[ieee 2014 ieee 29th international conference on microelectronics (miel) - belgrade, serbia...
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191978-1-4799-5296-0/14/$31.00 © 2014 IEEE
PROC. 29th INTERNATIONAL CONFERENCE ON MICROELECTRONICS (MIEL 2014), BELGRADE, SERBIA, 12-14 MAY, 2014
Analog Front End Stage of a Fiber Optic Magnetic Field Point Scanner
S. J. Petričević, P. Mihailović, M. Barjaktarović, J. Radunović
Abstract – Fiber optic Faraday magnetic field scanners are sophisticated sensing devices whose important part is electronic signal processing block. This paper presents some aspects of a design of an AFE (Fig. 2) for FOFMS that meets these requirements. Electronic section containing the AFE has been constructed and implemented into electronic processing section containing analog to digital conversion (ADC). This unit has been integrated into a sensor and used to collect and process data in order to asses the sensor performance figures..
I. INTRODUCTION
Faraday magnetic field sensing has been under
continuous investigation for several decades, with various applications and research directions in mind [1]-[7]. Advantages of these devices over other techniques used to sense magnetic fields include complete dielectric isolation, no field perturbation, enormous bandwidth and passive sensing head construction. Techniques and devices implemented in fiber optic communications have become readily available on the market making construction of the fiber optic Faraday magnetic field scanner (FOFMS) an attractive option.
Particular area of interesting applications for point type scanner include: magnetic flux leakage detection, power systems equipment monitoring and environment monitoring. Magnetic flux leakage detector operates with induction levels of up to tens of mT. Power systems monitoring involves fiber optic measuring of current via sensing its induced magnetic field. Health concerns have led to regulations regarding recommended maximum induction values near substations, ranging from 6 µT at 3 kHz up to 40 mT at low frequencies. Therefore potential applications for Faraday magnetic field scanner require a device capable of 100:1 signal to noise ratio, measurement range from 100 µT to 100 mT and 3 kHz frequency bandwidth.
Light from the source (usually a LED or a laser diode) is coupled with a transmitting fiber that carries the light to the sensor head. Polarization state of light is modulated by magnetic induction at the head, then converter to intensity change and carried to electronic processing block by two receiving fibers. These are converted by photo detectors (photodiodes or phototransistors) and converted to voltage for further processing.
This paper is concerned with a design of an electronic section that performs such function (also know as analog front end or AFE for short) tasked with providing adequate conversion of light to voltage. It must be designed to
measure low level modulation of an optical carrier imposed by the magnetic field with sufficient resolution, yet be capable of adapting to variations in the light carrier intensity due to other sources (aging, temperature, mechanical coupling etc.). Further, it must comply with conventional requirements for an analog amplifier stage such as offset, bandwidth, stability and others. These requirements are tightly coupled and mandate careful design approach.
Fiber optic sensing generally requires that some kind of normalization be applied in signal processing in order to eliminate effects arising from light source intensity changes, fiber bending, temperature, aging and other causes with similar spectrum to the sensed quantity. Our design is based on Δ/Σ normalization that can be expressed as
1 1 2
1 2
1 sin2
U Ur const BU U
(1)
Quantity r represents numerical value linearly related
to magnetic field induction B and is obtained from two voltages (U1 and U2). These represent intensities of light from two receiving fibers impinging on photodetectors (AFE output).
II. THE ELECTRONIC PROCESSING BLOCK
Electronic processing section (seen in fig. 1) of a
FOFMS determines to great extent the performance of a device. Analog front end (AFE) consists of transimpedance stages and part of power supply system and influences signal-to-noise ration of a sensor together with analog to digital converter
Fig. 1. Electronic processing section in a fiber optic magnetic field scanner.
AFE
LED
ADC
MCU
USB
POWER
PCUSB
TX FIBER
RX FIBER 2
RX FIBER 1
192
AFE output (voltages U1 and U2) are fed to 16 bit analog to digital converter inside a microcontroller unit (SiLabs C8051F064) that samples the voltages and creates data stream transmitted to a PC computer (via USB) for processing (Eq. 1). MCU also controls light source (LED). Power to the entire block is supplied from the same USB link by a multi stage switcher that creates clean dual analog supply (± 5V) for AFE and supply for other blocks.
III. ANALOG FRONT END
Two crucial aspects of AFE design need to be taken
into account: signal-to-noise ration and dynamic range. Light modulation that takes place in the sensing head is small, about 0.15% per mT of magnetic field induction [8]. If 100 points are required in the full range (about 10 μT resolution), SNR must be at least 1:70000. Transimpedance stages must produce voltages lower than ADC maximum input range (2.5 V) so voltage resolution translates to 35 μV per 1 LSB of ADC. AFE noise must remain below this level.
Fiber motion, light source aging, mechanical coupling effects and other causes cause wide range light intensity variations at the head input and at the photodetectors. This can cause the power at photodetectors to vary anywhere from few μW up to hundreds of μW. As mentioned earlier, voltage at ADC inputs (AFE outputs) must remain within specified range. Therefore transimpedance stage must have adjustable gain to adapt to such a condition of wide dynamic range.
Accuracy could also be a substantial problem. A look at Eq. 1 shows operations of subtraction, addition and division followed by inverse trigonometric function. Changes in values for voltages U1 and U2 are small (as explained due to low modulation) and if these contain errors from say op amp offsets, results calculated can be quite incorrect. Another source of error is the photodiode dark current that causes a DC voltage at the op amp output dependant on the transimpedance gain. These two error sources can be compensated for by op amp offset compensation techniques.
Of less concern is the bandwidth requirement. As stated in introduction, bandwidth of 3 kHz is required and can be accomplished with relative easy by using large bandwidth op amp. This is then compensated with a capacitor calculated for required bandwidth at maximum transimpedance gain (maximum transimpedance resistance).
Solution for AFE is seen in fig. 2. Wide dynamic range problem is solved by using a digital potentiometer for transimpedance resistance (Analog Devices AD5242). These dual units feature 1 MΩ resistance thus allowing for 2 μA of minimum photocurrents from detectors. They are controlled using I2C interface (SCL and SDA lines) allowing for several chips on the same line for reasons of expansion. Op amp of choice is Analog Devices AD8034 (dual JFET input high bandwidth) with compensating
capacitors (CTA and CTB) dimensioned for 3 kHz bandwidth. Offset and dark current compensation is accomplished by applying voltages VOA and VOB with additional damping networks.
CTA
47pF
VTIAA
3
21
84
TIAAAD8034
+5
C
B
E12
SHIE
LD
0
FTA
SFH250V SFH350V
VPDA
CTIA1100n
GND
GND GND
CTB
47pF
GND
VTIAB
5
67
TIAB
AD8034
+5
SCL
C
B
E12
SHIE
LD0
FTB
SFH250V SFH350V
SDA
VPDB
+5
RTIAA
100
RTIAB
100
-5
VBIAS
VBIAS
SELB
SELA
3
21
411
OPA
LM6134BIN
COP1100n
CTIA2100n
GND
GND
10
98
OPC
LM6134BIN
RC1
4K7
5
67
OPB
LM6134BIN
VBIAS
VC
+5
-30COP2100n
GND
U?
SYM 1 OF 1
?
?
AD7398BR
VC
C16
CA1 10
VOUTD14
REFLO 2
CA0 11
VOUTC13 VOUTB5 VOUTA4
GN
D1
CA2 7
VREFD 15
SDA 9SCL 8
VREFC 12VREFB 6VREFA 3
DAC
LTC2609
SCLSDA
GND
+5
+5
GND
GND
VOA
1.25VVAVBVCVD
RA2
4K7
RA1
4K7
VB
1.25V
CA2
100n
RB2
4K7
CB2
100n
RB1
4K7
VOA
X012
X114
X215
X311
Y01
Y15
Y22
Y34
INH6
A10
B9
VEE7
X 13
Y 3
VC
C16
GN
D8
MUX
MC74HC4052-5
+5
GND
SELASELB
VINA
VINB
COA10u
ROA1
100K
GND
VOB
COB10u
ROB1
100K
GND
VOB
CDAC
100n
GND
CDPOT100n
GND
ROA2100K
ROB2100K
RC2
68K
GND
12
1314
OPD
LM6134BIN
RD1
4K7
VCAL
VD
RD2
15K
GND
+
CC2
100uF
1.25V
VA
DTIABTMMBAT42
GND
DTIAATMMBAT42
GND
DTIAA-
TMMBAT42
GND
DTIAB-
TMMBAT42
GND
VINB
VINA
VPDA
VPDB
VCAL
VCAL
CD2100n
CMUX2100n
GND
CMUX1100n
GND
GND
GND
GND
A12 B1 4
W1
3
A216 B2 14
W2
15
O1
1
O2
13
AD
09
AD
110
SCL
7
SDA
8
SHD
WN
6
VSS 12
DG
ND
11
VDD5
DPOTAD52421M
RCAL1M
Fig. 2. Analog front end schematics.
Since analog voltages are required a digital to analog
converter (DAC, model LTC2609 from Linear Technologies) is required. A four channel unit (voltage VA, VB, VC and VD) used can also supply voltage for photo detector bias (VBIAS) and calibration (VCAL). Additional quad op amp (LM6134) and associated network provide for single to dual supply voltage conversion and scaling. Photodetectors FTA and FTB can be either photo diodes (model SFH250V from Siemens) or phototransistors (SFH350V) suitable for fiber coupling. Choice depends on the amount of optical power available at the receiving fiber. Photodiodes provide superior temperature and bandwidth performance.
Since channel resistance of AD5242 also exhibit error and channel differences, these must be taken into account by calibration. This must be done before sensing photocurrents and is accomplished by multiplexing the same calibration current from 1 MΩ RCAL into VINA or VINB transimpedance stage input. Channels are calibrated in turn and the calibration current can be adjusted by DAC to accommodate for dynamic range. Once calibration is done, multiplexer switches photo detector currents (VPDA and VPDB) to transimpedance inputs and the measurement can begin. The ADC is capable of clibration correction of offsets and gains for its channels and this option is used to compensate for operational amplifier offsets and resistance differences in digital potentiometer channels.
Multiplexer characteristics do not affect the performance since multiplexer channel resistance mismatches and values are much smaller then calibration resistance and detector output impedances.
Detector bias can be set to reduce their inherent pn junction capacitances but was found by test to be redundant.
The rest of the circuit involves some protection diodes and decoupling networks that do not affect its function.
193
IV. EXPERIMENTAL RESULTS AND DISCUSSION
Experiments with the FOFMS have been carried out in
laboratory conditions in order to test the performance of the scanner. Noise testing was accomplished by placing the scanners head inside Helmholtz coils with controlled current and then acquiring magnetic induction values for a long time. Details of the setup are discussed in [8].
0 20 40 60 80 100 120 140 160 180 2002.077
2.078
2.079
2.080
2.081
2.082
2.083
2.084
2.085
2.086
B [m
T]
t (s) Fig. 3. Scanner noise.
Result can be seen in fig. 3 demonstrating that the sensor’s noise level is about 8 μT (peak to peak). This noise level contains contribution noises form LED noise, photodetectro noise, AFE noise and ADC nois (e.g. system noise).
Fig. 4 demonstrates a scan of magnetic induction inside Helmholtz coils in a plane parallel with coils but placed in the middle between them.
Fig. 4. Magnetic field scan obtained by FOFMS
The field is quite uniform in the coil center, but rises as the sensing head approaches the windings, as can be expected. Excellent SNR and lineariry can be inferred by simetrical shape and smooth surface.
Amplitude response of the electronic block is seen in fig. 5 obtained by sweeping the excitation frequency.
0 1k 2k 3k 4k 5k 6k 7k-5
-4
-3
-2
-1
0
1
B(f)/
B(50
Hz)
[dB]
f[Hz] Fig. 5. Normalized amplitude response of the FOFMS.
V. Conclusion
Dedicated electronic processing block has been
constructed for a fiber optic magnetic field Faraday effect scanner. Attention in the paper has been placed on analog front end stage whose design is of crucial importance for the performance of the device. A solution adaptable to various conditions has been proposed and tested in laboratory conditions.
ACKNOWLEDGEMENT
This work was supported by the Ministry of
Education and Science of the Republic of Serbia, project III 45003.
REFERENCES
[1] Tabor, W.J. & Chen, F.S. (1969), "Electromagnetic propagation through materials possessing both Faraday rotation and birefringence: Experiments with ytterbium orthoferrite", Journal of Applied Physics, vol. 40, No. 7, pp. 2760-2765. [2] Jaecklin, A.A. & Lietz, M. (1972), "Elimination Of Disturbing Birefringence Effects On Faraday Rotation", Applied Optics, Vol. 11, No. 3, pp. 617-621. [3] Rogers, A.J. (1983), "Optical Fibre Current Measurement", Proceedings of SPIE - The International Society for Optical Engineering, pp. 196-201. [4] Ulmer Jr., E.A. (1990), "High-accuracy optical current transducer for electric power systems", IEEE Transactions on Power Delivery, vol. 5, no. 2, pp. 892-898. [5] Nikitin, P.I., Grigorenko, A.N., Sokol-Kutilovsky, O.L., Zvezdin, A.K. & Zvezdin, M.K. (1992), "Magnetic-field sensors for non-disturbing and wide-band measurements", Sensors and Actuators: A.Physical, Vol. 32, No. 1-3, pp. 671-677.. [6] Frosio, G. & Dandliker, R. (1994), "Reciprocal reflection interferometer for a fiber-optic Faraday current sensor", AppliedOptics, vol. 33, no. 25, pp. 6111-6122. [7] Williams, P.A., Day, G.W. & Rose, A.H. (1991), "Compensation for temperature dependence of Faraday Effect in diamagnetic materials: Application to optical fibre sensors", Electronics Letters, vol. 27, no. 13, pp. 1131-1132. [8] S. J. Petricevic, P. M. Mihailovic, J. B. Radunovic, “Performance analysis of the Faraday magnetic field point scanner”, Sensor Review, vol. 33, pp. 80-85, 2013.