2. Magnetic Losses of Ferrites under Inhomogeneous Winding

A typical wireless power transfer system is illustrated in Figure 3. It contains a full-bridge inverter and rectifier and corresponding compensating topology. The loosely coupled transformer contains a transmitter coil, a receiver coil, and corresponding magnetic cores. In this paper, the transmitter and receiver coils are both solenoid winding. On the primary side, the resonant capacitor C _P connects in series with the transmitter coil, to form the resonant network. On the secondary side, the resonant capacitor C _S connects in parallel with the receiver coil.

FIGURE 3:

Typical wireless power transfer system.

A typical flux distribution of the solenoid structure is shown in Figure 4. The total flux concerns the internal leakage flux, external leakage flux, and mutual flux, among which the internal leakage flux comprises the majority of leakage flux since its path length is much shorter than others.

FIGURE 4:

Flux distribution of the solenoid structure.

Corresponding equivalent magnetic reluctance network is analyzed in Figure 5. As seen in Figure 5, the core is divided into 7 parts in longitudinal direction. In order to clearly demonstrate the magnetic motive force and the magnetic reluctance in each flux path, at least 7 divisions have to be provided. With more divisions, theoretically, we can obtain a more accurate result, but the calculation complexity will increase dramatically. The discretization number is a trade-off between precision and complexity. Each core section is modelled as magnetic reluctance, while core section with excitation winding is modelled as a voltage source in series with magnetic reluctance. The voltage source corresponds to the number of turns and current excitation in the winding, represented by $\alpha \cdot i_p$ in Figure 5.

FIGURE 5:

Equivalent magnetic reluctance network.

A lumped magnetic reluctance model was built in Figure 6, concerning voltage source and reluctance inside the core and in the air.

FIGURE 6:

Lumped magnetic reluctance model.

In the situation of uneven flux distribution, values of parameters {R _l1, R _l2, R _l3, R _l4} and {R _m1, R _m2, R _m3, R _m4} cannot be derived using the empirical equation. FEM simulation is applied once to obtain flux distribution {ϕ ₁, ϕ ₂, ϕ ₃, ϕ ₄}. Substitute the flux values into the model in Figure 6; the magnetic reluctance values can be derived according to Kirchhoff’s voltage law.

In addition, the magnetic reluctance R_c can be calculated as

(1) $\begin{array}{}{R}_c=\frac{l_c}{{\mu }_0{\mu }_r{A}_c},\end{array}$

where l_c is the length of each individual core, μ ₀ is the vacuum permeability, and μ_r is the relative permeability of cores.

The total flux density along y-axis is

(2) $\begin{array}{}B=\frac{\varphi }{A_c},\end{array}$

where A_c is the cross-sectional area of the core in the x-z plane.

After obtaining all of the parameters in the lumped magnetic reluctance model, the magnetic flux density under different working conditions can be acquired:

(3) $\begin{array}{}B=\frac{A^{-1}U}{A_c},\end{array}$

where U is the magnetic motive force (MMF) matrix and A is the magnetic reluctance coefficient.

It is worth noting that the flux density in the primary core is excited not only by the primary winding but also by the secondary winding. By combining the results generated by primary and secondary excitations, the flux density distribution in the primary core can be calculated.

As a result, for cores under sinusoidal current excitation, the magnetic loss can be calculated using the Steinmetz equation:

(4) $\begin{array}{}{P}_V=k\cdot f^{\alpha }\cdot {\hat{B}}^{\beta },\end{array}$

where $\hat{B}$ is the peak induction of a sinusoidal excitation with frequency f, P_V is the time-average power loss per unit volume, and k and α are material parameters which can be obtained from the material datasheet.

By substituting (3) into (4), the magnetic loss in each section can be calculated. Generally, the highest flux density is designed well under saturation; thus, the ferrite usually works in the linear region and the overall magnetic loss can be summed.

3. Influence of Winding Parameters

To investigate the influence of winding parameters, we constructed two coupled coils, each with the same number of turns in total and different winding spaces between each turn. The receiver coil is designed to be homogeneous winding, while the transmitter coil was constructed with different spaces between each turn.

It would be desirable to reduce the magnetic loss while maintaining tight and compact windings. In this paper, different coil winding width ratio combinations were investigated and compared, in terms of coupling coefficient and magnetic loss.

The system configurations are as follows. The magnetic core is made of ultra-low-loss soft magnetic material DMR47. The overall dimension of the core is 500 ∗ 380 ∗ 12 mm, which is formed by small magnetic cubes (50 ∗ 38 ∗ 6 mm). The number of primary and secondary coil turns is both 45 turns. The air gap between primary and secondary coils is 200 mm. The system works at its resonant frequency 50 kHz. The input voltage is 160V and the load of the system is 50 Ω.

The coils were equally divided into 5 portions. The number of portions determines the number of combination possibilities of winding density. With more portions, we can obtain a much more accurate result, but the calculation complexity will increase dramatically. The discretization number is a trade-off between precision and complexity. The current in each section $\alpha \cdot i_p$ corresponds to the number of turns. Serially connect the 5 portions, and calculate the coupling coefficient of the receiver side with the transmitter side. Apply different current in each portion to realize the effects of inhomogeneous winding. A one-row five-column array indicates the current value in 5 portions. As seen in Figure 7, (9 : 9 : 9 : 9 : 9) indicates 9 turns in each portion.

FIGURE 7:

Magnetic field distributions in core with different winding parameters. (a) Homogeneous winding (9 : 9 : 9 : 9 : 9). (b) Winding parameters (10 : 10 : 5 : 10 : 10). (c) Winding parameters (17 : 4 : 3 : 4 : 17).

The receiver coil remains homogeneous winding, while different winding parameters of the transmitter coil were studied to seek for the optimal combination. Typical theoretical results were compared with simulations in ANSYS Maxwell; the effects of inhomogeneous winding were shown in Figures 7(a)–7(c) under the same magnetic induction intensity scale. The simulation results agree well with theoretical analysis, as shown in Table 1.

TABLE 1:Comparison of core loss in theoretical and simulation results.

In order to illustrate the effects of inhomogeneous winding on magnetic loss, the variations of coupling coefficient and core loss are depicted with different winding parameters, as shown in Figure 8.

FIGURE 8:

Variation of core loss and coupling coefficient with different winding parameters.

The horizontal axis represents the coupling coefficient, while the vertical axis is 1/core loss. The desired winding parameters are with high coupling coefficients and low core losses, so points positioned in the top right region are preferred.

As seen from Figure 8, the range of coupling coefficient is limited between 0.118 and 0.122. Homogeneous winding (9, 9, 9, 9, 9) has the worst performance, with the lowest coupling coefficient and highest core loss, compared with other cases with coarse winding in center. Inhomogeneous winding effectively reduced the magnetic loss in the ferrite core. The optimal situation within consideration range, with winding parameter (17, 4, 3, 4, 17), reduced the core loss by 5.6% compared with the homogeneous case, while the coupling coefficient increased by 1.9%. When designing the winding parameters, relative low magnetic field density in the core center helps to reduce the overall core loss.

4. Experimental Result and Discussion

Measurements for wireless power transfer system under inhomogeneous winding were obtained to evaluate whether the power loss reduction found for inhomogeneous winding translated to improve power efficiency well.

Primary coil turns are winded around the core with different spaces between each turn. The total number of turns remains constant, and the working frequency is unchanged, so the copper loss is assumed to be the same, and so is the eddy-current loss. The circuit always works at the soft switching mode, so the switching loss remain unchanged. Therefore, with different winding parameters, the variation in core loss results in the change in system efficiency. The overview of the experiment system is shown in Figure 9.

FIGURE 9:

Experimental setup for wireless power transfer under inhomogeneous winding.

The diagram of setups for measuring is shown in Figure 10. Test waveforms of the system are shown in Figure 11, including the primary current i_p, secondary current i_s, and output voltage of the inverter u_p. u_g represent the gate driving signal for MOSFET in the inverter bridge. The system works under ZVS condition, as not much of a voltage spike is observed in the waveform.

FIGURE 10:

The diagram of the setups for measuring.

FIGURE 11:

Test waveforms of the system.

The experimental and calculation results are compared in Figure 12. Since it is difficult to directly obtain the core loss, the experimental core losses were obtained by subtracting the measured total losses with the measured winding losses by using a LCR meter, the switching device losses, and the diode losses by integrating the voltage and current waveforms using a HDO4034 oscilloscope. The variation of measured core loss agrees well with the calculated results, assuming the winding loss and switching loss remain unchanged under the same frequency. The system power loss significantly reduces as coils are wound relatively coarsely in the center and tightly at two ends.

FIGURE 12:

Variation of core loss with different winding parameters.