Part | NCP1207 |

Category | |

Description | PWM Current-mode Controller For Quasi-resonant Operation |

Company | ON Semiconductor |

Datasheet | Download NCP1207 datasheet |

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Features, Applications |

AND8112/D A Quasi-Resonant SPICE Model Eases Feedback Loop Designs Prepared by: Christophe Basso Prepared by: Joel Turchi ON Semiconductor http://onsemi.com Within the wide family of Switch Mode Power Supplies (SMPS), the Flyback converters represent the structure of choice for use in small and medium power applications. For compact designs and radio-frequency sensitive applications, e.g. TV sets or set-top boxes, Quasi- Resonant power supplies start to take a significant market share over the traditional fixed frequency topology. However, if the feedback loop control is well understood with this latter, for instance via a comprehensive literature and SPICE models, the situation differs for self-oscillating variable switching frequency structures where no model still exists. This article will show how a simple large-signal averaged SPICE model can be derived and used to ease the design work during stability analysis. Quasi-Resonant Operation It is difficult to abruptly dig into the analytical analysis without giving a basic idea of the operation of a converter working in Quasi-Resonance (QR). Figure 1 depicts a typical FLYBACK converter drain-source waveform as you probably have already observed. When the switch is closed, the drain-source voltage VDS is near 0 V and the input voltage Vg appears across the primary inductance LP: the current inside LP ramps up with a slope of Leakage Inductance Plateau: (Vout + Vf)/N Core is ResetWhen the controller instructs the switch opening, the drain-source quickly rises and the energy transfer between primary and secondary takes place: the secondary diode conducts and the output voltage flies back on the primary side, over LP. This "Flyback" plateau is equal (V + Vf) / N, where N is the secondary to primary turn ratio, V the output voltage and Vf the diode forward voltage drop. During this time, the primary current decreases with a slope now imposed by the reflected voltage Figure 2. The Primary Current Ramps Up and Down to Zero in DCMFigure 2 zooms on the simulated primary current (actually circulating in the magnetizing inductor), showing how it moves over one switching cycle. When the primary current reaches zero, the transformer core is fully demagnetized: we are in Discontinuous Conduction Mode (DCM). The primary inductance LP together with all the surrounding capacitive elements Ctot create a LC filter. When the secondary diode stops conducting = 0, the drain branch is left floating since the MOSFET is already open. As a result, a natural oscillation occurs, exhibiting the following frequency value: As in any sinusoidal signal, there are peaks and valleys. When you re-start the switch in one valley, where the voltage is minimum, the MOSFET is no longer the seat of heavy turn-on losses engendered by capacitive effects: this is the so-called Quasi-Resonance operation where the switching frequency depends on the peak current, the various slopes ON and OFF and the number of valleys you choose after the core reset. In our study, we will first concentrate on a simplified SPICE version where the power switch is actuated right after the reset detection point (parasitic ringings are neglected) and later on, a more sophisticated declination will incorporate parasitic delays. Modeling the Switch Network Figure 3 depicts a Flyback topology where the switching elements generating the above waveforms have been highlighted: the power switch (usually a MOSFET transistor) and a diode, performing a rectification job. During the converter operation, the Pulse Width Modulator controller (PWM) instructs the transistor to turn ON, in order to store energy in the primary side. The primary current builds up until the setpoint imposed by the feedback loop is reached. At this time, the controller toggles the transistor to the OFF state and energy transfers to the secondary side. If the ON and OFF states can be described by a set of linear equations, there exists a discontinuity linking these two events. Despite the presence of linear elements in the converter (capacitors, inductors and resistors), the presence of the commuting switch clearly introduces the non-linearity that prevents us from directly writing the small-signal equations... When learning electronic circuits at school, there were some exercises in which we were asked to reveal the transfer function of bipolar amplifiers. At that time, we learned to replace the transistor symbol by its equivalent small-signal model: the schematic turned into the simple association of current and voltage sources that greatly simplified the analysis. In the average circuit modeling technique, we also follow the same philosophy: the exercise lies in isolating and replacing the switch network with a set of current and voltage sources whose electrical architecture do not vary with time. Therefore, plugging the equivalent model back into the converter of interest allows us to resolve its transfer characteristics. Deriving Equations The object of deriving a model consists in writing the equations that describe the switch network averaged input and output quantities that a) depend from each other b) obey to the control input. Let us draw the various waveforms before starting any line of algebra (Figure 4). From this picture, we can develop equations that will finally describe the averaged evolution of the values of interest, the input / output voltage and current of our switch network: where: V is the output voltage, Vg the input voltage, IP the primary peak current, N the / NP turn ratio and d the duty-cycle = 1 d). Please note that in this first approach, we do not consider any delay occurring at the switch opening or induced by equation 3. These events will considered later on, in a more complex model. Figure 3. A Flyback Power Supply where Switches have been Isolated0Averaging Input / Output Voltages From the inductor volt-second balance approximation, we know that the average voltage across an inductor operated in a steady-state converter is null. By looking at the V(LP) sketch, we obtain the following equation: t V(LP) u+ d(t) t Vg(t) u * d(t) t V(t) u + d(t) N t Vg(t) (1 * d(t)) N t V(t) u +0which lets us extract the classical output / input voltage ratio Now, by plugging equation 10 in equation 6, we obtain the average voltage across the primary switch terminal: <V1(t)> = t V(t) Vg(t) (1 * d(t)) + t V(t) Vg(t) u V(t) ut +t Vg(t) uwhich agrees with the inductor volt-second balance approximation (from Figure 1 since, by definition, <V(LP)> = 0, then Vg appears across the switch terminals). To reveal <V2(t)>, let us plug equation 10 into <V2(t)> = [t V(t) Vg(t) u] d(t) + [t V(t) Vg(t) u] t V(t) u +t V(t) u t V(t) Vg(t) uwhich again could be deduced from Figure 3 since the average voltage across the secondary inductance is zero... Averaging Input / Output Currents The peak inductor current depends on the time during which Vg is applied over LP. If we recall that this time (actually ton d x TS, then: From Figure 4, the average current <I1(t)> can be obtained by evaluating the triangular area (charge in Coulomb) and dividing by the switching period. This is expressed by equation 4. Now plugging equation 4, we obtain: however, from equation 11, we know that <V1(t)> = <Vg(t)> thus equation 14 turns into:A 100% Efficiency Power Transfer... Assuming that 100% of the primary stored energy is released to the secondary side, then we can use equations 11 and 12 to write: Applying the same technique to the secondary current I2(t), leads to:From equation 15, we can see that a current is generated by a voltage multiplied by a term. This term is obviously homogenous to the inverse of an impedance. By re-arranging equation 15, we obtain: |

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