Home / Study Materials / KTU B.Tech S5 LectureNotes Power Electronics

KTU B.Tech S5 LectureNotes Power Electronics

KTU B.Tech S5 LectureNotes Power Electronics

DOWNLOAD Module I & II LectureNotes

EC 307 Power Electronics & Instrumentation

MODULE I

 

Difference Between Linear Electronics and Power Electronics

Electronics has now become the core component in the development of the technology. The fast processing computers with there compact size and high efficiency became possible due to the virtue of advancement in the field of electronics.
The electronics is sub divided into two types namely 
(1) Linear Electronics 
(2) Power Electronics
We often mix up with these two words and sometimes use them interchangeably. But according to engineers these two have clearly distinguished from each other.

Linear Electronics

It is the branch of electronics in which we operate the devices in there active mode of operation. We know that the evolution of electronics started with the invention of Transistor. The two PN junctions placed side by side happened to the discovery of a BJT Transistor. Now we know that the operations of a BJT transistor can be shown by its current-voltage characteristic curve.

Now from the above figure it is clear that BJT has three regions of Operation

  1. Cut-Off Region
  2. Saturation Region
  3. Active Region

In linear electronics, we operate the transistor in its active region which can also be called ohmic region in which there is a relation-ship between current and the voltage with some gain value. This region is used in amplifiers circuits where we want to vary the current from collector to the emitter according to our need. In active region, the transistor itself also draws some power and hence causes power loss in it, which in return decrease the efficiency of the device.

Power Electronics

In power electronics, we deal with the cut-off and the saturation region of the transistor. Hence the transistor becomes a switch. When it is in cut off region, no current flows from collector to emitter ideally and it acts as an Off Switch. When it is in saturation region, rated current can flow from collector to emitter, hence act as an On Switch.

This the key difference between the mode of operation of transistor which gives rise to a complete new field in electronics called power electronics. The main feature of power electronics is high efficiency power conversion because in either On state or Off state the power drawn by the transistor is zero (ideally), and hence high efficient devices can be built with efficiency as high as 96%.

The switching converters which are the core of the power electronics actually use high speed switching transistors like MOSFETs and IGBTs which are also capable of sustaining voltages upto 1200 V and high currents. So these power devices help in the manufacturing of high speed devices

 

power semiconductor device is a semiconductor device used as a switch or rectifier in power electronics; a switch-mode power supply is an example. Such a device is also called a power device or, when used in an integrated circuit, a power IC.

A power semiconductor device is usually used in “commutation mode” (i.e., it is either on or off), and therefore has a design optimized for such usage; it should usually not be used in linear operation. Linear power circuits are widespread as voltage regulators, audio amplifiers, and radio frequency amplifiers.

Power semiconductors are found in systems delivering as little as a few tens of milliwatts for a headphone amplifier, up to around a gigwatt in a high voltage direct current transmission line.

Switches

Fig.2 : Current/Voltage/switching frequency domains of the main power electronics switches.

The trade-offs between voltage, current, and frequency ratings also exist for a switch. In fact, any power semiconductor relies on a PIN diode structure in order to sustain voltage; this can be seen in figure 2. The power MOSFET has the advantages of a majority carrier device, so it can achieve a very high operating frequency, but it cannot be used with high voltages; as it is a physical limit, no improvement is expected in the design of a silicon MOSFET concerning its maximum voltage ratings. However, its excellent performance in low voltage applications make it the device of choice (actually the only choice, currently) for applications with voltages below 200 V. By placing several devices in parallel, it is possible to increase the current rating of a switch. The MOSFET is particularly suited to this configuration, because its positive thermal coefficient of resistance tends to result in a balance of current between the individual devices.

The IGBT is a recent component, so its performance improves regularly as technology evolves. It has already completely replaced the bipolar transistor in power applications; a power module is available in which several IGBT devices are connected in parallel, making it attractive for power levels up to several megawatts, which pushes further the limit at which thyristors and GTOs become the only option. Basically, an IGBT is a bipolar transistor driven by a power MOSFET; it has the advantages of being a minority carrier device (good performance in the on-state, even for high voltage devices), with the high input impedance of a MOSFET (it can be driven on or off with a very low amount of power).

The major limitation of the IGBT for low voltage applications is the high voltage drop it exhibits in the on-state (2-to-4 V). Compared to the MOSFET, the operating frequency of the IGBT is relatively low (usually not higher than 50 kHz), mainly because of a problem during turn-off known as current-tail: The slow decay of the conduction current during turn-off results from a slow recombination of a large number of carriers that flood the thick ‘drift’ region of the IGBT during conduction. The net result is that the turn-off switching loss of an IGBT is considerably higher than its turn-on loss. Generally, in datasheets, turn-off energy is mentioned as a measured parameter; that number has to be multiplied with the switching frequency of the intended application in order to estimate the turn-off loss.

At very high power levels, a thyristor-based device (e.g., a SCR, a GTO, a MCT, etc.) is still the only choice. This device can be turned on by a pulse provided by a driving circuit, but cannot be turned off by removing the pulse. A thyristor turns off as soon as no more current flows through it; this happens automatically in an alternating current system on each cycle, or requires a circuit with the means to divert current around the device. Both MCTs and GTOs have been developed to overcome this limitation, and are widely used in power distribution applications.

A few applications of power semiconductors in switch mode include lamp dimmersswitch mode power suppliesinduction cookers, automotive ignition systems, and AC and DC electric motor drives of all sizes.

 

Power Diode Structure:

Power Diode is the two terminal(namely anode and cathode) two layer(P-N) device which is used in most of the power electronics circuits. The power semiconductor diode is similar to low power PN junction diode (signal diode). In fact, power diode is more complex in structure and in operation than their low power counterparts. This complexity happens because low power device must be modified to make them suitable for high power applications.

When the anode terminal is positive with respect to cathode, it is known as forward biased. When the anode terminal is negative with respect to the cathode, it is known as reverse biased.

The power diode plays the vital role in the power electronics circuits. The major and most important applications of power diode in converter circuits are working as a rectifier ( remember that the rectification operation is uncontrollable), freewheeling diode or flyback diode, reverse voltage protection, voltage regulation circuits etc.

When the anode is positive with respect to the cathode terminal the diode starts conducting. Then it act as an uncontrolled switch. ie we no need to provide any gate/base voltage to make it conduct the current. It operation as switch cannot be controlled by applying controlling voltage/current.

The structure of the power diode is little different from the small signal diodes. In this post we will discuss about the power diode structure in detail. The fundamentals of power diode is discussed separately. Please click here to know about basics of Power Diode.

 

  • As shown in the figure, there isheavilydoped n+ substrate with

    dopinglevel of 1019/cm3. This substrate forms a cathode of the power diode.

  • Onn+substrate, lightly doped n- epitaxial layer is grown. This layer is also known

    asdrift region. The doping level of n- layer is about 1014/cm3.

  • Thethe PNjunction is formed by diffusing a heavily doped p+ region. This p+ region forms anode of the diode.The doping level of

    p+region is about 1019/cm3.

  • The thickness of p+ region is 10µm. The thickness of n+substrate is 250µm.
  • The thickness of n- drift region depends upon the breakdown voltage of the diode.
  • The driftregion  determinesthe reverse breakdown voltage of the diode.
  • Its function is to absorb the depletion layer of thereversebiased p+n- junction.
  • As it is lightly doped, it will add significant ohmic resistance to the diode when it is forward biased.
  • For higher breakdown voltages, the drift region is wide.
  • The n- drift region is absent in low power signal diodes.

Conductivity modulation of drift layer:

  • When the power diode is forward biased (anode is made positive with respect to cathode), the holes will be injected from the p+ region into the drift region.
  • Some of the holes combine with the electrons in the drift region. Since injected holes are large, they attract electrons from the n+ layer.
  • Thus holes and electrons are injectedinthe drift region simultaneously.
  • Hence resistance of the drift region reduces significantly.
  • Thus diode current goes on increasing, but drift region resistance remains constant.
  • So on-state losses in the diode are reduced. This phenomenon is called as Conductivity modulationofdrift region.

 

 

Characteristics of Power Diode

The two types of characteristics of a power diode are shown in Fig. 3 and Fig. 4 named as follows:

(i) Amp-volt characteristics (i-v characteristics)

(ii) Turn-off characteristics (or reverse-recovery characteristics)

 

Figure 3. Amp-Volt Characteristics of Power Diode

 

Cut-in voltage is the value of the minimum voltage for VA (anode voltage) to make the diode works in forward conducting mode. Cut-in voltage of signal diode is 0.7 V while in power diode it is 1 V. So, its typical forward conduction drop is larger.   Under forward-bias condition, signal diode current increases exponentially and then increases linearly. In the case of the power diode, it almost increases linearly with the applied voltage as all the layers of P-I-N remain saturated with minority carriers under forward bias. Thus, a high value of current produces results in voltage drop which mask the exponential part of the curve. In reverse-bias condition, small leakage current flows due to minority carriers until the avalanche breakdown appears as shown in Fig. 3.

 

Figure 4. Turn-Off Characteristics of Power Diode: a) Variation of Forward Current if ; b) Variation of Forward Voltage Drop vf ; c) Variation of Power Loss

 

After the forward diode comes to null, the diode continues to conduct in the opposite direction because of the presence of stored charges in the depletion layer and the p or n-layer. The diode current flows for a reverse-recovery time trr. It is the time between the instant forward diode current becomes zero and the instant reverse-recovery current decays to 25 % of its reverse maximum value.

Time T:  Charges stored in the depletion layer removed.

Time Tb :  Charges from the semiconductor layer is removed.

Shaded area in Fig 4.a represents stored charges QR which must be removed during reverse-recovery time trr.

Power loss across diode = v* if    (shown in Fig. 4.c)

As shown, major power loss in the diode occurs during the period tb.

 

Recovery can be abrupt or smooth as shown in Fig. 5. To know it quantitatively, we can use the S – factor.

 

Ratio Tb/T: Softness factor or S-factor.

S-factor: measure of the voltage transient that occurs during the time the diode recovers.

S-factor = 1 ⇒ low oscillatory reverse-recovery process. (Soft –recovery diode)

S-factor <1  ⇒ large oscillatory over voltage (snappy-recovery diode or fast-recovery diode).

Power diodes now exist with forward current rating of 1A to several thousand amperes with reverse-recovery voltage ratings of 50V to 5000V or more.

 

Figure 5. Reverse-Recovery Characteristics for Power Diode

 

Schottky Diode: It has an aluminum-silicon junction where the silicon is an n-type. As the metal has no holes, there is no stored charge and no reverse-recovery time. Therefore, there is only the movement of the majority carriers (electrons) and the turn-off delay caused by recombination process is avoided. It can also switch off much faster than a p-n junction diode. As compared to the p-n junction diode it has:

(a) Lower cut-in voltage

(b) Higher reverse leakage current

(c) Higher operating frequency

Application: high-frequency instrumentation and switching power supplies.

 

Figure 6. Schottky Diode Symbol and Current-Voltage Characteristics Curve

 

Metal-Oxide Semiconductor Field-Effect Transistor (Power)

 

MOSFET is a voltage-controlled majority carrier (or unipolar) three-terminal device. Its symbols are shown in Fig. 7 and Fig. 8. As compared to the simple lateral channel MOSFET for low-power signals, power MOSFET has different structure. It has a vertical channel structure where the source and the drain are on the opposite side of the silicon wafer as shown in Fig. 10. This opposite placement of the source and the drain increases the capability of the power MOSFET to handle larger power.

 

Figure 7. MOSFET Symbol

 

Figure 8. MOSFET Symbols for Different Modes

 

In all of these connections, substrates are internally connected. But in cases where it is connected externally, the symbol will change as shown in the n-channel enhancement type MOSFET in Fig. 9. N-channel enhancement type MOSFET is more common due to high mobility of electrons.

 

Figure 9. N-channel Enhancement-Type MOSFET with Substrate Connected Externally

 

Figure 10. Cross-Sectional View of the Power MOSFET

 

Basic circuit diagram and output characteristics of an n-channel enhancement power MOSFET with load connected are in Fig. 11 and Fig. 12 respectively.

 

Figure 11. Power MOSFET Structural View with Connections

 

Drift region shown in Fig. 11 determines the voltage-blocking capability of the MOSFET.

When VGS = 0,

⇒ VDD makes it reverse biased and no current flows from drain to source.

When VGS > 0,

⇒ Electrons form the current path as shown in Fig. 11. Thus, current from the drain to the source flows. Now, if we will increase the gate-to-source voltage, drain current will also increase.

 

 

Figure 12. Drain Current (ID) vs Drain-to-Source Voltage (VDS) Characteristics Curves

 

For lower value of VDS, MOSFET works in a linear region where it has a constant resistance equal to VDS / ID. For a fixed value of VGS and greater than threshold voltage VTH, MOSFET enters a saturation region where the value of the drain current has a fixed value.

 

Figure 13. Output Characteristics with Load Line

 

If XY represents the load line, then the X-point represents the turn-off point and Y-point is the turn-on point where VDS = 0 (as voltage across the closed switch is zero). The direction of turning on and turning off process is also shown in Fig. 13.

Besides the output characteristics curves, transfer characteristics of power MOSFET is also shown in Fig. 14.

 

Figure 14. Gate-to-Source Voltage vs. Drain Current Characteristics for Power MOSFET

 

Here, VTH is the minimum positive voltage between gate and the source above which MOSFET comes in on-state from the off-state. This is called threshold voltage. It is also shown in the output characteristics curve in Fig. 12.

Close view of the structural diagram given in Fig. 11 reveals that there exists a fictitious BJT and a fictitious diode structure embedded in the power MOSFET as shown in Fig. 15.

As source is connected to both base and emitter of this parasitic BJT, emitter and base of the  BJT are short circuited. That means this BJT acts in cut-off state.

 

Figure 15. Fictitious BJT and Fictitious Diode in the Power MOSFET

 

Fictitious diode anode is connected to the source and its cathode is connected to the drain. So, if we apply the negative voltage VDD across the drain and source, it will be forward biased. That means, the reverse-blocking capability of the MOSFET breaks. Thus, this can be used in inverter circuit for reactive loads without the need of excessive diode across a switch. Symbolically, it is represented in Fig. 16.

 

Figure 16. MOSFET Representation with Internal Body Diode

 

Although MOSFET internal body diode has sufficient current and switching speed for most of the applications, there may be some applications where the use of ultra-fast diodes is required. In such cases, an external fast-recovery diode is connected in an antiparallel manner. But a slow-recovery diode is also required to block the body diode action as given in Fig. 17.

 

Figure 17. Implementation of Fast-Recovery Diode for Power MOSFET

 

One of the important parameters that affects the switching characteristics is the body capacitances existing between its three terminals i.e. drain, source and gate. Its representation is shown in Fig. 18.

 

Figure 18. MOSFET Representation Showing Junction Capacitances

 

Parameters CGS, CGD and CDS are all non-linear in nature and given in the device’s data sheet of a particular MOSFET. They also depend on the DC bias voltage and the device’s structure or geometry. They must be charged through gate during turn-on process to actually turn on the MOSFET. The drive must be capable of charging and discharging these capacitances to switch on or switch off the MOSFET.

Thus, the switching characteristics of a power MOSFET depend on these internal capacitances and the internal impedance of the gate drive circuits. Also, it depends on the delay due to the carrier transport through the drift region. Switching characteristics of power MOSFET are shown in Fig. 19 and Fig. 20.

 

Figure 19. Turn-on Characteristics of Power MOSFET

 

There is a delay from t0 to t1 due to charging of input capacitance up to its threshold voltage VTH. Drain current in this duration remains at zero value. This is called a delay time. There is a further delay from t1 to t2 during which the gate voltage rises to VGS, a voltage required to drive the MOSFET into on-state.  This is called the rise time. This total delay can be reduced by using a low-impedance drive circuit. The gate current during this duration decreases exponentially as shown. For the time greater than t2, the drain current ID has reached its maximum constant value I. As drain current has reached the constant value, the gate-to-source voltage is also constant as shown in the transfer characteristics of MOSFET in Fig. 20.

 

Figure 20. Transfer Characteristics of Power MOSFET with Operating Point

 

For turn-off characteristics, assume that the MOSFET is already in the switched-on situation with steady state. As t = t0, gate voltage is reduced to zero value; CGS and CGD start to discharge through gate resistance RG. This causes a turn-off delay time up to t1 from t0 as shown in Fig. 21. Assuming the drain-to-source voltage remains fixed. During this duration, both VGSand IG decreases in magnitude, drain current remains at a fixed value drawing current from CGD and CGS.

 

Figure 21. Turn-Off Characteristics of Power MOSFET

 

For the time where t> t > t1, gate-to-source voltage is constant. Thus, the entire current is now being drawn from CGD. Up to time t3, the drain current will almost reach zero value; which turns off the MOSFET. This time is known as the fall time, this is when the input capacitance discharges up to the threshold value. Beyond t3, gate voltage decreases exponentially to zero until the gate current becomes zero.

 

 

C. Power Bipolar Junction Transistor (BJT)

 

Power BJT is used traditionally for many applications. However, IGBT (Insulated-Gate Bipolar Transistor) and MOSFET (Metal-Oxide-Semiconductor Field-Effect Transistor) have replaced it for most of the applications but still they are used in some areas due to its lower saturation voltage over the operating temperature range. IGBT and MOSFET have higher input capacitance as compared to BJT. Thus, in case of IGBT and MOSFET, drive circuit must be capable to charge and discharge the internal capacitances.

 

Figure 22. (a) NPN BJT (b) PNP BJT

 

The BJT is a three-layer and two-junction npn or pnp semiconductor device as given in Fig. 22. (a) and (b).

Although BJTs have lower input capacitance as compared to MOSFET or IGBT, BJTs are considerably slower in response due to low input impedance. BJTs use more silicon for the same drive performance.

In the case of MOSFET studied earlier, power BJT is different in configuration as compared to simple planar BJT. In planar BJT, collector and emitter is on the same side of the wafer while in power BJT it is on the opposite edges as shown in Fig. 23. This is done to increase the power-handling capability of BJT.

 

Figure 23. Power BJT PNP Structure

 

Power n-p-n transistors are widely used in high-voltage and high-current applications which will be discussed later.

Input and output characteristics of planar BJT for common-emitter configuration are shown in Fig. 24. These are current-voltage characteristics curves.

 

Figure 24. Input Characteristics and Output Characteristics for the Common-Emitter Configuration of Planar BJT respectively

 

Characteristic curves for power BJT is just the same except for the little difference in its saturation region. It has additional region of operation known as quasi-saturation as shown in Fig. 25.

 

Figure 25. Power BJT Output Characteristics Curve

 

This region appears due to the insertion of lightly-doped collector drift region where the collector base junction has a low reverse bias. The resistivity of this drift region is dependent on the value of the base current.  In the quasi-saturation region, the value of ß decreases significantly. This is due to the increased value of the collector current with increased temperature. But the base current still has the control over the collector current due to the resistance offered by the drift region.  If the transistor enters in hard saturation region, base current has no control over the collector current due to the absence of the drift region and mainly depends on the load and the value of VCC.

A forward-biased p-n junction has two capacitances named depletion layer capacitance and diffused capacitance. While a reverse bias junction has only a depletion capacitance in action. Value of these capacitances depends on the junction voltage and construction of the transistor. These capacitances come into role during the transient operation i.e. switching operations. Due to these capacitances, transistor does not turn on or turn off instantly.

Switching characteristics of power BJT is shown in Fig.26.  As the positive base voltage is applied, base current starts to flow but there is no collector current for some time. This time is known as the delay time (td) required to charge the junction capacitance of the base to emitter to 0.7 V approx. (known as forward-bias voltage). For t > td, collector current starts rising and VCE starts to drop with the magnitude of 9/10th of its peak value. This time is called rise time, required to turn on the transistor. The transistor remains on so long as the collector current is at least of this value.

For turning off the BJT, polarity of the base voltage is reversed and thus the base current polarity will also be changed as shown in Fig. 26. The base current required during the steady-state operation is more than that required to saturate the transistor. Thus, excess minority carrier charges are stored in the base region which needs to be removed during the turn-off process. The time required to nullify this charge is the storage time, ts. Collector current remains at the same value for this time. After this, collector current starts decreasing and base-to-emitter junction charges to the negative polarity; base current also get reduced.

 

Figure 26. Turn-On and Turn-Off Characteristics of BJT

 

 

 

Insulated-Gate Bipolar Transistor (IGBT)

 

IGBT combines the physics of both BJT and power MOSFET to gain the advantages of both worlds. It is controlled by the gate voltage. It has the high input impedance like a power MOSFET and has low on-state power loss as in case of BJT.  There is no even secondary breakdown and not have long switching time as in case of BJT. It has better conduction characteristics as compared to MOSFET due to bipolar nature. It has no body diode as in case of MOSFET but this can be seen as an advantage to use external fast recovery diode for specific applications. They are replacing the MOSFET for most of the high voltage applications with less conduction losses. Its physical cross-sectional structural diagram and equivalent circuit diagram is presented in Fig. 27 to Fig. 29. It has three terminals called collector, emitter and gate.

 

Figure 27. IGBT Structure View

 

There is a p+ substrate which is not present in the MOSFET and responsible for the minority carrier injection into the n-region. Gain of NPN terminal is reduced due to wide epitaxial base and n+ buffer layer.

There are two structures of IGBTs based on doping of buffer layer:

 

  1. a) Punch-through IGBT: Heavily doped n buffer layer ➔ less switching time
  2. b) Non-Punch-through IGBT: Lightly doped n buffer layer ➔ greater carrier lifetime ➔ increased conductivity of drift region ➔ reduced on-state voltage drop

(Note: means implies)

 

Figure 28. Equivalent Circuit for IGBT

 

Figure 29. Simplified Equivalent Circuit for IGBT

 

Figure 30. Circuit Diagram for IGBT

 

Based on this circuit diagram given in Fig.30, forward characteristics and transfer characteristics are obtained which are given in Fig.31 and Fig.32. Its switching characteristic is also shown in Fig. 33.

 

Figure 31. Forward Characteristics for IGBT

 

Figure 32. Transfer Characteristics of IGBT

 

Figure 33. Turn-On and Turn-Off Characteristics of IGBT

 

(Note: Tdn : delay time ; Tr: rise time ; Tdf : delay time ; Tf1: initial fall time ; Tf2: final fall time)

GTO (Gate Turn-off Thyristor)

GTO can be turned on with the positive gate current pulse and turned off with the negative gate current pulse. Its capability to turn off is due to the diversion of PNP collector current by the gate and thus breaking the regenerative feedback effect.

Actually the design of GTO is made in such a way that the pnp current gain of GTO is reduced. Highly doped n spots in the anode p layer form a shorted emitter effect and ultimately decreases the current gain of GTO for lower current regeneration and also the reverse voltage blocking capability. This reduction in reverse blocking capability can be improved by diffusing gold but this reduces the carrier lifetime. Moreover, it requires a special protection as shown in Fig. 43.

Fig. 40 shows the four Si layers and the three junctions of GTO and Fig. 41 shows its practical form. The symbol for GTO is shown in Fig.42.

 

Figure 40. Four Layers and Three Junctions of GTO

 

Figure 41. Practical Form of GTO

 

Figure 42. Symbol of GTO

 

Overall switching speed of GTO is faster than thyristor (SCR) but voltage drop of GTO is larger. The power range of GTO is better than BJT, IGBT or SCR.

The static voltage current characteristics of GTO are similar to SCR except that the latching current of GTO is larger (about 2 A) as compared to SCR (around 100-500 mA).

The gate drive circuitry with switching characteristics is given in Fig. 43 and Fig. 44.

 

Figure 43. Gate Drive Circuit for GTO

 

Figure 44. Turn-On and Turn-Off Characteristics of GTO

 

 

MODULE II

Introduction to Switched mode regulators

Switching regulator basics

The basis of switch mode regulator revolves around the ability of inductors and capacitors to store energy. The capacitors and inductors are integral elements of the switch mode regulator technology.

  • Capacitance   If a current is applied to a capacitor, the capacitor gradually charges up and the voltage across it rises linearly at a rate equal to I/C where is the applied current and C is the capacitance. In thiscasethe voltage across the capacitor cannot change instantly.

When an instantaneous change in current occurs, the voltage changes linearly. [This assumes a current source with an infinite voltage capability is used].

  • Inductor::For an inductor, it is not possible for there to be an instantaneous change in current. Instead, when a voltage is applied, the current builds up linearly over time at a rate equal to V/L where V is the applied voltage and L is the inductance.

Using the standard equations it is possible to determine the current and voltage profiles:

The energy from the rising current is stored in the magnetic field associated with the inductor. If the current flowing through the inductor is suddenly interrupted, the magnetic field reacts against this and produces a very high “back emf” to counteract the change.
Having seen the fundamental or basic concepts behind switching voltages and currents to capacitors and inductors, these basic concepts can be applied to switch mode regulator solutions to provide a variety scenarios for voltage step up and step down circuits.

As the technology uses switching techniques where the series element is on or off, this approach provides much better levels of efficiency than a linear where power is dissipated.

 

Capacitor based switch mode regulation

The basic concept of the capacitor switched mode regulator is shown in the diagram. When the switch is closed, current is able to flow into the reservoir capacitor and provide charge. When the voltage on the capacitor is at is required level, the switch opens and the load will draw current from the capacitor.

As the voltage falls, this will be sensed by the control circuitry and the series switch will be turned on again to bring the capacitor voltage up to the required level.

This circuit is not as effective as may be thought at first sight. Although the only resistive element in the theoretical circuit is the load, this is not the only way in which energy is lost because charging a capacitor directly from a voltage source or a capacitor dissipates as much energy as is transferred to the capacitor. As a result of this, switching mode regulators cannot use capacitor switching techniques alone.

 

Inductor based switch mode regulation

It is also possible to use inductors as an element in switch mode regulators.

The inductor can be used to transfer energy from one voltage source to another. While a simple resistor can be used as a dropper to drop voltage when transferring from one voltage source at a higher voltage to one at a lower voltage, this is very wasteful in terms of power. If an inductor is used, then all the energy is transferred, assuming a perfect inductor.

The use of an inductor has the advantages that energy can be transferred from one source to another regardless of the respective values of voltage and their polarities. To achieve this the proper configuration is obviously required.

When the switches are in the positions shown above, the voltage V1 is applied across the inductor and the current i1 builds up at a rate equal to V1/L. Therefore the peak value obtained will be proportional to the time the switches are in this position, i.e. (V1/L) x t

When the switches are reversed, the current will continue to flow at a rate i2 which is equal to -V2/L.

As an ideal inductor dissipates no energy, there is no power loss in an ideal system using an inductor in this fashion. As a result, it is this method of energy transfer that forms the basis for all switching regulators.

 

Buck-Boost Converter basics

The buck-boost DC-DC converter offers a greater level of capability than the buck converter of boost converter individually, it as expected it extra components may be required to provide the level of functionality needed.

There are several formats that can be used for buck-boost converters:

  • +Vin, -Vout:   This configuration of a buck-boost converter circuit uses the same number of components as the simple buck or boost converters.Howeverthis buck-boost regulator or DC-DC converter produces a negative output for a positive input. While this may be required or can be accommodated for a limited number of applications, it is not normally the most convenient format.

When the switch in closed, current builds up through the inductor. When the switch is opened the inductor supplies current through the diode to the load.

Obviously the polarities (including the diode) within the buck-boost converter can be reversed to provide a positive output voltage from a negative input voltage.

  • +Vin, +Vout:   The second buck-boost converter circuit allows both input and output to be the same polarity.Howeverto achieve this, more components are required. The circuit for this buck boost converter is shown below.

In this circuit, both switches act together, i.e. both are closed or open. When the switches are open, the inductor current builds. At a suitable point, the switches are opened. The inductor then supplies current to the load through a path incorporating both diodes, D1 and D2.

 

The buck boost converter is a DC to DC converter. The output voltage of the DC to DC converter is less than or greater than the input voltage. The output voltage of the magnitude depends on the duty cycle. These converters are also known as the step up and step down transformers and these names are coming from the analogous step up and step down transformer. The input voltages are step up/down to some level of more than or less than the input voltage. By using the low conversion energy, the input power is equal to the output power. The following expression shows the low of a conversion.

Input power (Pin) = Output power (Pout)

For the step up mode, the input voltage is less than the output voltage (Vin<Vout). It shows that the output current is less than the input current. Hence the buck booster is a step up mode.

Vin<Vout and Iin>Iout

In the step down mode the input voltage is greater than the output voltage (Vin>Vout). It follows that the output current is greater the input current. Hence the buck boost converter is a step down mode.

Vin>Vout and Iin<Iout

What is a Buck Boost Converter?

It is a type of DC to DC converter and it has a magnitude of output voltage. It may be more or less than equal to the input voltage magnitude. The buck boost converter is equal to the fly back circuit and single inductor is used in the place of the transformer. There are two types of converters in the buck boost converter that are buck converter and the other one is boost converter. These converters can produce the range of output voltage than the input voltage. The following diagram shows the basic buck boost converter.

Buck Boost Converter

Working principle of Buck Boost Converter

The working operation of the DC to DC converter is the inductor in the input resistance has the unexpected variation in the input current. If the switch is ON then the inductor feed the energy from the input and it stores the energy of magnetic energy. If the switch is closed it discharges the energy. The output circuit of the capacitor is assumed as high sufficient than the time constant of an RC circuit is high on the output stage. The huge time constant is compared with the switching period and make sure that the steady state is a constant output voltage Vo(t) = Vo(constant) and present at the load terminal.

There are two different types of working principles in the buck boost converter.

  • Buck converter.
  • Boost converter.

Buck Converter Working

The following diagram shows the working operation of the buck converter. In the buck converter first transistor is turned ON and second transistor is switched OFF due to high square wave frequency. If the gate terminal of the first transistor is more than the current pass through the magnetic field, charging C, and it supplies the load. The D1 is the Schottky diode and it is turned OFF due to the positive voltage to the cathode.

Buck Converter Working

The inductor L is the initial source of current. If the first transistor is OFF by using the control unit then the current flow in the buck operation. The magnetic field of the inductor is collapsed and the back e.m.f is generated collapsing field turn around the polarity of the voltage across the inductor. The current flows in the diode D2, the load and the D1 diode will be turned ON.

The discharge of the inductor L decreases with the help of the current. During the first transistor is in one state the charge of the accumulator in the capacitor. The current flows through the load and during the off period keeping Vout reasonably. Hence it keeps the minimum ripple amplitude and Vout closes to the value of Vs

Boost Converter Working

In this converter the first transistor is switched ON continually and for the second transistor the square wave of high frequency is applied to the gate terminal. The second transistor is in conducting when the on state and the input current flow from the inductor L through the second transistor. The negative terminal charging up the magnetic field around the inductor. The D2 diode cannot conduct because the anode is on the potential ground by highly conducting the second transistor.

Boost Converter Working

By charging the capacitor C the load is applied to the entire circuit in the ON State and it can construct earlier oscillator cycles. During the ON period the capacitor C can discharge regularly and the amount of high ripple frequency on the output voltage. The approximate potential difference is given by the equation below.

VS + VL

During the OFF period of second transistor the inductor L is charged and the capacitor C is discharged. The inductor L can produce the back e.m.f and the values are depending up on the rate of change of current of the second transistor switch. The amount of inductance the coil can occupy. Hence the back e.m.f can produce any different voltage through a wide range and determined by the design of the circuit. Hence the polarity of voltage across the inductor L has reversed now.

The input voltage gives the output voltage and atleast equal to or higher than the input voltage. The diode D2 is in forward biased and the current applied to the load current and it recharges the capacitors to VS + VL and it is ready for the second transistor.

Modes Of Buck Boost Converters

There are two different types of modes in the buck boost converter. The following are the two different types of buck boost converters.

  • Continuous conduction mode.
  • Discontinuous conduction mode.

Continuous Conduction Mode

In the continuous conduction mode the current from end to end of inductor never goes to zero. Hence the inductor partially discharges earlier than the switching cycle.

Discontinuous Conduction Mode

In this mode the current through the inductor goes to zero. Hence the inductor will totally discharge at the end of switching cycles.

Applications of Buck boost converter

  • It is used in theself regulatingpower supplies.
  • It has consumer electronics.
  • It is used in the Battery power systems.
  • Adaptive control applications.
  • Power amplifier applications.

Advantages of Buck Boost Converter

  • It gives higher output voltage.
  • Low operating duct cycle.
  • Low voltage on MOSFETs

 

Waveforms and expression of DC-DC converters for output voltage, voltage and current ripple under continuous conduction mode.

 

 

http://www.ee.unlv.edu/~eebag/EE-442-642-DC-to-DC%20Converters.pdf

 

Isolated converters – Flyback, Forward, Push Pull, Half Bridge and Full Bridge Converters – waveforms and governing equations.

 

6.3 TRANSFORMER ISOLATION

In a large number of applications, it is desired to incorporate a transformer into a switching converter, to obtain dc isolation between the converter input and output. For example, in off-line applications (where the converter input is connected to the ac utility system), isolation is usually required by regulatory agencies. Isolation could be obtained in these cases by simply connecting a 50 Hz or 60 Hz transformer at the converter ac input. However, since transformer size and weight vary inversely with frequency, significant improvements can be made by incorporating the transformer into the converter, so that the transformer operates at the converter switching frequency of tens or hundreds of kilohertz.

When a large step-up or step-down conversion ratio is required, the use of a transformer can allow better converter optimization. By proper choice of the transformer turns ratio, the voltage or current stresses imposed on the transistors and diodes can be minimized, leading to improved efficiency and lower cost.

Multiple dc outputs can also be obtained in an inexpensive manner, by adding multiple secondary windings and converter secondary-side circuits. The secondary turns ratios are chosen to obtain the desired output voltages. Usually only one output voltage can be regulated via control of the converter duty cycle, so wider tolerances must be allowed for the auxiliary output voltages. Cross-regularion is a measure of the variation in an auxiliary output voltage, given that the main output voltage is perfectly regulated [18-20].

A physical multiple-winding transformer having turns ratio n1:n2:n3:… is illustrated in Fig. 6.17(a). A simple equivalent circuit is illustrated in Fig. 6.17(b), which is sufficient for understanding the operation of most transformer-isolated converters. The model assumes perfect coupling between windings and neglects losses; more accurate models are discussed in a later chapter. The ideal transformer obeys the relations

v1(t)     v2 (t)     v3(t)

=         =          =…

n1                 n2                  n3                                                                                     (6.16)

0 = n1i1(t)+n2i2 (t)+ n3i3 (t)+…

In parallel with the ideal transformer is an inductance LM, called the magnetizing inductance, referred to the transformer primary in the figure.

 

Fig. 6.17. Simplified model of a multiple-winding transformer (a) schematic symbol, (b) equivalent circuit containing a magnetizing inductance and ideal transformer.

Fig. 6.18. B-H characteristics of transformer core.

Physical transformers must contain a magnetizing inductance. For example, suppose we disconnect all windings except for the primary winding. We are then left with a single winding on a magnetic core – an inductor. Indeed, the equivalent circuit of Fig. 6.17(b) predicts this behavior, via the magnetizing inductance.

The magnetizing current iM(t) is proportional to the magnetic field H(t) inside the transformer core. The physical B-H characteristics of the transformer core material, illustrated in Fig. 6.18, govern the magnetizing current behavior. For example, if the magnetizing current iM(t) becomes too large, then the magnitude of the magnetic field H(t) causes the core to saturate. The magnetizing inductance then becomes very small in value, effectively shorting out the transformer.

The presence of the magnetizing inductance explains why transformers do not work in dc circuits: at dc, the magnetizing inductance has zero impedance, and shorts out the windings. In a well-designed transformer, the impedance of the magnetizing inductance is large in magnitude over the intended range of operating frequencies, such that the magnetizing current iM(t) has much smaller magnitude than il(t). Then il’(t) ≈il(t), and the transformer behaves nearly as an ideal transformer. It should be emphasized that the magnetizing current iM(t) and the primary winding current il(t) are independent quantities.

The magnetizing inductance must obey all of the usual rules for inductors. In the model of Fig. 6.17(b), the primary winding voltage vl(t) is applied across LM, and hence diM(t)

vl(t) = LM                                (6.17) dt

Integration leads to

1

iM(t) −iM(0) =      vl(τ)dτ                   (6.18) LM

So the magnetizing current is determined by the integral of the applied winding voltage. The principle of inductor volt-second balance also applies: when the converter operates in steady-state, the dc component of voltage applied to the magnetizing inductance must be zero:

1    Ts

0 = vl(t)dt                         (6.19) Ts0

Since the magnetizing current is proportional to the integral of the applied winding voltage, it is important that the dc component of this voltage be zero. Otherwise, during each switching period there will be a net increase in magnetizing current, eventually leading to excessively large currents and transformer saturation.

The operation of converters containing transformers may be understood by inserting the model of Fig. 6.17(b) in place of the transformer in the converter circuit. Analysis then proceeds as described in the previous chapters, treating the magnetizing inductance as any other inductor of the converter.

Practical transformers must also contain leakage inductance. A small part of the flux linking a winding may not link the other windings. In the two-winding transformer, this phenomenon may be modeled with small inductors in series with the windings. In most isolated converters, leakage inductance is a nonideality that leads to switching loss, increased peak transistor voltage, and that degrades cross-regulation, but otherwise has no influence on basic converter operation.

There are several ways of incorporating transformer isolation into a dc-dc converter. The full-bridge, half-bridge, forward, and push-pull converters are commonly used isolated versions of the buck converter. Similar isolated variants of the boost converter are known. The flyback converter is an isolated version of the buck-boost converter. These isolated converters, as well as isolated versions of the SEPIC and the Cuk converter, are discussed in this section.

 

 

 

Fig. 6.19. Full-bridge transformer-isolated buck converter: (a) schematic diagram, (b) replacement of transformer with equivalent circuit model.

6.3.1 Full Bridge and Half-Bridge Isolated Buck Converters

The full-bridge transformer-isolated buck converter is sketched in Fig. 6.19(a). A version containing a center-tapped secondary winding is shown; this circuit is commonly used in converters producing low output voltages. The two halves of the center-tapped secondary winding may be viewed as separate windings, and hence we can treat this circuit element as a three-winding transformer having turns ratio 1:n:n. When the transformer is replaced by the equivalent circuit model of Fig. 6.17(b), the circuit of Fig. 6.19(b) is obtained. Typical waveforms are illustrated in Fig. 6.20. The output portion of the converter is similar to the nonisolated buck converter – compare the vs(t) and i(t) waveforms of Fig. 6.20 with Figs. 2.1(b) and 2.10.

 

Fig. 6.20. Waveforms of the full-bridge transformer-isolated buck converter.

During the first subinterval 0 <t<DTs, transistors Q1 and Q4 conduct, and the transformer primary voltage is vT = Vg. This positive voltage causes the magnetizing current iM(t) to increase with a slope of Vg/LM. The voltage appearing across each half of the center-tapped secondary winding is nVg, with the polarity mark at positive potential. Diode D5 is therefore forward-biased, and D6 is reverse-biased. The voltage vs(t) is then equal to nVg, and the output filter inductor current i(t) flows through diode

D5.

Several transistor control schemes are possible for the second subinterval DTs<t<Ts. In the most common scheme, all four transistors are switched off, and hence the transformer voltage is vT = 0. Alternatively, transistors Q2 and Q4 could conduct, or transistors Q1 and Q3 could conduct. In any event, diodes D5 and D6 are both forward-biased during this subinterval; each diode conducts approximately one-half of the output filter inductor current.

Actually, the diode currents iD5 and iD6 during the second subinterval are functions of both the output inductor current and the transformer magnetizing current. In the ideal case (no magnetizing current), the transformer causes iD5(t) and iD6(t) to be equal in magnitude since, if il’(t) = 0, then niD5(t)=niD6(t). But the sum of the two diode currents is equal to the output inductor current:

iD5(t)+iD6(t) = i(t)                          (6.20)

Therefore, it must be true that iD5 = iD6 = 0.5i during the second subinterval. In practice, the diode currents differ slightly from this result, because of the nonzero magnetizing current. The ideal transformer currents in Fig. 6.19(b) obey

il‘(t) − niD5 (t)+ iD6(t) = 0                      (6.21)

The node equation at the primary of the ideal transformer is

il(t) = iM(t) +il‘(t) = 0                        (6.22)

Elimination of il(t) from Eqs. (6.21) and (6.22) leads to

il(t) − niD5 (t)+ niD6(t) = iM(t)                    (6.23)

Equations (6.23) and (6.20) describe, in the general case, the transformer winding currents during the second subinterval. According to Eq. (6.23), the magnetizing current iM(t) may flow through the primary winding, through one of the secondary windings, or it may divide between all three of these windings. How the division occurs depends on the i-v characteristics of the conducting transistors and diodes. In the case where il = 0, the solution to Eqs. (6.20) and (6.23) is

1

iD5(t) = i(t)− iM(t)

2n

(6.24)

  • 1

iD6 (t) = i(t)+ iM(t)

  • 2n

Provided that iM<<ni, then iD5 and iD6 are each approximately 0.5i.

The next switching period, Ts<t< 2Ts, proceeds in a similar manner, except that the transformer is excited with voltage of the opposite polarity. During Ts<t< (Ts + DTs), transistors Q2 and Q3 and diode D6 conduct. The applied transformer primary voltage is vT = –Vg, which causes the magnetizing current to decrease with slope – Vg/LM. The voltage vs(t) is equal to nVg, and the output inductor current i(t) flows through diode D6. Diodes D5 and D6 again both conduct during (Ts + DTs) <t< 2Ts, with operation similar to subinterval 2 described previously. It can be seen that the switching ripple in the output filter elements has frequency fs = 1/Ts. However, the transformer waveforms have frequency 0.5fs.

By application of the principle of inductor volt-second balance to the magnetizing inductance, the average value of the transformer voltage vT(t) must be zero when the converter operates in steady state. During the first switching period, positive volt-seconds are applied to the transformer, approximately equal to

(Vg − (Q1 and Q4 forward voltage drops))(Q1 and Q4 conduction time)  (6.25)

During the next switching period, negative volt-seconds are applied to the transformer, given by

−(Vg − (Q2 and Q3 forward voltage drops))(Q2 and Q3 conduction time)  (6.26)

The net volt-seconds, that is, the sum of Eqs. (6.25) and (6.26), should equal zero. While the full bridge scheme causes this to be approximately true, in practice there exist imbalances such as small differences in the transistor forward voltage drops or in the transistor switching times, so that <vT> is small but nonzero. In consequence, during every two switching periods there is a net increase in the magnitude of the magnetizing current. This increase can cause the transistor forward voltage drops to change such that small imbalances are compensated. However, if the imbalances are too large, then the magnetizing current becomes large enough to saturate the transformer.

Transformer saturation under steady-state conditions can be avoided by placing a capacitor in series with the transformer primary. Imbalances then induce a dc voltage component across the capacitor, rather than across the transformer primary. Another solution is the use of current-programmed control, discussed in a later chapter. The series capacitor is omitted when current-programmed control is used.

By application of the principle of volt-second balance to the output filter inductor L, the dc load voltage must be equal to the dc component of vs(t):

V = vs                                                                       (6.27)

By inspection of the vs(t) waveform in Fig. 6.20, <vs> = nDVg. Hence,

V = nDVg                              (6.28) So as in the buck converter, the output voltage can be controlled by variation of the transistor duty cycle D. An additional increase or decrease of the voltage can be obtained via the physical transformer turns ratio n. Equation (6.28) is valid for operation in the continuous conduction mode; as in the nonisolated buck converter, the full-bridge and half-bridge converters can operate in discontinuous conduction mode at light load. The converter can operate over essentially the entire range of duty cycles 0 ≤ D < 1.

Transistors Q1 and Q2 must not conduct simultaneously; doing so would short out the dc source Vg and lead to low efficiency and transistor failure. If necessary, delay can be introduced between the turn-off of one transistor and the turn-on of the next transistor to prevent overlapping conduction. Diodes D1 to D4 ensure that the peak transistor voltage is limited to the dc input voltage Vg, and also provide a conduction path for the transformer magnetizing current at light load. Details of the switching transitions of the full-bridge circuit are discussed further in a later chapter, in conjunction with zero-voltage switching phenomena.

The full-bridge configuration is typically used in switching power supplies at power levels of approximately 750 W and greater. It is usually not used at lower power levels because of its high parts count – four transistors and their associated drive circuits are required. The utilization of the transformer is good, leading to small transformer size. In particular, the utilization of the transformer core is very good, since the transformer magnetizing current can be both positive and negative. Hence, the entire core B-H loop can be used. However, in practice, the flux swing is usually limited by core loss. The transformer primary winding is effectively utilized. But the center-tapped secondary winding is not, since each half of the center-tapped winding transmits power only during alternate switching periods. Also, the secondary winding currents during subinterval 2 lead to winding power loss, but not to transmittal of energy to the load. Design of the transformer of the full-bridge configuration is discussed in detail in a later chapter.

The half-bridge transformer-isolated buck converter is illustrated in Fig. 6.21. Typical waveforms are illustrated in Fig. 6.22. This circuit is similar to the full-bridge of Fig. 6.19(a), except transistors Q3 and Q4, and their antiparallel diodes, have been replaced with large-value capacitors Ca and Cb. By volt-second balance of the transformer magnetizing inductance, the dc voltage across capacitor Cb, is equal to the dc component of the voltage across transistor Q2, or 0.5Vg. The transformer primary voltage vT(t) is then 0.5 Vg, when transistor Q1 conducts, and -0.5Vg when transistor Q2 conducts. The magnitude of vT(t) is half as large as in the full-bridge configuration, with the result that the output voltage is reduced by a factor of 0.5:

V = 0.5nDVg                            (6.29)

The factor of 0.5 can be compensated for by doubling the transformer turns ratio n. However, this causes the transistor currents to double.

 

Fig. 6.21. Half-bridge transformer-isolated buck converter.

Fig. 6.22. Waveforms of the half-bridge transformer-isolated buck converter.

So the half-bridge configuration needs only two transistors rather than four, but these two transistors must handle currents that are twice as large as those of the full-bridge circuit. In consequence, the half-bridge configuration finds application at lower power levels, for which transistors with sufficient current rating are readily available, and where low parts count is important. Utilization of the transformer core and windings is essentially the same as in the full-bridge, and the peak transistor voltage is clamped to the dc input voltage Vg by diodes D1 and D2. It is possible to omit capacitor Ca if desired. The current-programmed mode generally does not work with half-bridge converters.

6.3.2 Forward Converter

The forward converter is illustrated in Fig. 6.23. This transformer-isolated converter is based on the buck converter. It requires a single transistor, and hence finds application at power levels lower than those commonly encountered in the full-bridge and half-bridge configurations. Its nonpulsating output current, shared with other buck-derived converters, makes the forward converter well suited for applications involving high output currents. The maximum transistor duty cycle is limited in value; for the common choice n1 = n2, the duty cycle is limited to the range 0 ≤D< 0.5.

 

Fig. 6.23. Single-transistor forward converter.

Fig. 6.24. Forward converter, with transfonner equivalent circuit model.

 

Fig. 6.25. Waveforms of the forward converter.

The transformer magnetizing current is reset to zero while the transistor is in the off-state. How this occurs can be understood by replacing the three-winding transformer in Fig. 6.23 with the equivalent circuit of Fig. 6.17(b). The resulting circuit is illustrated in Fig. 6.24, and typical waveforms are given in Fig. 6.25. The magnetizing inductance LM, in conjunction with diode D1, must operate in the discontinuous conduction mode. The output inductor L, in conjunction with diode D3, may operate in either continuous or discontinuous conduction mode. The waveforms of Fig. 6.25 are sketched for continuous mode operation of inductor L. During each switching period, three subintervals then occur as illustrated in Fig. 6.26.

 

Fig. 6.26. Forward converter circuit: (a) during subinterval 1, (b) during subinterval 2, (c) during subinterval 3.

During subinterval 1, transistor Q1 conducts and the circuit of Fig. 6.26(a) is obtained. Diode D2 becomes forward-biased, while diodes D1 and D3 are reverse-biased. Voltage Vg is applied to the transformer primary winding, and hence the transformer magnetizing current iM(t) increases with a slope of Vg/LM as illustrated in Fig. 6.25. The voltage across diode D3 is equal to Vg, multiplied by the turns ratio n3/n1.

The second subinterval begins when transistor Q1 is switched off. The circuit of Fig. 6.26(b) is then obtained. The transformer magnetizing current iM(t) at this instant is positive, and must continue to flow. Since transistor Q1 is off, the equivalent circuit model predicts that the magnetizing current must flow into the primary of the ideal transformer. It can be seen that n1iM ampere-turns flow out of the polarity mark of the primary winding. Hence, according to Eq. (6.16). an equal number of total ampere-turns must flow into the polarity marks of the other windings. Diode D2 prevents current from flowing into the polarity mark of winding 3. Hence, the Current iMn1/n2 must flow into the polarity mark of winding 2. So diode D1 becomes forward biased, while diode D2 is reverse-biased. Voltage Vg applied to winding 2, and hence the voltage across the magnetizing inductance is –Vgn1/n2, referred to winding 1. This negative voltage causes the magnetizing current to decrease, with a slope of –Vgn1/n2LM. Sincc diode D2 is reverse-biased, diode D3 must turn on to conduct the output inductor current i(t).

When the magnetizing current reaches zero, diode D1 becomes reverse-biased. Subinterval 3 then begins, and the circuit of Fig. 6.26(c) is obtained. Elements Q1, D1, and D2 operate in the off state, and the magnetizing current remains at zero for the balance of the switching period.

By application of the principle of inductor volt-second balance to the transformer magnetizing inductance, the primary winding voltage vl(t) must have zero average. Referring to Fig. 6.25, the average of vl(t) is given by

vl= D(Vg )+ D2 (−Vg n1 / n2)+ D3 (0) = 0             (6.30)

Solution for the duty cycle D, yields

n2

D2 = D                             (6.31)

n1

Note that the duty cycle D3 cannot be negative. But since D + D2 + D3 = 1, we can write

D3 =1− D D2 ≥ 0                        (6.32)

Substitution of Eq. (6.31) into Eq. (6.32) leads to

n2

D3 =1− D(1+ ) ≥ 0                      (6.33)  n1

Solution for D then yields

1

D ≤                                                            (6.34)

n2

1+

n1

So the maximum duty cycle is limited. For the common choice n1 = n2, the limit becomes

D                                 (6.35)

If this limit is violated, then the transistor off-time is insufficient to reset the transformer magnetizing current to zero before the end of the switching period. Transformer saturation may then occur.

The transformer magnetizing current waveform iM(t) is illustrated in Fig. 6.27, for the typical case where n1 = n2. Figure 6.27(a) illustrates operation with D≤ 0.5. The magnetizing inductance, in conjunction with diode D1, operates in the discontinuous conduction mode, and iM(t) is reset to zero before the end of each switching period. Figure 6.27(b) illustrates what happens when the transistor duty cycle D is greater than 0.5. There is then no third subinterval, and the magnetizing inductance operates in continuous conduction mode. Furthermore, subinterval 2 is not long enough to reset the magnetizing current to zero. Hence, there is a net increase of iM(t) over each switching period. Eventually, the magnetizing current will become large enough then saturate the transformer.

 

Fig. 6.27. Magnetizing current waveform, forward converter: (a) DCM, D< 0.5; (b) CCM, D> 0.5.

The converter output voltage can be found by application of the principle of inductor volt-second balance to inductor L. The voltage across inductor L must have zero dc component, and therefore the dc output voltage V is equal to the dc component of diode D3 voltage vD3(t). The waveform vD3(t) is illustrated in Fig. 6.25. It has an average value of

n3

vD3 =V = DVg                          (6.36)

n1

This is the solution of the forward converter in the continuous conduction mode. The solution is subject to the constraint given in Eq. (6.34).

It can be seen from Eq. (6.34) that the maximum duty cycle could be increased by decreasing the turns ratio n2/n1. This would cause iM(t) to decrease more quickly during subinterval 2, resetting the transformer faster. Unfortunately, this also increases the voltage stress applied to transistor Q1. The maximum voltage applied to transistor Q1 occurs during subinterval 2; solution of the circuit of Fig. 6.26(b) for this voltage yields

n1max vQ1 =Vg (1+ )                         (6.37) n2

For the common choice n1 = n2, the voltage applied to the transistor during subinterval 2 is 2Vg. In practice, a somewhat higher voltage is observed, due to ringing associated with the transformer leakage inductance. So decreasing the turns ratio n2/n1, allows increase of the maximum transistor duty cycle, at the expense of increased transistor blocking voltage.

A two-transistor version of the forward converter is illustrated in Fig. 6.28. Transistors Q1 and Q2 are controlled by the same gate drive signal, such that they both conduct during subinterval 1, and are off during subintervals 2 and 3. The secondary side of the converter is identical to the single-transistor forward converter; diode D3 conducts during subinterval 1, while diode D4 conducts during subintervals 2 and 3. During subinterval 2, the magnetizing current iM(t) forward-biases diodes D1 and D2. The transformer primary winding is then connected to Vg, with polarity opposite that of subinterval 1. The magnetizing current then decreases, with slope = Vg/LM. When the magnetizing current reaches zero, diodes D1 and D2 become reverse-biased. The magnetizing current then remains at zero for the balance of the switching period. So operation of the two-transistor forward converter is similar to the single-transistor forward converter, in which n1=n2. The duty cycle is limited to D< 0.5. This converter has the advantage that the transistor peak blocking voltage is limited to Vg, and is clamped by diodes D1 and D2. Typical power levels of the two-transistor forward converter are similar to those of the half-bridge configuration.

Fig. 6.28. Two-transistor forward converter.

The utilization of the transformer of the forward converter is quite good. Since the transformer magnetizing current cannot be negative, only half of the core B-H loop can be used. This would seemingly imply that the transformer cores of forward converters should be twice as large as those of full- or half-bridge converters. However, in modern high-frequency converters, the flux swing is constrained by core loss rather than by the core material saturation flux density. In consequence, the utilization of the transformer core of the forward converter can be as good as in the full- or half-bridge configurations. Utilization of the primary and secondary windings of the transformer is better than in the full-bridge, half-bridge, or push-pull configurations, since the forward converter requires no center-tapped windings. During subinterval 1, all of the available winding copper is used to transmit power to the load. Essentially no unnecessary current flows during subintervals 2 and 3. Typically, the magnetizing current is small compared to the reflected load current, and has negligible effect on the transformer utilization. So the transformer core and windings are effectively utilized in modem forward converters.

6.3.3 Push-Pull Isolated Buck Converter

The push-pull isolated buck converter is illustrated in Fig. 6.29. The secondary-side circuit is identical with the full- and half-bridge converters, with identical waveforms. The primary-side circuit contains a center-tapped winding. Transistor Q1 conducts for time DTs during the first switching period. Transistor Q2 conducts for an identical length of time during the next switching period, such that volt-second balance is maintained across the transformer primary winding. Converter waveforms are illustrated in Fig. 6.30. This converter can operate oven the entire range of duty cycles 0 ≤D< 1. Its conversion ratio is given by

V = nDVg                              (6.38)

 

Fig. 6.29. Push-pull isolated buck converter.

Fig. 6.30. Waveforms of the push-pull isolated buck converter.

This converter is sometimes used in conjunction with low input voltages. It tends to exhibit low primary-side conduction losses, since at any given instant only one transistor is connected in series with the dc source Vg. The ability to operate with transistor duty cycles approaching unity also allows the turns ratio n to be minimized, reducing the transistor currents.

The push-pull configuration is prone to transformer saturation problems. Since it cannot be guaranteed that the forward voltage drops and conduction times of transistors Q1 and Q2 are exactly equal, small imbalances can cause the dc component of voltage applied to the transformer primary to be nonzero. In consequence, during every two switching periods there is a net increase in the magnitude of the magnetizing current. If this imbalance continues, then the magnetizing current can eventually become large enough to saturate the transformer.

Current-programmed control can be employed to mitigate the transformer saturation problems. Operation of the push-pull converter using only duty cycle control is not recommended.

Utilization of the transformer core material and secondary winding is similar to that for the full-bridge converter. The flux and magnetizing current can be both positive and negative, and therefore the entire B-H loop can be used, if desired. Since the primary and secondary windings are both center-tapped, their utilization is suboptimal.

6.3.4 Flyback Converter

The flyback converter is based on the buck-boost converter. Its derivation is illustrated in Fig. 6.31. Figure 6.31 (a) depicts the basic buck-boost converter, with the switch realized using a MOSFET and diode. In Fig. 6.3l(b), the inductor winding is constructed using two wires, with a 1:1 turns ratio. The basic function of the inductor is unchanged, and the parallel windings are equivalent to a single winding constructed of larger wire. In Fig. 6.3l(c), the connections between the two windings are broken. One winding is used while the transistor Q1 conducts, while the other winding is used when diode D1 conducts. The total current in the two windings is unchanged from the circuit of Fig. 6.31(b); however, the current is now distributed between the windings differently. The magnetic fields inside the inductor in both cases are identical. Although the two-winding magnetic device is represented using the same symbol as the transformer, a more descriptive name is “two-winding inductor.” This device is sometimes also called a “flyback transformer.” Unlike the ideal transformer, current does not flow simultaneously in both windings of the flyback transformer. Figure 6.3l(d) illustrates the usual configuration of the flyback converter. The MOSFET source is connected to the primary-side ground, simplifying the gate drive circuit. The transformer polarity marks are reversed, to obtain a positive output voltage. A 1:n turns ratio is introduced; this allows better converter optimization.

 

Fig. 6.31. Derivation of the flyback converter: (a) buck-boost converter; (b) inductor L is wound with two parallel wires; (c) inductor windings are isolated, leading to the flyback converter; (d) with a 1:n turns ratio and positive output.

The flyback converter may be analyzed by insertion of the model of Fig. 6.17(b) in place of the flyback transformer. The circuit of Fig. 6.32(a) is then obtained. The magnetizing inductance LM functions in the same manner as inductor L of the original buck-boost converter of Fig. 6.31(a). When transistor Q1 conducts, energy from the dc source Vg is stored in LM. When diode D1 conducts, this stored energy is transferred to the load, with the inductor voltage and current scaled according to the 1:n turns ratio.

 

Fig. 6.32. Flyback converter circuit: (a) with transformer equivalent circuit model, (b) during subinterval 1, (c) during subinterval 2.

During subinterval 1, while transistor Q1 conducts, the converter circuit model reduces to Fig. 6.32(b). The inductor voltage vL, capacitor current iC, and dc source current ig, are given by

vL=Vg

v

iC=−                              (6.39)

R ig= i

With the assumption that the converter operates in the continuous conduction mode, with small inductor current ripple and small capacitor voltage ripple, the magnetizing current i and output capacitor voltage v can be approximated by their dc components, I and V, respectively. Equation (6.39) then becomes

vL=Vg

V

iC=−                              (6.40)

R ig= I

During the second subinterval, the transistor is in the off state, and the diode conducts. The equivalent circuit of Fig. 6.32(c) is obtained. The primary-side magnetizing inductance voltage vL, the capacitor current iC, and the dc source current ig, for this subinterval are:

vvL=−

n

i     v

iC= −                             (6.41) n  R ig= 0

It is important to consistently define vL(t) on the same side of the transformer for all subintervals. Upon making the small-ripple approximation, one obtains

V vL=−

n

I     V

iC= −                             (6.42) n  R ig= 0

The vL(t), iC(t), and ig(t) waveforms are sketched in Fig. 6.33 for continuous conduction mode operation.

Fig. 6.33. Flyback converter waveforms, continuous conduction mode.

Application of the principle of volt-second balance to the primary-side magnetizing inductance yields

V

vL= D(Vg )+ D‘(− ) = 0                    (6.43) n

Solution for the conversion ratio then leads to

V            D Vg          D’

M(D) = = n                                                       (6.44)

So the conversion ratio of the flyback converter is similar to that of the buck-boost converter, but contains an added factor of n.

Application of the principle of charge balance to the output capacitor C leads to

V            I           V R       n          R

i= D(− )+ D‘( − ) = 0                   (6.45)

Solution for I yields

nV D’R

I =                                                             (6.46)

This is the dc component of the magnetizing current, referred to the primary. The dc component of the source current ig is

Ig = i= D(I)+ D‘(0)                       (6.47)

An equivalent circuit that models the dc components of the flyback converter waveforms can now be constructed. Circuits corresponding to the inductor loop equation (6.43) and to node equations (6.45) and (6.47) are illustrated in Fig. 6.34(a). By replacing the dependent sources with ideal dc transformers, one obtains Fig. 6.34(b). This is the dc equivalent circuit of the flyback converter. It contains a 1:D buck-type conversion ratio, followed by a D‘:1 boost-type conversion ratio, and an added factor of 1:n, arising from the flyback transformer turns ratio. By use of the method developed in Chapter 3, the model can be refined to account for losses and to predict the converter efficiency. The flyback converter can also be operated in the discontinuous conduction mode; analysis is left as a homework problem. The results are similar to the DCM buck-boost converter results tabulated in Chapter 5, but are generalized to account for the turns ratio 1:n.

 

 

Fig. 6.34. Flyback converter equivalent circuit model, CCM: (a) circuits corresponding to Eqs. (6.43), (6.45), and (6.47); (b) equivalent circuit containing ideal dc transformers.

The flyback converter is commonly used at the 50 to 100 W power range, as well as in high-voltage power supplies for televisions and computer monitors. It has the advantage of very low parts count. Multiple outputs can be obtained using a minimum number of parts: each additional output requires only an additional winding, diode, and capacitor. However, in comparison with the full-bridge, half-bridge, or two-transistor forward converters, the flyback converter has the disadvantages of high transistor voltage stress and poor cross-regulation. The peak transistor voltage is equal to the dc input voltage Vg plus the reflected load volt V/n; in practice, additional voltage is observed due to ringing associated with the transformer leakage inductance. Rigorous comparison of the utilization of the flyback transformer with the transformers of buck-derived circuits is difficult because of the different functions performed by these elements. The magnetizing current of the flyback transformer is unipolar, and hence no more than half of the core material B-H loop can be utilized. The magnetizing current must contain a significant dc component. Yet, the size of the flyback transformer is quite small in designs intended to operate in the discontinuous conduction mode. However, DCM operation leads to increased peak currents in the transistor, diode, and filter capacitors. Continuous conduction mode designs require larger values of LM, and hence larger flyback transformers, but the peak currents in the power stage elements are lower.

6.3.5 Boost-Derived Isolated Converters

Transformer-isolated boost converters can be derived by inversion of the source and load of buck-derived isolated converters. A number of configurations are known, and two of these are briefly discussed here. These converters find some employment in high-voltage power supplies, as well as in low-harmonic rectifier applications.

A full-bridge configuration is diagrammed in Fig. 6.35, and waveforms for the continuous conduction mode are illustrated in Fig. 6.36. The circuit topologies during the first and second subintervals are equivalent to those of the basic nonisolated boost converter, and when the turns ratio is 1:1, the inductor current i(t) and output current io(t) waveforms are identical to the inductor current and diode current waveforms of the nonisolated boost converter.

 

 

 

Fig. 6.35. Full-bridge transformer-isolated boost converter.

Fig. 6.36. Waveforms of the transformer-isolated full-bridge boost converter, CCM.

During subinterval 1, all four transistors operate in the on state. This connects the inductor L across the dc input source Vg, and causes diodes D1 and D2 to be reverse-biased. The inductor current i(t) increases with slope Vg/L, and energy is transferred from the dc source Vg to inductor L. During the second subinterval, transistors Q2 and Q3 operate in the off state, so that inductor L is connected via transistors Q1 and Q4 through the transformer and diode D1 to the dc output. The next switching period is similar, except that during subinterval 2, transistors Q1 and Q4 operate in the off stare, and inductor L is connected via transistors Q2 and Q3 through the transformer and diode D2 to the dc output. If the transistor off-times and the diode forward drops are identical, then the average transformer voltage is zero, and the net volt-seconds applied to the transformer magnetizing inductance over two switching periods is zero.

Application of the principle of inductor volt-second balance to the inductor voltage waveform vL(t) yields

V

vL= D(Vg )+ D‘(Vg − ) = 0                    (6.48)

n

Solution for the conversion ratio M(D) then leads to

M(D) = =                          (6.49)

This result is similar to the boost converter M(D), with an added factor of n due to the transformer turns ratio.

The transistors must block the reflected load voltage V/n = Vg/D’. In practice. additional voltage is observed due to ringing associated with the transformer leakage inductance. Because the instantaneous transistor current is limited by inductor L, saturation of the transformer due to small imbalances in the semiconductor forward voltage drops or conduction times is not catastrophic. Indeed, control schemes are known in which the transformer is purposely operated in saturation subinterval 1 [13, 15].

A push-pull configuration is depicted in Fig. 6.37(a). This configuration requires only two transistors, each of which must block voltage 2V/n. Operation is otherwise similar to that of the full-bridge. During subinterval 1, both transistors conduct. During subinterval 2, one of the transistors operates in the off sate, and energy is transferred from the inductor through the transformer and one of the diodes to the output. Transistors conduct during subinterval 2 during alternate switching periods, such that transformer volt-second balance is maintained. A similar push-pull version of the Watkins-Johnson converter, converter 6 of Fig. 6.15, is illustrated in Fig. 6.37(b).

Fig. 6.37. Push-pull isolated converters: (a) based on the boost converter, (b) based on the Watkins-Johnson converter.

 

 

 

6.3.6 Isolated Versions of the SEPIC and the Cuk Converter

The artifice used to obtain isolation in the flyback converter can also be applied to the SEPIC and inverse-SEPIC. Referring to Fig. 6.38(a), inductor L2 can be realized using two windings, leading to the isolated SEPIC of Fig. 6.38(b). An equivalent circuit is given in Fig. 6.38(c). It can be seen that the magnetizing inductance performs the energy-storage function of the original inductor L2. In addition, the ideal transformer provides isolation and a turns ratio.

Fig. 6.38. Obtaining isolation in the SEPIC: (a) basic nonisolated converter, (b) isolated SEPIC, (c) with transformer equivalent circuit model.

Typical primary and secondary winding current waveforms ip(t) and is(t) are portrayed in Fig. 6.39, for the continuous conduction mode. The magnetic device must function as both a flyback transformer and also a conventional two-winding transformer. During subinterval 1, while transistor Q1 conducts, the magnetizing current flows through the primary winding, and the secondary winding current is zero. During subinterval 2, while diode D1 conducts, the magnetizing current flows through the secondary winding to the load. In addition, the input inductor current il flows through the primary winding. This induces an additional component of secondary current il/n, which also flows to the load. So design of the SEPIC transformer is somewhat unusual, and the rms winding currents are larger than those of the flyback transformer.

 

Fig. 6.39. Waveforms of the isolated SEPIC, continuous conduction mode.

By application of the principle of volt-second balance to inductors L1 and LM, the conversion ratio can be shown to be

V            nD Vg       D’

M(D) = =                                                            (6.50)

Ideally, the transistor must block voltage Vg/D‘. In practice, additional voltage is observed due to ringing associated with the transformer leakage inductance.

An isolated version of the inverse-SEPIC is shown in Fig. 6.40. Operation and design of the transformer is similar to that of the SEPIC.

 

 

Fig. 6.40. Isolated inverse-SEPIC.

Isolation in the Cuk converter is obtained in a different manner [18]. The basic nonisolatedCuk converter is illustrated in Fig. 6.41(a). In Fig. 6.41(b), capacitor C1 is split into two series capacitors C1a and C1b. A transformer can now be inserted between these capacitors, as indicated in Fig. 6.41(c). The polarity marks have been reversed, so that a positive output voltage is obtained. Having capacitors in series with the transformer primary and secondary windings ensures that no dc voltage is applied to the transformer. The transformer functions in a conventional manner, with small magnetizing current and negligible energy storage within the magnetizing inductance.

 

Fig. 6.41. Obtaining isolation in the Cuk converter: (a) basic nonisolatedCuk converter, (b) splitting capacitor C1 into two series capacitors, (c) insertion of transformer between capacitors.

Utilization of the transformer of the Cuk converter is quite good. The magnetizing current can be both positive and negative, and hence the entire core B-H loop can be utilized if desired. There are no center-tapped windings, and all of the copper is effectively utilized. The transistor must block voltage Vg/D‘, plus some additional voltage due to ringing associated with the transformer leakage inductance. The conversion ratio is identical to that of the isolated SEPIC, Eq. (6.50).

The isolated SEPIC and Cuk converter find application as switching power supplies, typically at power levels of several hundred watts. They are also now finding use as ac-dc low-harmonic rectifiers.

 

Isolation in the Cuk converter is obtained in a different manner [18]. The basic nonisolatedCuk converter is illustrated in Fig. 6.41(a). In Fig. 6.41(b), capacitor C1 is split into two series capacitors C1a and C1b. A transformer can now be inserted between these capacitors, as indicated in Fig. 6.41(c). The polarity marks have been reversed, so that a positive output voltage is obtained. Having capacitors in series with the transformer primary and secondary windings ensures that no dc voltage is applied to the transformer. The transformer functions in a conventional manner, with small magnetizing current and negligible energy storage within the magnetizing inductance.

 

Fig. 6.41. Obtaining isolation in the Cuk converter: (a) basic nonisolatedCuk converter, (b) splitting capacitor C1 into two series capacitors, (c) insertion of transformer between capacitors.

Utilization of the transformer of the Cuk converter is quite good. The magnetizing current can be both positive and negative, and hence the entire core B-H loop can be utilized if desired. There are no center-tapped windings, and all of the copper is effectively utilized. The transistor must block voltage Vg/D‘, plus some additional voltage due to ringing associated with the transformer leakage inductance. The conversion ratio is identical to that of the isolated SEPIC, Eq. (6.50).

The isolated SEPIC and Cuk converter find application as switching power supplies, typically at power levels of several hundred watts. They are also now finding use as ac-dc low-harmonic rectifiers.

x

Check Also

KTU B.Tech Lecture Notes WATER RESOURCES ENGINEERING

KTU B.Tech Lecture Notes WATER RESOURCES ENGINEERING   MODULE I Hydrologic cycle-precipitation-mechanism, ...

KTU B.Tech S5 Lecture Notes Geomatics

KTU B.Tech S5 Lecture Notes Geomatics CE307 Geomatics    CE 307  GEOMATICS  ...