Appendix K REVIEWED

This is my original writeup of this appendix, it is now all installed. Appendix K : Line Parameters: Comparison of Network and Maxwell Views 1 (a) The Network Model 1 (b) Characteristic Impedance in the Network Model 1 (c) Characteristic impedance computed from Maxwell's Equations 3 (d) Low frequency case (no skin effect) 4 (e) High frequency case for round conductor (strong skin effect) 5 Appendix K : Line Parameters: Comparison of Network and Maxwell Views (a) The Network Model The usual model of a transmission line is an infinite repetition of differentially small R,L,C,G segments as shown here between the vertical red lines, . Fig K.1 This is of course electrically identical to the following Fig K.2 where R = R1 + R2 and L = L1 + L2. In the circuit diagrams, it is implied that R,L,C,G are all quantities per unit length of the transmission line. Thus, if the distance between the two red lines is δ, the values of the lumped parameters in Fig K.2 are Rδ,Lδ,Cδ,Gδ. For example, if δ doubles, the total conductance of the segment doubles since it is a measure of current flowing between the conductors. The model implied by the picture is then the limit as δ→0. We wish to compare these parameters R,L,C,G with our parameters calculated from Maxwell's equations. (b) Characteristic Impedance in the Network Model The first step to this end is to compute the impedance Zin one would see looking into the left end of the above "two-port network" consisting of a single segment terminated by some impedance Zt. If we set this computed impedance Zin equal to Zt, the resulting Zt must then be the "characteristic impedance" of the infinite transmission line looking in from the left end. The impedance of a capacitor C and inductor L operating at frequency ω is determined by Q = CV => I = ∂tQ = C∂tV => I = jωCV => ZC = V/I = 1/(jωC) V = L∂tI => V = jωLI => ZL = V/I = jωL . (K.1) If we momentarily set δ = 1, then using the usual circuit rules for computing impedance we see that Zin = (1/G) || ZC || (R+ZL+ Zt) ZC = 1/(jωC) ZL = jωL . since these three elements are in parallel. For parallel elements, since all have the same voltage Vin, it is easier to add up the inverse impedances ("admittances"), which basically adds up the three currents to get the total current (a fact easily shown) so then Zin-1 = G + ZC-1 + (R + ZL + Zt)-1 or Zin-1 = G + jωC + (R + jωL + Zt)-1 . (K.2) To find the characteristic impedance we set Zin = Zt = Z0 to get Z0-1 = G + jωC + (R + jωL + Z0)-1 . (K.3) Now we reinstall our δ factors to get Z0-1 = (G+jωC)δ + (K.4) or [(R+jωL)δ + Z0] Z0-1 = (G+jωC)δ [(R+jωL)δ + Z0] or [(R+jωL)δ + Z0] = (G+jωC)δ [(R+jωL)δZ0 + Z02] . (K.5) We enter into Maple the equation in the form (K.4). The two quadratic solutions go into array elements s[1] and s[2], and s[1] gives the physical solution. This result includes terms of order δ0, δ and δ2 and we then take the limit δ→0 simply by setting δ = 0. The extra Maple commands are just guides to help Maple obtain the result in a simple form. Thus we arrive at the famous result for the characteristic impedance of a transmission line in the network model described above, Z0 = . (K.6) (c) Characteristic impedance computed from Maxwell's Equations The main results of Chapter 4 appear in summary box (4.11.30) from which we quote in part, = - z i(z) where z = R + jωL transmission line equations = - yV(z) (4.11.11) y = G +jωC (4.11.12) z = Zs1 + Zs2 + jωLe (4.11.13) XL ≡ ωLe , XC ≡ 1/(ωC) y = jωC' = jωC + (σ/ε)C (4.11.20) G = (σ/ε)C (4.11.21) R = Re(Zs1+ Zs2) L = Le + (1/ω) Im(Zs1+ Zs2) Le = (μ/4π)K (4.11.25) and (4.11.26) C = 4πε/K (4.11.22) G = 4πσ/K (4.11.22) + (4.11.21) (K.7) Assuming the transmission line carries a wave of the usual form ej(kz-ωt), we know that V(z) = V(0)e-jkz => ∂zV(z) = jkV(z) i(z) = i(0)e-jkz => ∂zi(z) = jki(z) . (K.8) Thus the transmission line equations above may be written jkV = - z i jk i = - yV . (K.9) Multiply the first by i and the second by V and subtract the resulting equations to get 0 = - z i2 + yV2 => z i2 = yV2 => (V/i)2 = z/y (K.10) Therefore we find that the characteristic impedance of the infinite transmission line is Z0 = V/i = = (K.11) where R,L,G,C are the parameters computed from Maxwell's equations. Since this result agrees exactly with our network computation, we conclude that these R,L,G,C parameters are the same in both the Maxwell and network models. Thus, we make the connection between the network parameters and the Maxwell calculation parameters as follows: R = Re(Zs1+ Zs2) L = Le + (1/ω) Im(Zs1+ Zs2) Le = (μ/4π)K G = 4πσ/K C = 4πε/K (K.12) where K is the dimensionless real integral in Chapter 4, see (4.4.8). Recall that this integral requires knowledge of both the conductor geometry as well as the normalized Jz current distributions inside the conductors. Here ε, μ and σ are for the dielectric between the conductors. (d) Low frequency case (no skin effect) At low frequencies where there is no skin effect, the conductor current densities are uniform, so that Jz = I/area for each conductor. In Chapter 2 for a round conductor C1 at low frequency we found that Zs(ω) = + jω // low frequency limit (2.4.12) => Re(Zs) = and Im(Zs) = ω . (K.13) From (K.12) we then find that for low frequencies and round conductors, R = + = Rdc1 + Rdc2 (K.14) L = Le + ( + ) = Le + (Li1 + Li2) . (K.15) In this case parameter R is just the sum of the DC resistances of the conductors (per unit length), and parameter L is the sum of the external inductance Le and the internal inductances of the two wires. Here σi and μi are for the material from which conductor Ci is constructed. The external inductance Le can be interpreted as the inductance of the red wire loop below, Fig K.3 The sides of the red loop make contract on any line on the conductor surfaces, though here we show it having its minimal size. The red loop may in fact be replaced by any loop, possibly non-planar, which captures all the external magnetic flux passing between the conductors. See Fig 4.11 and discussion there. Although we have not formally proven it, it seems clear that for arbitrary conductor cross sections the following equations will apply at low frequency : R = + Ai = cross section area of Ci (K.16) L = Le + (Li1 + Li2) . (K.17) Appendix C computes the DC Li for various conductor cross section shapes. One result quoted there from the literature is that for a square conductor, Li = (μi/8π) [0.96639] . (C.4.11) Thus the Li for a square cross-section conductor is barely different from that of a round conductor. (e) High frequency case for round conductor (strong skin effect) At high frequencies there is a pronounced skin effect. In Chapter 2 for a round conductor C1 at high frequency (and with a symmetric current distribution) we found that Zs(ω) ≈ (1+j) δ1 << 16a1 (2.4.16) Re(Zs) = Im(Zs ) = where here δ1 is the skin depth δ1 = and a1 is the wire radius. From (K.12) we find that for high frequencies and round conductors, R = + L = Le + (1/ω) Im(Zs1+ Zs2) = Le + (1/ω) R . (K.18) In this case, we recognize 2πa1δ1 as the effective current carrying cross-sectional area of round conductor C1, so the expression for R is quite intuitive. Since, δ ≡ => 1/δ = and 1/ω = μ1σ1δ12/2 (K.19) we may write Li(ω) = (1/ω) Im(Zs) = (1/ω) = (1/ω) = (K.20) so Li(ω) ~ 1/. Expressing Li instead in terms of δ1 we find Li(δ1) = (1/ω) Im(Zs) = (1/ω) = μ1σ1(δ12/2) = μ1 (1/4π) (δ1/a1) = [ 2 (δ1/a1) ] . (K.21) The DC internal inductance of a thin shell of radius a and thickness d is shown in Appendix C.6 to be Li = μi (d/a) = [ (4/3)(d/a) ] thin shell, valid for d << a (C.6.8) so the high frequency internal inductance of a round wire is the same as the DC internal inductance a shell of thickness d = (3/2)δ. This is perhaps reasonable since for the DC shell Jz is uniform over distance d, but for the skin effect case Jz decays down to 1/e in distance δ. On the other hand, for the DC current interpretation above, this 1/e drop-off is offset by the fact that some current still exists inside the skin depth δ. In any event, the above expression (C.6.8) shows that the inductance of a thin cylindrical shell is linear in the shell thickness d, so we expect that the high frequency Li of a round wire should be linear in δ, and thus proportional to 1/. Section 2.5 shows how to handle non-round conductors and non-symmetric current distributions by replacing 2πa by an effective active perimeter D. For the special case of Chapter 6, everything can be computed exactly.