## Friday, September 8, 2017

### Field Weakening, Part 1

Previously on Motor Diddlers, we learned how to optimize the torque produced by an IPM operating in the current-limited regime. We can't stay in this regime forever; at higher RPM's, all motors enter a voltage-limited operating regime.

What's surprising is how quickly IPM's become voltage-limited. Using the data from the last post, we can plot the maximum achievable current versus speed:

The "base speed" of the motor is very low, about 800 rad/s (2500 RPM). Furthermore, we quickly run out of volts past base speed; the motor cannot turn much faster than 1500 rad/s (5000 RPM) if we constrain ourselves to the MTPA trajectory. This is a result of the much higher inductance of an IPM; at high electrical frequencies this inductive impedance limits how much current we can put into the stator.

Fortunately, we can use this higher inductance to our advantage. Recall that $$V_q=R_s I_q+\omega L_d I_d+\omega\lambda$$; this means that if $$I_d$$ is negative, we can cancel out the $$\omega\lambda$$ term (what would conventionally be called "back EMF" in a surface PM machine) in the expression for $$V_q$$. On a surface PM machine, this current would be wasted; however, if $$L_d < L_q$$, the $$(L_d-L_q)I_d I_q$$ term in the torque equation will generated positive torque! Furthermore, the $$L_d/\lambda$$ ratio is often an order of magnitude higher for IPM's, which greatly reduces the amount of d-axis current required to cancel out the flux linkage. This is, in a nutshell, why IPM's field weaken much better than their surface PM counterparts.

It is fairly straightforward to compute the optimal field-weakening trajectory:

Starting from the motor equations $$\begin{array}{lcl} \tau=\frac{3}{2}n_p(\lambda I_q+(L_d-L_q)I_d I_q)\\ V_d=R_s I_d-\omega L_q I_q\\ V_q=R_s I_q+\omega L_d I_d+\omega\lambda\\ V_s=\sqrt{V_d^2+V_q^2}\\ I_s=\sqrt{I_d^2+I_q^2} \end{array}$$ we note that in the voltage limited operating regime, maximum torque must be achieved when the voltage vector is on the boundary of the allowable area, in which case the optimization problem becomes an equality: $$\begin{cases} \frac{3}{2}n_p(\lambda I_q+(L_d-L_q)I_d I_q) = \tau_0\\ (R_s I_d-\omega L_q I_q)^2 + (R_s I_q+\omega L_d I_d+\omega\lambda)^2 = V_0^2 \end{cases}$$ If we ignore saturation, this system is the intersection of a constant-torque hyperbola (which is independent of speed) and a series of shrinking ellipses.

This system is polynomial (and in fact only a quartic) and can be solved in many ways. For example, one element of the reduced Groebner basis of the ideal generated by the two equations is the very long $$(L_d-L_q)^2(R_s^2+L_q^2w^2)I_q^4 + (L_q^2\lambda^2\omega^2+R_s^2\lambda^2+(L_d-L_q)^2(2R_s\tau_0\omega-V_0^2))I_q^2- 2\lambda\tau_0(R_s^2+L_d L_q\omega^2)+ R_s^2\tau_0^2+L_d^2\tau_0^2\omega^2$$ where we have included the factor of $$3/2n_p$$ in $$\tau_0$$ for brevity's sake. The roots of this polynomial are easily found with a variety of numeric or analytic methods; in the case of multiple real solutions the correct one is the $$(I_d,I_q)$$ vector with the shortest length.
Unfortunately, the system is no longer polynomial if the motor saturates (that is, $$L_d$$ and $$L_q$$ are functions $$l_d(I_d,I_q)$$, $$l_q(I_d,I_q)$$ of the axis currents). In order to solve the system in this case, we will have to turn to more complicated (and less reliable) numeric methods, the nature of which will be the subject of the next post in this series.