 3.4.3 and the
pulse obtained is same as shown in Fig. 3.8.
4.5.5.2 Rated output condition
Open loop hardware implementation results (5V, 0.5A), (3.3V,
0.33A) of multi-output push-pull converter with voltage doubler at rated
load conditions are as shown in Fig.4.22 (a) and (b) respectively. The
output voltages obtained (5V, 3.3V) and the hardware prototype
developed is shown in Fig. 4.23. The distortions in Fig.4.22 (a) and
Fig.4.23 (a) are due to the presence of ESR and ESL in the output
electrolytic capacitor and can be reduced by adding a non-electrolytic
capacitor (47 µF) at the output.
(a) (b)
Fig: 4.22 (a) First Output voltage and current (I01) (b) Second output voltage and current (I02)
102
(a) (b)
Fig: 4.23 (a) Both output voltages (b) Open loop Hardware Prototype.
(a) (b) Fig: 4.24 Waveforms of switch-1 pulse, Vcr1 and switch-2 pulse, Vcr2.
The resonant capacitor voltages with the corresponding gating
pulses are illustrated in Fig. 4.24(a) and (b). From the figure it is
observed that the peak capacitor voltages 1 and 2 are 58V and 66V
respectively. It is observed that when the voltage across the capacitor
crosses zero, the switches are turned ON which reduces the switching
losses and thereby increases the efficiency.
4.5.5.3 Line transients
The output voltages for ±15% supply voltage variation are shown in
Fig. 4.25. It was observed that the 5V output is regulated by the PWM
controller IC UC3825 and the voltage variation in the other output is
recorded. The regulated and unregulated voltages for the supply variation
103
are as shown in Fig. 4.25(a) and (b). From the results, it is observed that
only output-1 (5V/500mA) is regulated for all line changes applied
because of the feedback loop provided from output-1 to UC3825. The
change in output voltage – 1 and 2 from the desired value is calculated to
be 125mV (5V- 4.875V) and 1.2V (3.6V-2.4V) respectively. The regulation
of the regulated output is within the standard specification range
(150mV) as specified in Table 3.4, while that of output-2 is above the
standard range. This could be overcome by regulating load-2 by a post
regulator IC UC3834 as discussed in the latter section 5.3.4.
(a) (b)
Fig: 4.25 Output voltages for supply voltage (a) Decrease (b) Increase
4.5.5.4 Load transients
Closed loop implementation of multi-output push-pull converter
for load transients are presented and discussed in this section. The
output voltage waveforms for both the load variations (increase and
decrease) are presented in the Fig. 4.26. The load regulation waveforms
for ±20% load variations are presented in Fig. 4.26(a) and (b) respectively.
In open loop implementation, both the output voltages are observed to
vary when the load resistance is varied, but for closed loop, that is, in
104
Fig. 4.26, the regulated output is almost constant for load variation.
From the results it is observed that output-1 is regulated for the load
changes applied because of the feedback loop provided in UC3825,
whereas the unregulated second output voltage varies with the load
variations. The load voltages were observed for ± 20% variations in load-
1 and the waveforms obtained are as shown in Fig. 4.27.(b)
(a) (b)
Fig: 4.26 Output voltages for second load resistance (a) decrease (b) increase
(a) (b)
Fig: 4.27 Output voltages for first load resistance (a) decrease
(b) increase
4.6 Current fed push-pull converter
The current fed converters are dual to the voltage fed converters,
where the input voltage is transformed to a constant current source with
105
the help of a high valued inductance added in series with the voltage
source. This inductor added at the input side does not increase the
component count in the converter as the necessity of filter inductor at
the output of the voltage fed converter is removed.
This section deals with the current fed push-pull converter that
operates with ZVS. The converter is designed to operate at high switching
frequency and a zero voltage switching technique is used to reduce the
losses associated with high operating frequency. A 4.7W, 50 kHz current
fed ZVS push-pull converter is chosen. The operating modes of the
circuit, design and experimental implementations are explained in detail.
4.6.1 Principle of Operation
Fig. 4.28 shows the ZVS current fed push-pull converter. Two
transformers - one main and another auxiliary, through which the
regulation principle is applied, are put to use in the circuit diagram. Li
and Ctun are the current fed inductor and the resonant capacitor
respectively. Lm and Llk are the magnetizing and leakage inductances of
the main transformer respectively. Cout is the output filter capacitor; LB
and CB are the (auxiliary boost converter) inductor and capacitor
respectively. For achieving ZVS, parasitic elements such as, transformer
leakage inductance and MOSFET internal capacitance, are used in the
resonant circuit. Hence, by maintaining ZVS, switching losses can be
reduced. The regulating transformer is connected to the additional
106
secondary winding of the main transformer. Variable control voltage is
imparted by the auxiliary converter through the auxiliary switch. Based
on the variation in the output voltage, the duty cycle of the switch is
varied by the error detector, compensator and comparator circuit. The
current equivalent to the control voltage is in turn given back to the
input and hence the desired regulation is achieved.
Fig: 4.28 Converter Circuit diagram
4.6.2 Modes of Operation
The converter operates in four different modes. Mode 1 and Mode 3
are power transfer intervals, while mode 2 and mode 4 are zero power
transfer regions. Once the converter is rightly tuned for constant
107
frequency and fixed duty cycle, all the switches work in a resonant
fashion. The operational waveforms [89] are displayed in Fig. 4.29.
A. Mode 1
Switch S1 is turned ON at zero voltage so that switching losses are
reduced. Ctun and the leakage inductance of the main transformer form a
resonant tank. Hence, when the switch is turned ON, the current
increases in a resonant fashion. This causes a half sinusoidal current
flow through the closed circuit formed by source S1 and magnetizing
inductance in primary circuit; while in the secondary, the closed circuit
is formed by D1/D3, load and secondary winding. During this instant, the
parasitic capacitance of S2 (Cds2) is charged to twice of the Ctun voltage.
The magnetizing inductance (Lm) of the main transformer is charged. The
transformer turns ratio regulation is applied through the regulating
transformer as well as diode D3. The circuit diagram for mode 1 operation
is presented in Fig. 4.30(a).
B. Mode 2
When the current through S1, D1 and D3 falls to zero, the switch S1
is turned OFF to achieve zero current switching. The energy stored in the
magnetizing inductance (Lm) discharges the parasitic capacitance of S2
(Cds2). Therefore, the parasitic capacitance of S1 (Cds1) is charged with a
constant current. In this mode, all the diodes are OFF, there is no
transfer of energy from the input to the output and Ctun is charged by the
108
supply current Iin. The circuit diagram for mode 2 operation is displayed
in Fig. 4.30(b).
Fig: 4.29 Theoretical waveforms
C. Mode 3
The switch S2 is turned ON at zero voltage so that switching losses
are reduced. During this period, the current through the switch
increases in a resonant fashion because Ctun and leakage inductance of
the main transformer form a resonant tank. Thereby, a half sinusoidal
current flow through the closed circuit is formed through source S2 and
magnetizing inductance in primary circuit; while in the secondary, the
closed circuit is formed by D2/D4, load and secondary winding.
The parasitic capacitance of S1 (Cds1) will be charged to twice the
Ctun voltage. The magnetizing inductance (Lm) of the main transformer is
discharged and the transformer turns ratio regulation is applied through
109
the regulating transformer and diode D4. The circuit diagram for mode 3
operation is illustrated in Fig. 4.30(c).
(a) Mode 1 operation
(b) Mode 2 & 4 operation
(c) Mode 3 operation
Fig: 4.30 Modes of operation
D. Mode 4
When the current through switch S2 falls to zero, it is turned OFF;
ensuring zero current switching. During this interval, Ctun is charged
110
with the supply current Iin. The parasitic capacitance of S2 (Cds2) is
charged from the energy stored in the magnetizing inductance (Lm) and in
the parasitic capacitance of S1 (Cds1). Transfer of energy from the input
side to the output does not occur in this mode as all the switches and
diodes are in OFF state. The circuit diagram for mode 4 operation is
presented in Fig. 4.30(b).
4.6.3 Regulation Method
The regulation is based on addition or subtraction of voltage in the
AC path of the converter. Here, a controlled transformer is used as a post
regulator which adds or subtracts an additional voltage to the output
filter of the converter. This technique is implemented with ZVS for a
current fed push-pull converter for any operating conditions.
Vc = RMS value of the controlled AC voltage obtained from an auxiliary
PWM controlled converter
Vs = RMS value of the AC voltage obtained from the non-regulated input
Vo = Average value of the regulated output
1 : No = turns-ratio relationship, from input to output of the main
transformer of the converter
An additional winding with a turns ratio 1: NM, with regard to the
primary is used in the main transformer so that regulation can be
implemented. A small regulating current transformer having a turn’s
ratio 1: NR is also used to add or subtract the controlled voltage.
The following equations govern the regulation:
111
VM = Vdc
VC = NR VR + NM VM
VO = NO VM –VR
The output VO is given by:
(
)
Where,
By varying the duty cycle of the auxiliary converter, the control voltage
VC is changed, thereby regulating the output voltage. But the voltage
regulation is limited by the input voltage and transformer turns ratio. If
VS varies between zero and Vs, the output will vary between:
( ) (
) ( )
( ) ( ) ( )
From equations (4.9) and (4.10), it can be seen that by fixing and
the regulation limit can also been fixed.
4.6.4 Design
The design procedure for a 4.7W, 15V current fed push-pull
converter is detailed in this section.
112
4.6.4.1 Specifications
This section deals with the specifications and design aspects of the
power converter. The push-pull converter is fed from a DC source and
the converter is followed by a main transformer. Secondary of the main
transformer are connected to the regulating transformer and are used to
obtain the desired regulation. The specifications of the converter are as
given below:
Switching frequency (fs) = 50kHz
Output power (P0) = 4.7W
Input voltage (Vdc) = 12±15%V
Output voltage-1 (V0) = 15V
Output current-1 (I0) = 0.31A
Switching frequency of Push-pull MOSFET, fs = 50kHz
Switching frequency of Boost converter MOSFET = 120kHz
4.6.4.2 Converter Design
Maximum supply voltage
Minimum supply voltage
Tuning capacitor voltage, Vct = 1.05 * = 14 V
= 0.59
= 0.55
Maximum average input current,
113
Assuming η as 90%, = 1.31 A
For 20% ripple in input current, that is, X = 0.1 (for 20% peak to peak
ripple), maximum input current ripple magnitude is
Therefore,
Minimum inductance required is
Current fed inductor is chosen as Li = 150
Peak primary current magnitude
Output capacitance, ( )
If the voltage ripple is 3% and y is 0.015, then output capacitance Cout =
450µF.
4.6.4.3 Transformer and Inductor Design
Design of transformer and inductors are carried out as per the
design elaborated in section 3.3.1.4 and the results obtained are
tabulated in Table 4.6.
Table 4.6 Transformer and Inductor design details
Parameters Core selected
Transformer design
1004 mm4 ,
Np = 12
,
From Appendix –I : core - EE 20/10/5
,
,
From Appendix –II : SWG =32 ( ), SWG =37 (
) Resonant Inductor Design
,
From Appendix –I : core - E 22/10/5
, ,
From Appendix –II : SWG =22 ( )
114
4.6.4.4 Tuning Capacitor Design
Using equations (4.1) – (4.4), M = 2.35, Im = 1.675 A and Zo >15
Choosing Zo = 20, Where √
(4.11)
From equation (4.11), Ctun = 1µF and Lm = 400µH
4.6.4.5 Boost Converter Design
The boost converter operates at twice the switching frequency of
the main switches. The tuning capacitor value is much lower than the
product value of transformer ratio so as to avoid interference with the
resonant stage.
Input voltage Vi = 4V to 5 V
Output voltage Vob = 12V
For a boost converter,
(4.12)
When Vi = 4V, Dbmax = 0.67
When Vi = 5V, Dbmin = 0.58
Considering the worst case, the design is continued with Dbmin.
The input-output relation is:
(4.13)
From equation (4.13),
Choose input current ripple as 5%, thus
The minimum value of inductance is given by:
115
(4.14)
Substituting the values in the above equation we get
Boost inductor value LB is chosen as 300
Peak current magnitude
The design of the inductor is similar to the design explained in the
section 3.2.1.4 and the calculated values are tabulated in Table 4.7.
The value of capacitance is given by
(4.15)
For 3% output voltage ripple and R=10 , Capacitance C = 0.22µF.
Table 4.7 Boost Inductor Design
Parameters Core selected
From Appendix –I : core - EE 20/10/5
,
,
From Appendix –II : SWG =28 ( )
4.6.5 Closed loop Simulation Results
The converter designed in section 4.6.4 is simulated. Since the
auxiliary part of the converter requires a pulsating current for the
regulating transformer to work, the converter needs to be operated in
closed loop condition. Duty ratio of the auxiliary switch is primarily
dependent on the load voltage. Hence, by adjusting the duty cycle of the
switch, the required output voltage is obtained. The output voltage is
sensed and is compensated by a network for closed loop operation.
116
Pulses required to drive the auxiliary switch are produced by comparing
the DC output of the compensator with a ramp signal. This change is
then fed back to the primary of the converter allowing it to operate in a
closed manner. Fig. 4.31(a) shows the output voltage and load current
during open loop operation for variation in load of ±25%.
The closed loop regulated output voltage and output current for
different values of a resistive load ranging from ±25% are presented in
Fig. 4.31(b).
(a) (b)
Fig: 4.31 (a) Open loop output voltage and output current (b) Closed loop Output Voltage and Load current
From Fig. 4.32, it can be observed that the switch is operated
under ZVZCS, that is, it is turned ON at zero voltage and turned OFF at
117
zero current. The maximum switch voltage and switch current are 28.6V
and 2.54A respectively.
Fig: 4.32 Resonant voltage and current waveforms
(a)
(b)
Fig: 4.33 Voltage waveforms for load change within ± 25%
(a) Switch-1 (b) Switch-2
118
The tuning capacitor’s maximum and minimum voltages are 14V
and 10V respectively. The major advantage of the converter is that the
load variations do not affect resonance. For a load change of ± 25%,
Fig. 4.33(a) and (b) shows the switch voltages; similarly Fig. 4.34 (a) &
(b) shows the switch currents. Resonant part alone is zoomed to
justify that resonance is unaffected by load changes.
(a)
(b)
Fig: 4.34 Current waveforms for load change within ± 25% (a) Switch-1 (b) Switch-2
4.6.6 Experimental Results
The closed loop implementation of ZVS current-fed push-pull
converter which is powered by a 12V DC supply is described here.
119
Considering the voltage rating which is well below 100V and current
ratings below 2A, MOSFET IRF840 is selected as the switch. Fig. 4.35
shows the hardware circuit. The hardware implementation details of the
converter are given in Table 4.8.
Fig: 4.35 Hardware circuit of the converter
Table 4.8 Hardware implementation details
MOSFETS IRF 840
Diodes MUR1560
Pulse generator IC SG 3525
Optocoupler IC TLP 250
Tuning capacitor 1.4µF , 100 V box type
Auxiliary capacitor 220 nF , 100 V box type
Output capacitor 220µF, electrolytic
Main transformer core EE 20/10/5, With turns ratio 1 : 1.5
Current transformer RM14 core with 3C90, 2 turns in primary, 10 turns in secondary
Current fed inductor 150 µH; core EE 20/10/5, With 45 turns of SWG 22
Auxiliary inductor 300µH; core EE 20/10/5, With 60 turns of SWG 28
4.6.6.1 Pulse Generation for Main Switches
The pulses needed to turn ON the two switches during open loop
and closed loop operation is generated using dsPIC30f4011. Closed loop
120
operation is dependent on the auxiliary switch present in the secondary
of the converter where the regulation technique is employed.
The required isolation and amplification of the pulses for the
MOSFET is achieved by using an opto-coupler – TLP 250(Detailed in
Appendix-V).
4.6.6.2 Pulse Generation from Analog Controller IC SG3525
This section deals with pulse generation for SMPS circuits with
analog controller IC SG3525. In SMPS circuits, this 16 pin pulse
generation IC with lower external part count is used for deriving switch
pulses. The first pin of the IC takes in the feedback input. The feedback
voltage is obtained from the voltage divider circuit connected across the
output load. The reference voltage generated in the IC at the 16th pin (5V)
is fed to the reference input pin 2 of the IC. Pin 14 and 2 are inputs of
the error detector circuit. The PI controller output at the 9th pin is
compared with saw tooth waveform generated at the 7th pin of the IC.
PWM generator generates the pulses at 11th and 14th pin and these
pulses are used to turn ON the switches. The SG3525 with PI controller
is shown in Fig. 4.36. The desired frequency is related to the values of
timing resistor (RT), timing capacitor (CT) and dead time resistor (RD) as
derived in equation (4.16).
( ) (4.16)
121
Fig: 4.36 SG3525 as PI controller
The saw tooth and the PI output generated from SG3525, as shown
in Fig. 4.37(a) and (b), are fed to the error detector which produces the
pulses after comparison. The pulse width of the switch can be changed
by varying the control voltage with which the ramp is compared.
(a) (b)
Fig: 4.37 (a) Saw tooth generated from SG3525 (b)PI output from SG3525
Whenever the output voltage is varied, the DC compensated value
also changes, thereby altering the pulse width of the switch. The saw
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tooth waveform produced by CT and the PI controller output produced at
pin 9 are compared as explained in Fig. 4.38(a). The pulse width
generated for an increase or decrease in load variations are 24% and
45% as verified in Fig. 4.38(b) and (c) respectively.
(a) (b) (c)
Fig: 4.38 (a) Pulse for normal load (b) Pulse generated when load increases (c) Pulse generated when load decreases
4.6.6.3 Pulse Generation for Auxiliary Switches
For the operation of the auxiliary switch in closed loop operation of
the converter, PWM pulses are generated with a switching frequency of at
least 100kHz, since the auxiliary side of the converter should be operated
at about two times the switching frequency. The pulse circuitry using IC
SG3525 and the pulse width generated for normal load is 47% as
illustrated in Fig. 4.36 and 4.38(b) respectively. The output voltage is
regulated whenever there is a change in line or load. RT, CT and RD are
designed for generating a ramp of frequency 120kHz from equation (4.16)
and designed values are CT = 0.01µF, RD = 100Ω, RT = 1kΩ.
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4.6.6.4 Load transients
Addition of compensator and PWM generator circuitry to produce
closed loop pulses for the auxiliary switch completes the closed loop
circuit of the converter. The pulses produced for the switch depends on
the load voltage. For a load variation of ±20%, the waveforms of closed
loop voltage and current are shown in Fig. 4.39(b) and (c) and the change
in output voltage from the desired value is calculated to be ±700mV
respectively. From these waveforms it is clear that the output voltage is
regulated stringently for ±20% load variations, while the load change
applied is clearly confirmed in the current waveforms. Output voltage
and current for rated condition are illustrated in Fig. 4.39(a).
(a) (b) (c)
Fig: 4.39 (a) Output voltage and load current (b) Output voltage and load current for 20% decrease of load (c) Output voltage and load current for
20% increase of load
4.6.6.5 Line transients
Line regulation is the response of the closed loop circuit for
changes in supply voltage. The output voltage and current waveform for
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decrease in supply of 15% is displayed in Fig. 4.40. The controller
responds to the supply variations and regulates the output voltage
stringently as observed in the waveform illustrated in Fig. 4.40. Similarly,
waveform is observed for increase in supply also.
Fig: 4.40 Output voltage and load current for 15% supply variation
4.6.6.6 Resonant Waveform
The MOSFET switches are turned ON at zero voltage and turned
OFF at zero current to achieve ZVZCS. The first switch, gate pulse and
switch-1 voltage waveforms are shown in Fig. 4.41(a). The peak voltage
across the switch is 30.4V which is about two times the source voltage.
Fig. 4.41(b) shows the switch-2 voltage waveform.
(a) (b)
Fig: 4.41 (a) Switch-1 pulse and switch-1 voltage (b) Switch-2 pulse
and switch-2 voltages
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The switch-2 voltage produces a peak value of 34.4 V when the
duty cycle of the switch is 29.2. Switch-1 and 2 current waveforms are
shown in Fig. 4.42(a) and (b). The main advantage of the converter is that
load and supply variations do not affect resonance. The resonant
waveforms for a load change of ±20% and supply variations of ±15% are
observed and the results validate the above statement.
(a) (b)
Fig: 4.42 (a) Switch-1 current with gate pulse (b) Switch-2 current with gate pulse
4.7 Analysis
The efficiency and regulation is assessed for a load change of
±25%. The graph of efficiency versus output power and regulation versus
load current is plotted in Fig. 4.43(a) and (b) respectively. It is observed
that the efficiency (as per equation 4.8) is about 90.31% at rated load of
48Ω. Regulation in this case is less than 4%. Regulation is as good as
0.13% for normal input voltage of 12V and a rated load of 48Ω. For the
rated load condition, regulation is less than 1% and the converter works
well even for a load change of ±25%.
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(a) (b)
Fig: 4.43 (a) Efficiency v/s Output power (b) Regulation v/s load current
The efficiencies of hard switched multi-output (MO) push-pull
converter, push-pull ZVS, push-pull ZVS with voltage doubler (VD), ZVS
multi-output push-pull, ZVS multi-output push-pull with voltage doubler
and current fed push-pull converters are compared in table 4.9. From
the table, it is verified that push-pull ZVS MO VD and current fed push-
pull converters have higher efficiencies and are therefore preferred for
low power aerospace and communication applications.
Table 4.9 Efficiency comparison
Hard
switched MO push-pull
Push-
pull ZVS
Push-
pull ZVS VD
Push-
pull ZVS MO
Push-pull
ZVS MO VD
Current fed
Push-pull
49% 57% 64.2% 76.2% 89% 90.31%
The peak amplitude of the output voltage Ymax = 16.76V and the
minimum is Ymin = 15.041V as observed from Fig. 4.44 (a). From these
observed values the peak overshoot is calculated by:
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Maximum peak overshoot, Mp (%) =
(4.17)
Mp = 11.733 %
The settling time and peak time of the current fed push-pull converter in
open loop are 3.537ms and 0.4958 ms respectively.
Similarly for the current fed push-pull converter in closed loop
system, the maximum and minimum amplitude of the output voltage are
Ymax = 15.282V and Ymin = 15.04V respectively as observed from Fig.
4.44(b). The Maximum peak overshoot Mp (%) was calculated as 1.88%
while the settling time and peak time of the converter are 2.317ms and
0.39ms.
(a) (b)
Fig: 4.44 Current fed push-pull converter (a) Open loop time response (b) Closed loop time response.
From the time response waveforms of the open loop and closed
loop system, it is deduced that the performance of the closed loop system
is better and its peak over shoot is lesser and settles faster.
4.8 Cascoded Transformer Connection
To reduce the saturation effect and primary current in the multi-
output high frequency transformers, cascoded transformer connection is
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simulated in PSIM to study the working of the same. The circuit diagram
implemented is as shown in Fig. 4.45.
Fig: 4.45 Cascoded multi-output push-pull circuit.
The outputs responses obtained from cascoded multi-output push-
pull circuit reveal that the settling time, peak overshoot, peak times are
same as the multi-output topology with single transformer as discussed
in section 3.3. This configuration splits the primary current between the
two primaries of the cascoded transformers which further leads to less
saturation. Hence single multi-output transformers can be replaced with
two parallel transformers to obtain the same output and performance,
with the added advantage of lower saturation effect. Simulated results of
output voltage and currents (5V, 0.5A) & (12.5V, 0.25A), (12.5V, 0.1A) &
(3.3V, 0.3A) are shown in figure 4.46 and 4.47 respectively.
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(a) (b)
Fig: 4.46 First and second output waveforms (5V/.5A) & (12.5V, 0.25A)
(a) (b)
Fig: 4.47 Third and fourth output waveforms (12.5V/.1A) & (3.3V, 0.3A)
4.9 Conclusion
The soft switched push-pull converter with multi-output and
voltage doubler is simulated in PSIM and hardware implementation of
the same is carried out. The analysis of the output obtained reveal that
the resonance of soft switched push-pull converter is not affected by the
applied variation. As tabulated in Table 4.9, the efficiency of ZVS multi-
output voltage doubler push-pull topology (89%) and current fed push-
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pull converters (90%) are higher when compared to hard switched push-
pull/ push-pull ZVS/ push-pull ZVS-VD/ push-pull ZVS-MO individual
topologies. The closed loop time domain analysis reveals that the output
settles faster with less peak overshoot. Hence the modified topology with
all the push-pull ZVS multi-output voltage doubler and current fed push-
pull converter are well suited for low power aerospace and
communication applications with tight regulations. The efficiency can be
increased further if the experimental prototype is fabricated on a Printed
Circuit Board (PCB).