
Citation: | Yanhua Peng, Hui Xu, Shuo Cui, et al., “A novel method to acquire circuit transmission characteristics by noncontact power injection and detection,” Chinese Journal of Electronics, vol. x, no. x, pp. 1–13, xxxx. DOI: 10.23919/cje.2024.00.148 |
To address problematic circuit transmission characteristics, test terminals are needed. In this study, an innovative method for determining the transmission characteristics of circuits by employing two semirigid coaxial probes with a T-shaped structure for signal injection and detection is developed. Initially, the proposed method can obtain circuit characteristics from 100 kHz to 10 GHz with a separation distance between the probes greater than 28 mm and a separation distance between the microstrip lines at the location of the injected and detected signals greater than 1.6 mm. Subsequently, an equivalent circuit model is proposed and validated through a 10 GHz measurement on a microstrip line, obtaining the root mean square error (RMSE) is 0.14 dB. Furthermore, the methodology is applied to measure the gain of a low-noise amplifier across frequencies from 100 MHz to 10 GHz. The maximum error is less than 1.66 dB, and the RMSE is 0.58 dB. Additionally, the transmission loss of parallel microstrip lines is investigated within the 3 GHz range, yielding the RMSE is 0.8 dB. The proposed approach enables precise testing of circuit transmission characteristics and facilitates the extraction of circuit equivalent parameters.
As the frequency and operational rate of integrated circuits increase, and their complexity also increases. It thus becomes imperative to precisely quantify the transmission characteristics of circuits at each node within a processed printed circuit board (PCB) [1]–[4].
To accurately obtain the characteristics of a transmission line, scholars usually test it with the help of a vector network analyzer (VNA). In such a test, the PCB is connected to the VNA through a direct port connection, and characteristics such as the S-parameters of the transmission line on the PCB are acquired [5], [6]. In addition, several efforts have been made to determine the characteristics of the transmission line via time-domain reflection, in which one end of the PCB is connected to a time-domain pulse signal and the other end is connected to a standard load, and the characteristics of the transmission lines are obtained via the reflected signal [7], [8].
Although these methods can be used to test the characteristics of transmission lines, it is necessary to ensure that such test lines have connecting terminals. However, as shown in Figure 1, circuits that have already been soldered may include many interconnecting transmission lines without test terminals, and characterization using the above methods would require unacceptable disruption of the corresponding circuit structures. Therefore, the advantages of near-field measurements with noncontact circuits make this method worthy of consideration for solving the above problems [9]–[11].
In near-field inspection methods, the radiation characteristics of a circuit are usually obtained by controlling a near-field probe to perform a near-field scan on the PCB [12], [13]. Some efforts have also used two probes for near-field measurements to verify the measurement efficiency [14], [15] and have used the measurements of one of the near-field probes as a reference to obtain more radiative characteristics of the PCB [16].
In the above processes, the near-field electric and magnetic field probes passively receive the radiation signal from the PCB. The electromagnetic radiation characteristics of the PCB must be accurately recognized. Accordingly, efforts have proposed electric and magnetic field calibration factors (CFs) [14], which are used to calculate the true electromagnetic field at the current position from the measurement results. In [17], [18] and [19], near-field broadband high-resolution electric and magnetic field probes of a PCB structure were used to measure near-field radiated signals from the PCB.
In addition, for relatively simple structures such as semirigid coaxial probes, the coupling capacitance between the probe and the PCB can be further determined based on a CF. In [20] and [21], a waveform transmitted on a signal line was obtained with the help of a coupling capacitor after near-field detection.
Furthermore, semirigid coaxial probes have been used in many works for the near-field active injection of signals into PCBs because of their higher voltage resistance characteristics than those of PCB-structured probes [22]. In [23], a near-field injection platform based on semirigid coaxial probes was designed, and injection experiments in the 1 GHz range were performed on the circuit. In [24], a 6 GHz semirigid coaxial probe was used to inject broadband signals into the PCB, and the waveform relationship between the probe input port and the PCB output port was also calculated using coupling capacitance.
In the above works, semirigid coaxial probes were mainly used for near-field signal injection, while probes of PCB structures were mainly employed for near-field detection. Furthermore, these probes were structured as passive signal measurement sensors alone or for active signal injection, which enabled the performance of near-field radiation source identification or electromagnetic immunity analyses of PCBs.
Therefore, to analyze the transmission characteristics of a circuit without destroying the circuit structure, a novel method using dual probes is proposed. In the characterization process, one probe is used for active signal injection, and the other probe is used for signal detection.
In this process, the voltage resistance and resolution of signal injection and detection must be balanced. Thus, a novel T-shaped semirigid coaxial probe is designed here. Compared with the conventional probe structure, the newly designed probe offers excellent spatial resolution while ensuring broadband characteristics.
Moreover, an equivalent circuit model is developed for characterizing the proposed method. According to the proposed model, after obtaining the response curve of the probe, the equivalent coupled circuit parameters of the probe can be calculated. Then, using the test results of the dual probes, the tested PCB transfer characteristics and the specific equivalent component parameter values are obtained. Therefore, assessing whether the performance of the test circuit satisfies a given set of application requirements is a straightforward process.
The remainder of this article is organized as follows. Section II describes the noncontact power injection and detection methods. According to the proposed method, Section III simulates and tests the performances of the proposed probe. In Section IV, the effectiveness of the proposed method is evaluated using a PCB with known parameters. In Section V, to verify the feasibility of the proposed method, the gain of the low-noise amplifier (LNA) and the transmission characteristics of the parallel microstrip lines (MLs) are measured. Finally, a summary is presented in Section VI.
To accurately characterize the PCB and obtain an equivalent circuit model, an overall noncontact signal injection, and detection structure is constructed, as shown in Figure 2. The injection probe couples the signal generated by the signal source into the PCB, and then the detection probe obtains the signal radiated via PCB transmission.
In the process as shown in Figure 2(a), the signal injected from the injection probe is denoted as X(ω), the injection and detection probes are defined as Hi(ω) and Hd(ω), the coupling between the injection probe and the test PCB is denoted as Hp1(ω), the transmission characteristics of the signal in the PCB is Hline(ω), the coupling between the PCB and the detection probe is Hp2(ω), and the final output is Y(ω). These relationships can be expressed as follows:
Hline(ω)=Y(ω)X(ω)Hi(ω)Hp1(ω)Hd(ω)Hp2(ω). |
(1) |
where, ω denotes the angular frequency, which is related to the frequency f by ω=2π×f.
Since the relationship between X(ω) and Y(ω) can be expressed when using VNA for testing:
Y(ω)=X(ω)S21. |
(2) |
Eq.(1) can be further expressed as:
Hline(ω)=S21Hi(ω)Hp1(ω)Hd(ω)Hp2(ω). |
(3) |
The circuit equivalent model of the structure is shown in Figure 2(b). The injection and detection probes are equivalent to coaxial cables, and the impedances of these probes are Z1 and Z2, The coupling impedance between the signal structure of the injection probe and the reference ground is equivalent to a series connection between capacitor C2 and resistor R1 (the capacitor C4 in series with resistor R2 for the detection probe). The coupling between the injection probe and the test PCB circuit is equivalent to capacitance C1 (the coupling of the detection probe is capacitance C3). To solve for PCB characteristics, the components are modeled as a combination of multiple groups of inductors, resistors, and capacitors [20].
To obtain the transmission characteristics Hline(ω), the remaining part of Eq.(1) needs to be solved with the input signal X(ω) and the output signal Y(ω) determined. The main focus is on the calculation of Hp1(ω)Hi(ω) and Hp2(ω)Hd(ω).
The injection probe needs to couple the signal into the PCB, which is consistent with the process in [24]. As shown in Figure 3(a). The current ii(ω) of the signal injected into the PCB from the probe can be expressed as:
ii(ω)=ig(ω)+io(ω). |
(4) |
where io(ω) is the signal that eventually reaches the PCB. ig(ω) is the current at the output after the probe is coupled to the ground. Kirchhoff’s laws are used to calculate the current, and the following equation can be obtained:
ii(ω)=Vi(ω)−Vg(ω)Z1ig(ω)=Vg(ω)R1+1jωC2io(ω)=(Vg(ω)−Vo(ω))×jωC1. |
(5) |
Since the signal Vi(ω) injected by the injection probe is greater than or equal to Vg(ω), we consider the variable n(ω) such that Vi(ω)=n(ω)×Vg(ω), where |n(ω)|≥1. The relationship between the voltages can thus be expressed as:
Hp1(ω)Hi(ω)=Vo(ω)Vi(ω)=Vo(ω)n(ω)×Vg(ω)Hp1(ω)Hi(ω)=1n(ω)−n(ω)−1jωZ1C1×n(ω)+C2(C1+jωC2C1R1)×n(ω). |
(6) |
As shown in Figure 3(b), the detection probe is coupled to the radiated signal of the PCB [25], [26]. The current ii1(ω) of the signal coupled from the PCB to the probe can be expressed as:
ii1(ω)=ig1(ω)+io1(ω). |
(7) |
In conjunction with the previous analysis of the injection probe, the following relationship exists when detecting the probe operation:
ii1(ω)=(Vi1(ω)−Vg1(ω))×jωC3ig1(ω)=Vg1(ω)R2+1jωC4io1(ω)=Vg1(ω)−Vo1(ω)Z2. |
(8) |
Since the detection signal Vo1(ω) output from the detection probe is less than or equal to Vg1(ω), we use the variable m(ω) such that Vo1(ω)=m(ω)×Vg1(ω), where |m(ω)|≤1. The relationship between the voltages can thus be expressed as:
Hp2(ω)Hd(ω)=Vi1(ω)Vo1(ω)=Vi1(ω)m(ω)×Vg1(ω)Hp2(ω)Hd(ω)=1m(ω)+1−m(ω)jωZ2C3×m(ω)+C4(C3+jωC3C4R2)×m(ω). |
(9) |
For the injection probe to inject more signals into the PCB, as well as for the detection probe to couple more PCB signals, it can be seen from Hp1(ω)Hi(ω) and Hp2(ω)Hd(ω) given in (6) and (9) that it is necessary to ensure a coupling of large capacitances C1 and C3 and small capacitances C2 and C4.
The values of C1 and C3 are mainly determined by the PCB and the probe port. C2 and C4 are determined by the distance between the inner conductor of the probe and the ground of the outer conductor. As shown in Figure 4, the probe and the transmission line on the PCB are equated as two metal bodies, and the capacitance between them can be approximated as:
C∝2εrl4πkd. |
(10) |
where r is the radius of the conductor at the probe port, l is the conductor length, d is the distance between parallel classes, and ε and k are the permittivity and electrostatic force constant, respectively.
This section presents the design of the injection and detection probes involved in the proposed model. The characteristics of the proposed method were tested to ensure the subsequent identification of PCB characteristics.
Considering that the near-field probes used in the proposed method need to guarantee high injection efficiency, large withstand voltages, and high sensitivity, the SR-141-M17 [27] semirigid cable is used as the base element of the probe, and the directionality of the probe is further enhanced by adding additional conductors to the output port of the center conductor.
A full-wave model of the probe is shown in Figure 5. This model includes a near-field probe, a wide bandwidth PCB circuit, and end launch connectors. Port 1 of the probe and port 2 and port 3 of the PCB are included in the whole model. The three ports in the model satisfy the following S-parameter correlation:
S=[S11S21S31S12S22S32S31S23S33]=[S11S21S21S21S22S32S21S23S22]. |
(11) |
According to (11), the S-parameter matrices of the injection and detection probes are the same. Therefore, the simulation results of the injection probe are used as the basis for the final performance of the two probes.
As shown in Figure 5, the probe comprises a semirigid cable with an outer conductor diameter of D1=3.58 mm, a dielectric diameter of D2=2.99 mm, a center conductor radius of r=0.46 mm, and an added conductor with a length of l and a radius of r.
First, the length of the semirigid cable is fixed at a constant l1=20 mm. Then, to reduce the coupling capacitance between the center conductor and the outer conductor, l3 is fixed to 3 mm. The probe is fixed at 0.5 mm from the PCB, the frequency range is from 100 kHz to 10 GHz, and
As shown in Figure 6, the whole simulation process is divided into three steps. Firstly, after determining the parameters of the probe, S21 from port 1 to port 2 in Figure 5 is first obtained. Then, according to Figure 2(b), the equivalent circuit model is established in ADS software. Finally, the optimization algorithm of ADS software is used to acquire the equivalent S21 curve and the corresponding circuit parameters.
As shown in Figure 7, the length of l2 is fixed to 0 mm, and the length of l is varied from 2 mm to 14 mm. Therefore, from the first step of the simulation process, obtaining S21 under different l is available. Differences are made between S21 at different lengths l and S21 of the structure without the additional conductor, and the results obtained are defined as the gains. As the length l increases, the gain in the lower frequency band increases.
Above the frequency of 6 GHz, the gain becomes weaker after l≥8 mm. After the third step of the simulation process is completed. The capacitance parameters at different lengths can be obtained.Since the equivalent parameters have the smallest R1 and R2 at l=8 mm, the coupling capacitance almost no longer increases. Therefore the l of the probe is selected as 8 mm by combining the above simulations.
As shown in Figure 8, the length of l2 is designed to vary from 0 mm to 3 mm to analyze the variation in the transmission characteristics at different lengths. The differences between S21 of l2 other lengths and S21 of l2=3 mm are defined as the gains. As the length increases, the gain difference with respect to l2=3 mm decreases. However, C1 and C3 remain essentially unchanged, but C2 and C4 slowly increase. Therefore l2 is determined to be 0 mm.
Frequency range: As shown in Figure 9, the probe is kept parallel to the direction of the ML. Port 1 of the VNA is connected to the probe, port 2 of the VNA is connected to one end of the ML, and the other end of the ML is connected to a 50 Ω load. The VNA completes the measurements according to segmented settings. 201 points from 100 kHz to 20 MHz,
As shown in Figure 10, the signal injection response factor S21 (referring to the model in Figure 5) obtained from the simulation and the measurement match well. Starting at the frequency of 100 kHz, the S21 of the probe increases rapidly, reaching −40 dB at 400MHz and −30 dB at 1.6 GHz, and then remains stable in the higher frequency range. The difference (the result of subtraction) obtained from simulation and measurement is less than 2.8 dB. These test results show that the proposed method has broadband characteristics and good stability when injecting and detecting signals.
Coverage of signal injection and detection: The coverage of the method is defined as the distance of 6 dB from the maximum power position [25], [28], [29]. The radio frequency signal source SMA100B and the spectrum analyzer (SA) FSV3044 settings are consistent with the directionality of the signal injection and detection. The probe is controlled to move in the direction perpendicular to the ML (X-direction) in steps of 0.1 mm. The test results in Figure 11 fully show that the probe covers within 1.6 mm in the range of 10 GHz. Therefore, it is necessary to ensure that there are no other MLs present in the X-direction of both the injection and detection probes during noncontact signal injection and detection.
Suitable distance of the probes for the proposed method: The injection and detection probes are fixed at 1 mm from the ML. Port 1 of the VNA is connected to the injection probe, and port 2 is connected to the detection probe. The VNA is set to scan
The distance pd between the injection probe and the detection probe starts at 33 mm and approaches incrementally by 1 mm, as shown in Figure 12. As pd decreases, a coupling capacitance forms between the two probes and gradually increases. When pd is less than 28 mm, the capacitance becomes large enough to affect the original signal, causing resonance in the transmission curve and rendering the proposed method inoperative.
Influence of the height d between the probe and the PCB: As shown in Figure 4, the distance d between the probe and the PCB influences the coupling capacitance during signal injection and detection. Different d values affect the magnitude of the injected and detected signals. The distance pd is fixed at 40 mm. By adjusting d from 0.5 mm to 3.5 mm in 0.5 mm steps to obtain the response curves of the injection and detection probes at different distances, the height range suitable for the proposed method is obtained.
As shown in Figure 13, as d increases, the coupling capacitance between the probe and ML decreases, resulting in a weaker response between the detection and injection probe. When d is greater than 2 mm, the detection probe cannot accurately acquire the injection signal. Therefore, the d should be less than 2 mm during the measurement process.
It is important to note that all the above measurements are conducted to ensure that the injection and detection probes are aligned in parallel with the ML on the PCB to achieve optimal coupling capacitance for maximum signal injection and detection efficiency.
While validating the proposed method, it is preferable to obtain the equivalent coupling parameters of the injection probe and the detection probe. Then, the identification of the circuit characteristics can be performed by combining the relationship between the input and output signals.
To validate the proposed method, a PCB with known circuit structure parameters is tested to determine the equivalent circuit parameters of the injection probe and the detection probe. Then, the injection and detection probes are simultaneously placed into the circuit, and the S-parameters are obtained via VNA. These results are compared with those of the equivalent circuit structure to verify the accuracy of the methodology. Therefore, the equivalent parameters of the circuit with a known structure are obtained.
To ensure a solid connection between the probe and the entire measurement system, copper foil is employed to envelop the probe, thereby guaranteeing proper alignment of the probe’s outer conductor with the reference ground of the entire system.
As shown in Figure 14, the injection probe and the detection probe were placed 0.5 mm directly above the ML, and the distance between the two probes was 35 mm. The PCB has an RO4003C substrate with a thickness of 32 mils, a width of the ML of 1.69 mm, and a height of 35 μm. The two ports of the PCB are connected using end-launch connectors with two 50 Ω loads.
Ultimately, an equivalent circuit model is created, as shown in Figure 2(b). During the model parameter determination, the VNA is set up to output signals from 100 kHz to 10 GHz with 15 dBm power and
In step 3, as shown in Figure 14, the signal from port 1 of the VNA is injected into the circuit through the injection probe, and then the output of the detection probe is connected to port 2 of the VNA, thereby obtaining the response curve of the whole link. Then, the equivalent model of the whole link is established. The two probes with equivalent parameters and the PCB were replaced with a transmission line model. Finally, the response curve obtained from the test is used as the final optimization result to obtain the equivalent parameters of the PCB. The accuracy of the proposed method is determined by comparing it with curves obtained from the model.
As shown in Figure 15, the results obtained by equivalent circuit modeling are in good agreement with the measurements. In the model, Z1 and Z2 are characterized using the inductance. Therefore, the equivalent circuit parameters of the probes must be recorded in Table 1.
Component Number | Value | Component Number | Value |
Z1 | 1.51 nH | C3 | 0.3 pF |
C1 | 0.28 pF | Z2 | 1.3 nH |
R1 | 0.8 Ω | Rl1,Rl2…,Rl6 | 0.11 Ω |
C2 | 2.1 pF | Ll1,Ll2…,Ll6 | 0.05 nH |
R2 | 0.01 Ω | Cl1,Cl2…,Cl6 | 0.001 pF |
C4 | 0.09 pF |
The root mean square error (RMSE), as a metric for measuring the accuracy of actual data, is utilized here to characterize the differences between the proposed method and the conventional measurement approach. The formula for calculating the RMSE is as follows:
RMSE=√∑ni=1(Pi−Ci)2n. |
(12) |
here, n represents the number of samples, Pi denotes the measured value of the proposed method, and Ci represents the measurement value of the traditional method. As shown in Figure 16, based on Table 1, the S-parameters between the injection probe and the detection probe in the equivalent circuit are obtained. In addition, the actual S-parameters of both probes can be measured by the VNA test. By setting the VNA to generate high power, larger X(ω) and Y(ω) of (1) are guaranteed, which effectively prevents the signal from being too small and causes it to drown in noise. As shown in Figure 16, the maximum difference is 1.79 dB at 4 GHz, and the RMSE is 0.64 dB.
The PCB with known characteristics is shown in Figure 14 is modified into an equivalent structure consisting of multiple sets of inductors, resistors, and capacitors, as shown in Figure 2(b). Combining the response curves between the injection probe and the detection probe obtained from the test, the values of each component in Table 1 can be determined (we use six groups of inductors, resistors, and capacitors for the equivalent [20]). The probes’ inherent impedances Z1 and Z2 are equivalent to the inductance, thus the unit henry (H) is employed.
As shown in Figure 17, comparing the transmission function of PCBs with known parameters obtained from VNA tests reveals that the equivalent model of the proposed method is consistent with the transmission loss characteristics of the actual circuit structure. For the tested PCB structures, the error between the VNA test result and the equivalent model result is less than 0.24 dB, and the RMSE is 0.14 dB.
The above measurements and simulation results verify the effectiveness of the proposed method.
Broadband LNAs are an integral component of many receiver devices, radar systems, and communications equipment[30]. LNAs are typically placed at the front of a system circuit for weak signal amplification or in the middle for general signal amplification. Because these circuits have been processed to differentiate the performance of the amplifier from that predicted via theory, it is necessary to test the actual performance of the amplifier (especially its gain characteristics). Corresponding and conventional test methods require the addition of test terminals at the input and output of the LNA, which destroys the circuit structure.
Therefore, in this subsection, the proposed method is used to test the gain of an LNA, and its feasibility is evaluated by comparing the results with those of a conventional direct port test.
As shown in Figure 18, the TLLA0.1G18G-30-25 LNA [31] is selected for testing. Since the LNA is sealed by the case, the ML from Figure 14 is used to connect to the port of the LNA. In this configuration, the coupling parameters of the injection and detection probes are consistent with those discussed in the previous sections.
In the test, the signal at port 1 of the VNA is coupled to the ML structure through the injection probe and passed through the board to the input of the LNA. The signal is amplified by the LNA and output to the ML, which is connected to port 2 of the VNA through the detection probe. The LNA operates from 0.1 GHz to 18 GHz and has an amplification of approximately 35 dB. Therefore, in combination with the frequency range of the probe, the VNA frequency is set from 0.1 GHz to 10 GHz, the number of scanning points is
To confirm the validity and accuracy of the measurement results of the proposed method, a direct port connection test of the LNA is performed using the VNA. Because the maximum value of the LNA input signal is -5 dBm and the maximum input signal of the VNA port is 27 dBm, the NVA frequency range is set from 0.1 GHz to 10 GHz. Testing is conducted at
In Figure 19, the LNA gain curves obtained by using the proposed method and by using the conventional method are given. The comparison reveals that the maximum error of the two methods is 1.66 dB at 0.8 GHz in the measurement band, the average overall error is 0.13 dB, the RMSE is 0.58 dB.
MLs are widely used in PCBs to transmit signals. With increasingly high device integration, the PCB ML spacing continues to decrease, such that multiple MLs often appear in parallel. When the distance between the MLs is too close, line coupling phenomena occur, which couples the signal originally transmitted in the ML to a similar ML. This process directly reduces the transmission quality of the signal.
A PCB with 6 MLs is used for measurement, as shown in Figure 20. The thickness of the PCB is 1.6 mm, the thickness of the MLs is 35 μm, the width of each ML is 0.762 mm, and the distance between the MLs is 0.508 mm.
Since FR4 usually operates in the 3 GHz band and below, the frequency range of the VNA is set to 100 kHz to 3 GHz, the power is set to 10 dBm, and the number of points is set to 1001. The near-field injection probe injects the signal into the red ML at a height of 0.5 mm from the PCB, and the detection probe is located at the other end of the red ML. The 6 MLs are connected to a 50 Ω load at both ends.
Before testing, it is necessary to obtain the equivalent parameters of the injection and detection probes at a line width of 0.762 mm. In practical scenarios, the line widths of MLs may vary across different circuits. The necessity of fabricating each circuit and obtaining equivalent parameters through testing for different ML widths can increase the complexity of the proposed method. Therefore, we propose establishing equivalent parameter curves for various line widths of FR4 before testing, enabling direct acquisition of equivalent parameters during subsequent tests.
Therefore, a PCB with 0.2 mm, 0.3 mm, 0.4 mm, 0.5 mm, 1 mm, 2 mm, 3 mm, and 4 mm line widths is designed. As shown in Figure 21, the equivalent parameters of the injection and detection probes for different line widths are obtained by testing.
The S21 curves of the injection probe and detection probe at different line widths are tested separately using VNA, and the corresponding circuit parameters can be obtained by combining them with the equivalent circuit model in Figure 2(b) after considering the FR4 substrate. The trends of the injection probe and detection probe for different components at different line widths are shown in Figure 22.
After obtaining the parameters of the injection and detection probes corresponding to the 0.762 mm linewidth, further optimization is conducted in conjunction with the VNA measurements to obtain the equivalent model results shown in Figure 23. Clearly, the theoretically obtained results based on the equivalent circuit vary only slightly from the measurement results, with good agreement realized in the 3 GHz frequency band. The specific values of the parameters in the equivalent model are shown in Table 2. The probes’ inherent impedances Z1 and Z2 are equivalent to the inductance, thus the unit henry (H) is employed.
Component Number | Value | Component Number | Value |
Z1 | 0.6 nH | Z2 | 1.3 nH |
C1 | 0.165 pF | Rl1,Rl2,Rl3 | 0.1 Ω |
R1 | 0 Ω | Ll1,Ll2,Ll3 | 1.97 nH |
C2 | 1.26 pF | Cl1,Cl2,Cl3 | 2.27 pF |
R2 | 0 Ω | Rl4,Rl5,Rl6 | 0.3 Ω |
C4 | 1.3 pF | Ll4,Ll5,Ll6 | 3.79 nH |
C3 | 0.18 pF | Cl4,Cl5,Cl6 | 2.17 pF |
Finally, the ML direct connection test using VNA is performed to verify the effectiveness of the proposed method. A comparison of the results obtained using the proposed method and direct VNA measurements is shown in Figure 24. The maximum error between the results obtained by the proposed method and the traditional measurement method is less than 1.47 dB in the range of 3 GHz, and the RMSE is 0.71 dB.
In this article, a novel method is proposed for identifying the transmission characteristics of circuits using dual probes. One probe is dedicated to signal injection, while the other is employed for signal detection. Utilizing specially designed semirigid coaxial probes featuring a T-shaped structure, the proposed method facilitates the identification of transmission characteristics within the frequency range of 10 GHz. This can be achieved with a minimum distance between the two probes exceeding 28 mm and a minimum spacing between the probes and an ML greater than 1.6 mm.
As shown in Table 3, an equivalent model corresponding to the proposed method is also proposed. The validity of the model is then confirmed through practical circuit testing. An error of less than 0.24 dB in the 10 GHz range in the ML transmission loss is achieved, and the circuit equivalent parameters are obtained based on the model.
Ref. | Probe | Method | Frequency | Target | Equivalent Parameters |
Max Error |
[20] | E Probe | Detection | 10 MHz-6 GHz | Reconstructing Signal | NO | - |
[24] | E Probe | Injection | 30 MHz-4 GHz | Injection Signal | NO | - |
[32] | E Probe | Detection Twice | UP to 12 GHz | Transmission Characteristic | NO | 17.2 dB |
[2] | E probe and M probe | Detection at Two Positions | 700 MHz-20 GHz | Transmission Characteristic | NO | 5.2 dB |
Proposed | E probe and E probe | Injection and Detection | 100 kHz-10 GHz | Transmission Characteristic | YES | 0.24 dB |
Finally, application tests are carried out using the proposed method for LNA gain and parallel ML circuits with FR4 as the substrate. The RMSE between the transmission characteristics obtained by the proposed method and the actual characteristics is less than 0.9 dB.
In future work, we will further verify the feasibility of the proposed method, especially in cases where the circuit impedance is unknown.
For Eq. (6) can be calculated by referring to the following derivation.
Firstly, Hp1(ω)Hi(ω) can be expressed as:
Hp1(ω)Hi(ω)=Vo(ω)Vi(ω)=Vo(ω)n(ω)×Vg(ω). |
(A-1) |
Subsequently, Eq. (4) can be updated by bringing back ig(ω), ii(ω), and io(ω) from Eq. (5) into Eq. (4):
n(ω)×Vg(ω)−Vg(ω)Z1=Vg(ω)R1+1jωC2+(Vg(ω)−Vo(ω))×jωC1. |
(A-2) |
The variables to be solved in the above equation are Vg(ω) and Vo(ω), which are obtained by arranging the equation:
Vo(ω)Vg(ω)=1−n(ω)−1jωZ1C1+1jωC1R1+C1C2. |
(A-3) |
Finally, bringing this result back to Eq. (A-1), Hp1(ω)Hi(ω) can be expressed as:
Hp1(ω)Hi(ω)=Vo(ω)n(ω)×Vg(ω)=1n(ω)−n(ω)−1jωZ1C1×n(ω)+C2(C1+jωC2C1R1)×n(ω). |
(A-4) |
Eq. (9) is also calculated by the same process as described above.
Firstly, Hp2(ω)Hd(ω) can be expressed as:
Hp2(ω)Hd(ω)=Vi1(ω)Vo1(ω)=Vi1(ω)m(ω)×Vg1(ω). |
(A-5) |
Subsequently, Eq. (7) can be updated by bringing back ig1(ω), ii1(ω), and io1(ω) from Eq. (8) into Eq. (7):
(Vi1(ω)−Vg1(ω))×jωC3=Vg1(ω)R2+1jωC4+Vg1(ω)−m(ω)×Vg1(ω)Z2. |
(A-6) |
The variables to be solved in the above equation are Vg1(ω) and Vo1(ω), which are obtained by arranging the equation:
Vi1(ω)Vg1(ω)=1+1−m(ω)jωZ2C3+C4jωC3C4R2+C3. |
(A-7) |
Finally, bringing this result back to Eq. (A-5), Hp2(ω)Hd(ω) can be expressed as:
Hp2(ω)Hd(ω)=Vi1(ω)m(ω)×Vg1(ω)=1m(ω)+1−m(ω)jωZ2C3×m(ω)+C4(C3+jωC3C4R2)×m(ω). |
(A-8) |
This work was supported in part by the National Natural Science Foundation of China (NSFC) under Grant
[1] |
A. P. Shitvov, D. E. Zelenchuk, A. G. Schuchinsky, et al., “Passive intermodulation generation on printed lines: Near-field probing and observations,” IEEE Transactions on Microwave Theory and Techniques, vol. 56, no. 12, pp. 3121–3128, 2008 DOI: 10.1109/TMTT.2008.2007136
|
[2] |
J. Stenarson, K. Yhland, and C. Wingqvist, “An in-circuit noncontacting measurement method for s-parameters and power in planar circuits,” IEEE Transactions on Microwave Theory and Techniques, vol. 49, no. 12, pp. 2567–2572, 2001 DOI: 10.1109/22.971651
|
[3] |
Z. Z. Peng and D. L. Su, “Analytical models of passive linear structures in printed circuit boards,” Chinese Journal of Electronics, vol. 30, no. 2, pp. 275–281, 2021 DOI: 10.1049/cje.2020.08.017
|
[4] |
P. Xiao, J. G. He, Z. S. Peng, et al., “Field-line-circuit coupling based method for predicting radiated electromagnetic emission of IGBT-PMSM drive system,” Chinese Journal of Electronics, vol. 30, no. 3, pp. 561–569, 2021 DOI: 10.1049/cje.2021.04.010
|
[5] |
J. A. Reynoso-Hernandez, M. A. Pulido-Gaytan, R. Cuesta, et al., “Transmission line impedance characterization using an uncalibrated vector network analyzer,” IEEE Microwave and Wireless Components Letters, vol. 30, no. 5, pp. 528–530, 2020 DOI: 10.1109/LMWC.2020.2984377
|
[6] |
Q. Xu, K. Chen, X. Q. Shen, et al., “Comparison of the normalized maximum field strength using e-field probe and VNA methods in a reverberation chamber,” IEEE Antennas and Wireless Propagation Letters, vol. 18, no. 10, pp. 2135–2139, 2019 DOI: 10.1109/LAWP.2019.2938833
|
[7] |
C. K. Lee and S. J. Chang, “A method of fault localization within the blind spot using the hybridization between TDR and wavelet transform,” IEEE Sensors Journal, vol. 21, no. 4, pp. 5102–5110, 2021 DOI: 10.1109/JSEN.2020.3035754
|
[8] |
H. P. Yang and H. Wen, “TDR prediction method for PIM distortion in loose contact coaxial connectors,” IEEE Transactions on Instrumentation and Measurement, vol. 68, no. 12, pp. 4689–4693, 2019 DOI: 10.1109/TIM.2019.2900963
|
[9] |
Y. H. Peng, H. Xu, H. Y. Zhou, et al., “High accuracy near-field electromagnetic emission identification system using characteristics recognition and image localization,” IEEE Transactions on Instrumentation and Measurement, vol. 72, article no. 3001211, 2023 DOI: 10.1109/TIM.2023.3314814
|
[10] |
T. H. Song, X. C. Wei, Z. Y. Tang, et al., “Broadband radiation source reconstruction based on phaseless magnetic near-field scanning,” IEEE Antennas and Wireless Propagation Letters, vol. 20, no. 1, pp. 113–117, 2021 DOI: 10.1109/LAWP.2020.3042538
|
[11] |
X. Z. Lu and L. N. Song, “Study on the impact of imbalance between transmission lines on crosstalk: a novel perspective of displacement current,” Chinese Journal of Electronics, vol. 34, no. 1, pp. 1–11, 2025 DOI: 10.23919/cje.2024.00.049
|
[12] |
Q. Huang, R. Q. Chen, W. X. Fang, et al., “Radiation emission source localization by magnetic near-field mapping along the surface of a large-scale IC with BGA package,” IEEE Transactions on Electromagnetic Compatibility, vol. 64, no. 2, pp. 495–505, 2022 DOI: 10.1109/TEMC.2021.3123536
|
[13] |
J. Wen, X. C. Wei, Y. L. Zhang, et al., “Near-field prediction in complex environment based on phaseless scanned fields and machine learning,” IEEE Transactions on Electromagnetic Compatibility, vol. 63, no. 2, pp. 571–579, 2021 DOI: 10.1109/TEMC.2020.3004251
|
[14] |
W. H. Shao, W. X. Fang, Y. Huang, et al., “Simultaneous measurement of electric and magnetic fields with a dual probe for efficient near-field scanning,” IEEE Transactions on Antennas and Propagation, vol. 67, no. 4, pp. 2859–2864, 2019 DOI: 10.1109/TAP.2019.2897476
|
[15] |
L. Wang, X. X. Liu, G. Lu, et al., “A new method to improve the detection sensitivity of differential magnetic-field probe for near-field scanning,” IEEE Transactions on Antennas and Propagation, vol. 71, no. 7, pp. 6225–6230, 2023 DOI: 10.1109/TAP.2023.3281060
|
[16] |
Y. Kuznetsov, A. Baev, M. Konovalyuk, et al., “Autocorrelation analysis and near-field localization of the radiating sources with cyclostationary properties,” IEEE Transactions on Electromagnetic Compatibility, vol. 62, no. 5, pp. 2186–2195, 2020 DOI: 10.1109/TEMC.2019.2946748
|
[17] |
W. Liu, Z. W. Yan, J. W. Wang, et al., “Ultrawideband real-time monitoring system based on electro-optical under-sampling and data acquisition for near-field measurement,” IEEE Transactions on Instrumentation and Measurement, vol. 69, no. 9, pp. 6603–6612, 2020 DOI: 10.1109/TIM.2020.2968755
|
[18] |
X. He, X. C. Li, Z. H. Peng, et al., “An ultrawideband magnetic probe with high electric field suppression ratio,” IEEE Transactions on Instrumentation and Measurement, vol. 70, article no. 8005309, 2021 DOI: 10.1109/TIM.2021.3121493
|
[19] |
J. W. Wang, Z. W. Yan, J. W. Liu, et al., “Miniature active differential magnetic field probe with high sensitivity for near-field measurements,” IEEE Transactions on Antennas and Propagation, vol. 70, no. 2, pp. 1575–1580, 2022 DOI: 10.1109/TAP.2021.3111300
|
[20] |
W. X. Fang, H. M. Qiu, C. Y. Luo, et al., “Noncontact RF voltage sensing of a printed trace via a capacitive-coupled probe,” IEEE Sensors Journal, vol. 18, no. 21, pp. 8873–8882, 2018 DOI: 10.1109/JSEN.2018.2869908
|
[21] |
C. Y. Luo, W. X. Fang, Y. Shen, et al., “Collocated and simultaneous measurements of rf current and voltage on a trace in a noncontact manner,” IEEE Transactions on Microwave Theory and Techniques, vol. 67, no. 6, pp. 2406–2415, 2019 DOI: 10.1109/TMTT.2019.2905204
|
[22] |
X. Wu, F. Grassi, S. A. Pignari, et al., “Performance of electric near-field probes for immunity tests,” in Proceedings of 2020 XXXIIIrd General Assembly and Scientific Symposium of the International Union of Radio Science, Rome, Italy, pp. 1–4, 2020.
|
[23] |
T. Dubois, S. Jarrix, A. Penarier, et al., “Near-field electromagnetic characterization and perturbation of logic circuits,” IEEE Transactions on Instrumentation and Measurement, vol. 57, no. 11, pp. 2398–2404, 2008 DOI: 10.1109/TIM.2008.926371
|
[24] |
X. L. Wu, F. Grassi, G. Spadacini, et al., “Test design methodology for time-domain immunity investigations using electric near-field probes,” IEEE Transactions on Electromagnetic Compatibility, vol. 64, no. 3, pp. 603–612, 2022 DOI: 10.1109/TEMC.2022.3149537
|
[25] |
W. Liu, Z. W. Yan, J. W. Wang, et al., “An ultrawideband electric probe based on u-shaped structure for near-field measurement from 9 kHz to 40 GHz,” IEEE Antennas and Wireless Propagation Letters., vol. 18, no. 6, pp. 1283–1287, 2019 DOI: 10.1109/LAWP.2019.2915258
|
[26] |
Z. Min, Z. W. Yan, W. Liu, et al., “A miniature high-sensitivity active electric field probe for near-field measurement,” IEEE Antennas and Wireless Propagation Letters, vol. 18, no. 12, pp. 2552–2556, 2019 DOI: 10.1109/LAWP.2019.2942956
|
[27] |
Online]. https://ecatalog.hubersuhner.com/material/22810041. (查阅网上资料, 未找到本条文献信息, 请确认)
SR-141-M17, (2024
|
[28] |
Y. X. Liu, X. C. Li, X. He, et al., “An ultra-wideband electric field probe with high sensitivity for near-field measurement,” IEEE Transactions on Instrumentation and Measurement, vol. 72, article no. 8001910, 2023 DOI: 10.1109/TIM.2023.3261946
|
[29] |
IEC 61967-6: 2002, Integrated circuits-measurement of electromagnetic emissions, 150 kHz to 1 GHz- part 6: Measurement of conducted emissions-magnetic probe method, document, Available at: https://webstore.iec.ch/en/publication/6193.
|
[30] |
J. X. Li, Y. Yuan, J. L. Zeng, et al., “A broadband LNA with multiple bandwidth enhancement techniques,” IEEE Microwave and Wireless Technology Letters, vol. 33, no. 5, pp. 551–554, 2023 DOI: 10.1109/LMWT.2023.3234158
|
[31] |
TLLA0.1G18G-30-25, (2024). [Online]. https://www.talentmw.com/productDe1625.html. (查阅网上资料, 未找到本条文献信息, 请确认)
|
[32] |
Z. Z. Peng, H. Xu, and D. Su, “A method of extracting transmission characteristics of interconnects from near-field emissions in PCBs,” Applied Sciences, vol. 13, no. 5, article no. 2874, 2023 DOI: 10.3390/APP13052874
|
Component Number | Value | Component Number | Value |
Z1 | 1.51 nH | C3 | 0.3 pF |
C1 | 0.28 pF | Z2 | 1.3 nH |
R1 | 0.8 Ω | Rl1,Rl2…,Rl6 | 0.11 Ω |
C2 | 2.1 pF | Ll1,Ll2…,Ll6 | 0.05 nH |
R2 | 0.01 Ω | Cl1,Cl2…,Cl6 | 0.001 pF |
C4 | 0.09 pF |
Component Number | Value | Component Number | Value |
Z1 | 0.6 nH | Z2 | 1.3 nH |
C1 | 0.165 pF | Rl1,Rl2,Rl3 | 0.1 Ω |
R1 | 0 Ω | Ll1,Ll2,Ll3 | 1.97 nH |
C2 | 1.26 pF | Cl1,Cl2,Cl3 | 2.27 pF |
R2 | 0 Ω | Rl4,Rl5,Rl6 | 0.3 Ω |
C4 | 1.3 pF | Ll4,Ll5,Ll6 | 3.79 nH |
C3 | 0.18 pF | Cl4,Cl5,Cl6 | 2.17 pF |
Ref. | Probe | Method | Frequency | Target | Equivalent Parameters |
Max Error |
[20] | E Probe | Detection | 10 MHz-6 GHz | Reconstructing Signal | NO | - |
[24] | E Probe | Injection | 30 MHz-4 GHz | Injection Signal | NO | - |
[32] | E Probe | Detection Twice | UP to 12 GHz | Transmission Characteristic | NO | 17.2 dB |
[2] | E probe and M probe | Detection at Two Positions | 700 MHz-20 GHz | Transmission Characteristic | NO | 5.2 dB |
Proposed | E probe and E probe | Injection and Detection | 100 kHz-10 GHz | Transmission Characteristic | YES | 0.24 dB |