Wideband Active Small Magnetic Loop Antenna

Chavdar Levkov LZ1AQ,    lz1aq@abv.bg,   www.lz1aq.signacor.com


 Last revision v.1.1     13 June 2011


There are now extremely wideband software defined radios (SDR) where the wideband antenna is a natural choice.  Wideband small magnetic loops (WSM loop) are used already 3-4 decades and I was curious to see what can be reached with them and to evaluate their usefulness as a wideband SDR input. The WSM loop should work in short circuit mode in order to reach flat frequency response in wideband frequency range.  The antenna should be used with an amplifier since the loop current is very small. This amplifier must be with very low input impedance. [1, 2, 4, 6, 12].


 Schematics and Construction

A circuit diagram of active WSM loop antenna is shown on Fig.1. The antenna specification is given for 1m diameter circular loop with aluminum conductor with diameter 3.4 mm.



Fig. 1 Schematics diagram of wideband active small loop amplifier. Common base circuit. DC operating point voltages and currents are given.



Diameter:                    1 m, 1 turn 

Material:                     aluminum conductor with 3.4 mm diameter

Loop inductance:       4 uH

Antenna Factor Ka:   6 dB meters-1 @ 10 MHz (computed from the spice model)

                                   (1 uV/m input signal will give 0.5 uV output voltage)

Flatness:                     Within 3 dBmeters-1 0.5  – 30 MHz;   (computed from the spice model)

Noise floor:                  >= 0.7 uV/m   (computed from the spice model)

Power supply:              Remote, 13.5 V  >150 mA

Dynamic range:            TBS;  1 dB Compression point >= 130 dBuV/m ( 5.6 V/m p-p output voltage, from the spice model)



An experimental amplifier and antenna construction are shown in Fig. 2 ,3,4 .   



 Fig.2                                                                                     Fig.3



The construction of the loop  should be considered with the  following rule:  the ratio of  loop area to loop inductance should be maximized (see the Appendix) .  That automatically means that circular shape with 1 turn is the best choice.  The practical diameter is around 1 m with the conductor as fat  as possible.  The material might be copper or aluminum – actually the loop Q-factor is not important. The important factor is  the low loop inductance.  1m diam. loop made from aluminum wire 3.4 mm gives inductance around 4 uH.  I have used also 0.9 m diam. loop made from  double foil  FR-4  PCB material (Fig.3)  with 1.5mm thickness and 20 mm width  which reduces the loop inductance to 3 uH.  The best results can be obtained with “parallel” and “crossed parallel ”  loops (CP loop, see Fig. 5 , 13,14 , Appendix I,II). For urban locations where the noise level is much higher smaller loops can be used. 


Fig.5    The author at the experimental green field.

 4 m2 4-squares crossed parallel loop is mounted on a wooden frame..


 This antenna will be used outdoors and the amplifier is placed in a small, IP55 secured, plastic box (Fig.2). These boxes are widely available on the market - any similar one can be used.  The connecting cable between the antenna and receiver (RX) is shielded LAN cable FTP type with 4 twisted pairs. The signal and power use separate pairs. RJ45 standard connectors are used. These connectors are very cheap and reliable but the RJ connector should to be placed inside the box since it is not waterproof. There is no need for the box to be shielded – it is supposed that the antenna will be mounted at least several meters away from electrical equipment and direct near field influence to amplifier board will be reduced.  The FTP shield must be connected to RX ground (chassis), but at the far (antenna) end should be left floating. The power supply (PS) ground also is floating if independent DC supply is used. Do not use switching PS  - it will be very difficult to remove its noise. The control box Fig.4 contains RJ and BNC connectors, PS  chokes and L9, L10 balun.  The box should be shielded since it is placed in the shack and interferences are possible. The LAN cable has 100 ohms impedance and it can be connected directly to 75 or 50 ohms input of the RX without any noticeable adverse effects. For the purists a 2:1 wideband impedance matching transformer can be used for precise matching.

There are 4 unused wires in the cable. The unused wires should be grounded in the RX part. They can be used for remote control of additional relays or rotator.  I have used 1 relay to switch 2  identical loops rotated 90 deg.  to each other.


Some comments on the amplifier schematic

The amplifier is a standard common base differential amplifier. The differential input resistance of the amplifier is around 3 ohms at 1 MHz (rises with frequency, module =7 ohms @ 30MHz, spice modeling) and this assures flatness of the antenna factor in wide band. This very low input impedance reduces also the electric field sensitivity to minimal levels. The gain of the amplifier with 1 m2 loop is set to give approximately between 0  to +6 dBmeters-1 antenna factor (depends from the loop size, shape and inductance, see the Appendix).  In this case the level of output internal noise at the active WSM loop  is about 10-15  dB above the internal  noise level of RX with -130dBm @500Hz MDS  (this sensitivity is very common  between commercial transceivers).   Increasing the amplifier gain will increase only the non-linear distortions level.

The differential amplifier has two advantages for the non-linear distortions reduction:  reduces with 6 dB the signal level of each arm and reduces the output level of  2nd (and all even)  order distortions  with 20 – 30 dB. The reduction depends from the symmetry of the transistor pairs and output wideband transformer. The second order distortions are the main source of spurious signals in this wideband antenna.

The transistors are the popular PN2222A which have quite linear response [7]  noise figure of 4 dB and acceptable power dissipation. Using lower noise transistors do not improve substantially the noise floor (Appendix I).  To improve the 2nd order  distortions a matched transistor pairs should be used (at least  hFE). The collector currents of the first and second pair are  25 mA and 40 mA correspondingly.  The power dissipation of PN2222A  (TO92 case)  is  0.5 w at 50 deg. C ambient temperature and these transistors work without radiators. In the case where the loop will be used for frequencies up to 50 MHz  the output transistor pair should be with FT > 1 GHz e.g.  BFR96 or something similar.

 There is no classical matching of the antenna to the amplifier input since the antenna actually is working in short circuited mode. I have modeled several solutions with input wideband transformers. Slight reduction in the noise floor at some frequencies  can be obtained but not significant, so I leave the simplest solution without any transformer.  There is an input LP filter (C5, L1, R21, C10, L2, R22) to reduce the signals from the FM broadcasting band. This filter also raises the frequency response in the higher frequencies. The filter Q-factor is controlled by R21,R22 resistors. In authors city location there are  very strong nearby FM stations and without this filter the nonlinear distortions occur. This filter can be omitted if there are no FM transmitters in the vicinity or the antenna will be used up to 50 MHz.  

This amplifier can withstand very high filed intensities without additional protection.  For example the loop was mounted 20 m from a full sized antenna feed with 1.5 Kw PA and works flawlessly during 48 hours ham radio SW contest. Static leakage resistor with 100 K value can be connected between antenna amplifier common point and ground.

The possible common mode currents are reduced  by using separating transformers, chokes and baluns between amplifier and  RX and PS parts.



All experiments are performed with  vertical loop plane with loop center  height approximately 2 m above the ground.   Horizontal loop plane is possible but then the polarization is horizontal. The horizontal loop should be placed at least wavelenth/4 height to have omni directional low angle pattern and acceptable signal levels.


Noise floor

The active WSM loop noise floor  is a figure which measures the ability of this antenna to receive weak signals. This is the magnitude of the internal noise voltage  (effective values) at the output of the amplifier Vnout  [uV]  but multiplied  by the antenna factor K[1/meter] (antenna factor Ka is  reciprocal of effective height h ). The measurement must be performed in predefined bandwidth which in our case is 1 KHz. This is convenient way to compare the external and internal noise in  the active antenna expressed in [uV/m] as if the internal noise is coming from the space. 


Nfloor =  Vnout * Ka              in  [ uV/m]                 (1)


If we have antenna factor Ka  =1 m -1  that means that field with 1 uV/m will give output voltage of 1 uV. If the active antenna output noise voltage measured in the screened chamber is 1 uV   at  BW=1KHz  the noise floor of this antenna is 1 uV/m. In this case the power of the antenna noise and external signal are equal.  

Measuring the antenna noise in screened chamber needs special equipment. More simple way is to replace the loop with equivalent inductance with lump parameters with the same value. Measuring  the noise on the band with small magnetic (SM) loop,  and then the noise with equivalent inductance will clearly show the relative noise floor of the active antenna  compared with the current band noise. The equivalent inductance should to be wound on the ferrite toroidal core to minimize the external field influence.

  The results of such experiment are shown on Fig.6 .  N/N is the ratio of the power of current band noise + internal noise to the power of the internal noise of the antenna. The band noise was measured directly from the spectrum display of the SDR at frequencies where there are no transmitting stations (Fig.6a).  As it can be seen, in city location, the band noise is much higher and is the limiting factor  for antenna sensitivity.  For rural locations however  this is not the case.  N/N ratio should be above  10 dB  if we want that the real sensitivity of the active antenna is not degraded noticeably by its internal noise.



Fig.6   An experimental measurement  of band noise to noise floor ratio of active circular WSM loop 0.86m diam., aluminum conductor 3.4 mm.

This ratio is measured at different times of the day in rural place. 





Fig.6a   Comparing two different magnetic loops with 2-channel synchronized RX. Quiet rural location.

The spectrum is result of 10 sec 2-channel averaging of the signals on 14 MHz CW portion of the band.

The upper channel is signal from tuned low Q-factor (Q=25) loop. The lower is from the wideband loop.

Both loops have 0.86 m diam. and are placed 5 m from each other.

Notice that S/N ratio in tuned loop is 6 – 10 dB better than that in the wideband loop.

The yellow traces are the output signal when the loops are substituted with toroidal coils with same

 equivalent inductance as the corresponding loop. These traces present  the internal noise level of the active antenna – its noise floor. .

For the tuned loop the external noise is 8 dB higher than the noise floor. For the wideband loop this value is only 2 dB.


Non-linear distortions

This is a very wideband antenna and total MW and HF spectrum is applied at its input. I measured the wideband power  at the amplifier output (1m diam., 4 uH loop) with thermocouple power meter (HP432A). In urban environment  Pout =  -22 to -29 dBm depending from the time of the day ( night time is higher).  In rural places Pout is  from  -24 to bellow -30dBm.  (An active  GSM handy induces -15 dBm when 1 meter from the loop.)  These are averaged values and the peaks can be much higher.

I do not have an access to good measuring equipment to obtain reliable figures for the 2nd and 3d order distortions. What I have done is to check carefully whether there are any signs of such distortions on the band.  I checked the 2nd order  products (F1+F2  and 2F ) which might exist as a spurious signals in 14.400 – 15.200 MHz band as  result of action of the strong broadcasting stations on 41 m band with frequencies  7.200-7.600 MHz.  The important condition is that there must be no propagation on 14-15 MHz band to be sure that all existing signals are spurious. Night winter time is most suitable for this experiment. This test was performed several times at night time with SDR (Winrad) which is very convenient for this purpose. The SDR RX has  input narrow band pass filter (200 KHz BW at 14.7 MHz with attenuation > 35dB for 7 MHz)  to avoid direct second harmonic mixing.   Fig.7 shows the results of this experiment. All candidate spurious frequencies  should be multiples of 5 KHz since this is the distance between broadcasting frequencies. I used a 60m long wire (LW) antenna connected through the antenna tuner directly to the SDR input for reference. At start the LW antenna was switched on (upper part of the waterfall display). Then the active loop was switched which is well seen on the picture. (lower part of the display).    There are probable very weak spurious traces at 14660, 14720 and 14740. 14730 exist in both cases so it is real signal. If the band is open these spurious signals will be buried in the band noise. A slight noise probably from pulse PS is seen very well on the LW antenna. Seemingly there is a “reduction” of this noise when the loop is activated. But  it should be considered that the noise floor of the loop in this case is at least 10 -15 dB  above the noise floor of the LW antenna.

3-d order  distortions (2F1-F2) can  also be  found in this way but they are buried in the same  41 m band. There are chances to find such spurious products  in the vicinity of the BC band . I tried to identify light carriers that exist on the amateur 40 m band and are multiples of  5 KHz but do not find an obvious candidate for such case in this natural experiment.


Fig.7   A 96 KHz SDR display to check the existence of 2nd order spurious products from 41 m BC band.


Comparison with full sized antenna

The results of precise comparison of the 1 m diam. thin loop with full sized antenna  - Long wire (LW 60 m length, 15 m above the ground) are shown in WSML_eval.pdf  in real environment,  at the same time.  The comparison is performed with synchronized 2-channel  direct conversion receiver.  Active SML and LW are fed into each channel input and the signal from the each channel output is fed to  the two sound card inputs. A dual channel spectrum-analyzer is used (Spectralab, Sound Technolgy Inc.).  The spectrograms are made in amateur bands with averaging of 10 seconds (see more detailed description of the method in previous article [23]).   The place is quiet rural with low level of man made noise.  The noise floor is acceptable on  1.8  and 3.5 MHz bands but on 14 MHz  at least additional  6 -10 dB   reduction of the WSM loop  noise floor is needed. Do not pay attention to the absolute level of the signals  - just the S/N ratio is important.

The most striking lack of sensitivity is at day time on 14 MHz band. The S/N ratio of a full size LW  antenna is 5 to 15 dB better than the WSML. Some of this inefficiency is due to the location of the loop -  only 1.5 m above the ground (the lower part of the loop)  but in the same conditions a tuned loop gives 4 - 6 dB lower noise floor (Fig.6a).  At the twilight time when the band noise increases, the wideband and tuned loop antennas become almost equal.



This antenna acts almost as a pure magnetic transducer. The input impedance of the amplifier is so low that any currents induced by electric field become very small compared to the currents induced by magnetic filed.  This antenna does not need shield or any type  of grounding. For vertically polarized low elevation angle signals the antenna has very sharp null.  The directivity for the sky wave signals is not determined since their polarization is stochastic.   The influence of nearby non-resonant conductive object is negligible. The differential circuit also reduces the influence of common mode currents.  It works from height almost zero above the ground (there is almost no change in signal levels when the loop side is placed several  centimeters above the ground in field environment).  The wideband properties are excellent  - from LW to upper HF even 50 MHz band can be included. The dynamic range obtained from on the air tests on the bands  is good and no apparent non-linear distortions are found.  The circuit is very simple, stable and cheap and there is nothing critical for adjustment.  The antenna can be mounted outdoor and connected with FTP cable to RX and PS parts. The FTP cable  is widely available  and the associated connectors are very reliable and cheap.  This is my favorite antenna for my city office where nothing else can survive the EMC pollution. The only drawback of this active antenna is  its relatively higher  noise floor specially for frequencies above 10 MHz  which is several dB above the atmospheric noise levels for quiet rural locations at some frequencies and times of the day (for single loop 1m diam.) . The antenna noise floor is acceptable  and suitable for all locations where the man made noise is moderate and above. The noise floor limit of these types of WSM loops is essential  - see the Appendix section for more details. The noise floor can be reduced by using “fat” , parallel or parallel crossed loops especially for places where the electromagnetic noise is very low. 






Appendix  I          Analysis of the Active Wideband SM Loop Performance


Tuned Loop

In previous article  [23]   it was pointed out that the sensitivity of narrow band high Q-factor SM loop antenna  is limited  by the thermal noise of its  loss resistance.  The noise floor of such antenna with modest  size  (1 turn loop 0.5 to  1m diam.)  which can be reached in the range between 1 – 30 MHz  can be bellow the atmospheric noise level  in quiet rural location.  The “signal- to- thermal noise ratio”  is described by simple equation:  

                                            ( 2 )


where E is the e.m.f.  induced in tuned loop form  external filed with intensity e (uV/m). f is frequency in MHz, A is the loop equivalent area in m2Bw is the  measurement noise bandwidth in Hz, RL is loss resistance in ohms, Un (uV) is the loop thermal noise voltage at specified Bw.


1. For magnetic transducer it is more natural to use H  (the intensity of the magnetic field component) expressed  in  uÀ/m instead of e.  In electromagnetic wave in free space (vacuum and in far zone) the ratio between e and Í is always the same – the so called free space impedance = 377 ohms.  Intensity of  e  = 1 uV/m is always equal  to Í = 0.00266 uA/m. Further on e values will be used since the intensity of the electromagnetic  field is given usually in V/m. 

2. In previous article [23, Eq.3]  I have used the term “effective area” A  as parameter which is:  geometric loop area times  number of turns times permeability. This term is used in different sense in the antenna terminology. There , antenna effective area is a measure how much power of the incoming wave front can absorb and fed to its optimal load  any antenna. To avoid misinterpretations I will use the  term “equivalent area”.

A useful graphic is presented on Fig.8   which can give a rough estimation of the loop size and Q-factor in order to reach 10 dB S/N ratio for signal with field intensity e of 0.2 uV/m  at 1 KHz bandwidth. The level of 0.2 uV/m was somewhat arbitrary chosen by me as an average lower boundary of atmospheric noise in rural locations according to ITU reports.



Fig. 8  Minimal area of 1-turn circular magnetic loop in order to reach 10 dB S+N/N ratio

for signal with field intensity e of 0.2 uV/m. N  is the thermal noise voltage of loop loss

 resistance measured in 1 KHz bandwidth. Q is Q-factor of the tuned loop.


The drawback of such SM loop  is that it is very narrow band and continuous tuning is needed even in narrow ham radio bands.  The placement of this type of loop outdoors is not very convenient since its needs some kind of remote tuning. 



Computer modeling of  active WSM Loop

The absolute measurements to obtain the active WSM loop parameters need sophisticated equipment which was not available.  Here I will present the results of computer modeling of this active antenna as well as some experimental results. 3 programs are used for this purpose. All three sources are freeware.

-  Excel spreadsheet [24]  where  the well known analytic formulas to compute the SM loop parameters are realized. Especially the current that flows into SML induced by incident electromagnetic wave  with known intensity can be computed with good accuracy.

- Antenna modeling program MMANA (v.1.7) which is implemented with MININEC core. The analysis of simple antennas in free space is accurate.

- Spice program LTSpiceIV  from Linear Technology Inc.  The spice programs are quite accurate in their small signal and noise analysis.


 Equivalent circuit of the loop and loop bandwidth

The equivalent circuit of the antenna in the spice model is shown on Fig. 9. This is Norton equivalent circuit  which is more convenient for analysis  in the frequency range where:


                       XL1>>R2.                                        (3)




 Fig.9  Norton equivalent spice model. The current source is in uA and is frequency independent.


 R2 is the loop loss resistance, L1 is the loop inductance, C1 is the loop capacitance and R1 is the load resistance which is actually the input resistance of the wideband common base amplifier. The value of the current source if  (3)  is fulfilled is equal to:


                        I1 = E / XL1                                   (4)

where E is the e.m.f induced by the incident field, XL1  is the impedance of L1.   E and XL1 are functions of the physical shape and size and  can be computed from the RX_Mag_Loop.xls  for simple single turn  loops. This model is adequate for frequencies above the lower bandwidth limit of the loop fC .


f =  R2/ (2*pi*L1)              (5)

Above  let say 3* fC  the value of the current source does not depend from the frequency .  I1 and can be computed by the same RX_Mag_Loop.xls spreadsheet.  The current I1 can  be calculated at arbitrary  frequency above 3* fC  and for field intensity of 1 [uV/m].  It should be expressed as LTSpice current source in [uA].  Then  all voltages in the model will be in [uV] and the gain will be obtained directly as equivalent effective height h.  Then the  antenna factor Ka  can be plot as  1/ h

The loss resistance is deliberately left serial to inductance. This is more realistic physical model since its value depends from physical factors (skin effect and radiation resistance)  and not from serial-to-parallel transformation formula. Above  frequencies 3* fCR2  can be neglected and a fixed value in the model can be used – let say 1 ohm.  Bellow fthe current source is no more frequency independent and more suitable model is the Thevenin (serial) equivalent circuit. In our case fC  is rather low. For the SM loops sizes and inductances of interest it is well bellow 100 KHz. 

There is another low cutoff frequency  fL which is more important for the wideband loop response:


f =  R1/ (2*pi*L1)              (6)

 fL determines where the  flat  frequency response of the output voltage begins. Above  fL   (where  XL1>>R1)  the loop has flat antenna factor. 



Results from the spice modeling

The results from modeling with LTSpice IV  are presented on  Fig 10 and Fig.11.  The amplifier is the same as shown on Fig.1. Two main parameters are shown. 



Fig. 10 Antenna Factor for 1 turn 1 m diam. circular loops.

Norm:  L1=3.6uH and I1=  0.00073 uA

 Fat:    L1=1.7uH and I1=  0.00153 uA

NoFilter:  Norm. without input LP filter.

BFR93:  Nofilter with BFR93 transistors as second pair.    


 The antenna factor  Ka is expressed in dB (20logKa). Two different loops – normal and “fat” are modeled.  The “fat” loop is with conductor diameter of 40 mm and the normal - with 3.4 mm aluminum. Fat loop has almost 6 dB higher gain. High frequency response (Fig.10) is limited by the Fof the second transistor pair and the parasitic stray inductance of the output wideband transformer. The input “anti FM” low-pass filter flattens the response at higher frequencies which is not bad. The differential input resistance of the amplifier is around 3 ohms at 1 MHz and rises with frequency. The  module of Rin becomes around 7 ohms at  30MHz and this assures flatness of the antenna factor in wide band.




Fig.11 Noise floor of  1 turn 1 m diam. circular loop at 1 KHz bandwidth

 Norm:  L1=3.6uH and I1=  0.00073 uA, with  LP filter

Fat:    L1=1.7uH and I1=  0.00153 uA, with LP filter

LT62Nor: 2 op.amp differential amplifier  LT6230-10, with input LP filter.


Noise analysis was performed for  CB amplifier with the same two  loops and also for differntial current-to-voltage convertor with LT6230-10 op. amplifiers (with normal loop). As it can be seen the noise floors for all cases of the WSM loop are  above the 0.2 uV/m line  and that means that the antenna sensitivity is limited by the  internal noise rather by the external atmospheric noise.  


Limitation of the models

 This model is reliable at about frequencies 15 MHz with the used single turn loop. Above this frequency the loop can not be presented by simple fixed inductance since the wave and resonance effects can not be neglected. The loop becomes longer than 0,1 wavelength  and its equivalent inductance, losses and radiation pattern becomes different. For example,  the loop  Q-factor drops dramatically above these frequencies.  For CP loops the model is adequate up to 30-40 MHz. For frequency bellow the fC  the loop model should be changed to serial (Thevenin)  with frequency dependant source but this is beyond of the scope of this paper.


 Wideband loop noise floor

 The current that flows in the wideband loop is very small.  In 1 m2 loop with inductance of 4 uH,  the induced short circuit current  from 1uV/m external field in the flat frequency response region will be 0.7 nA. The voltage drop across 3 ohms load resistor will be 2.1 nV. From the other  hand the thermal noise voltage at 290 deg. K of 3 ohm resistor at BW of 1 KHz  is 7 nV.  In this case we have 3.3 uV/m  equivalent  noise floor of the loop which is terminated with 3 ohms load resistor.  Actually speaking this is the main factor that limits the noise floor of a WSML.

 It is good to increase the load resistance since the thermal noise is proportional to square root of the resistance. If we increase 2 times the load resistance  we should increase the loop inductance 2 times to preserve the loop lower bandwidth limit. If the loop area is preserved that will reduce 2 times the loop current!  Obviously this limitation is fundamental. The antenna large bandwidth and low noise floor of small antenna  are antagonist factors. High Q-factor tuned loop has very low noise floor but very narrow bandwidth.


How to reduce the noise floor of wideband SML

     In the flat frequency response region  the current in the loop with fixed area is determined only by the loop inductance. The loop works in short circuited mode with very small load resistance. The loop loss resistance is not important since it is much smaller that the inductive resistance of the loop. The obvious solution is to maximize the loop short circuited current.


Loop size

MMANA modeling  gives the following results:     L of  1 m2 quad loop = 4.5 uH,      L of  2 m2  =  6.8 uH ,  the induced voltage is doubled but the current through the load resistor is increased only 1.33 times. From the other hand increasing the loop size  will lower the upper frequency response (0.1 wavelength rule).


Loop turns

Doubling the loop turns increases 2 times the induced voltage  and 4 times the inductance and the short circuit current is reduced 2 times.


Loop inductance

One of the methods to reduce the inductance when the physical size is fixed is to make a “fat loop”. The conductor diameter can be increased and the inductance can be lowered significantly. For example 1 m diam. loop with conductor diameter 3.4 mm has inductance of 4 uH. (MMANA simulation)  The same loop with conductor diameter 40 mm will have already 2.1 uH. The current through the pickup load resistor will be increased almost 2 times  and the noise floor will be reduced.


 Fig. 12 “Hermes” loop


Parallel loops

On Fig. 12   is given the commercial loop construction (named Hermes).  [18, 3].   Probably these are two parallel connected loops with 1 m diameter. The inductance is declared to be  equal to 1.4 uH.  It is not clear whether the axial connections on the picture are electrical or just mechanical.

 I have modeled two parallel square loops with MMANA. A single loop with 1m side conductor diameter 3.6 mm  has inductance of 4.5 uH. Two parallel loops at distance  8 cm  with conductor with the same diameter has  3 uH inductance. Axial electrical connections  at additional 3  points as in  the Fig.12 does not change the inductance and the radiation pattern. The mechanical construction of the parallel loops is much more convenient than using a fat conductor.


Parallel  crossed loops

In his very interesting page PA0SIM [1] used wideband loop antenna which he called Alford loop (K6STI has described loop with the same pattern  in QST article [8] ). I will call these loops ‘crossed parallel loops’ (CP loop),  (Appendix II).





Fig.13, 14 Crossed parallel loops (square shapes).

The drawing is not scaled to show better the connections between loops.

 The conductor was PVC insulated copper wire  1.8  mm diam. The distances between inner sides of quad wires are 3 cm.


On Fig,.13 and 14  are shown two type of crossed loops tested by me. These are big loops consisting of 2  or 4 parallel loops in one plane (area is 2 and 4 m2). These loops have very weak mutual coupling compared to the normal parallel loops.  Their terminals should be cross connected as shown in the Fig.13,14  so that currents induced by the incident field are added. The main properties of these crossed loops are  that they have much lower equivalent  inductance and increased short circuit current, preserving at the same time the small loop radiation pattern (compared to single turn loop with same area).

These two loops have  2.2  and 12.5 times lower inductance correspondingly  compared to a single square loop with the same area. (MMANA model, see Appendix II). The short circuit current is increased which leads to lower noise floor.  With these loops two decades of bandwidth with flat frequency response can be reached.

Preliminary  experiments with these CP loops were performed and they were compared to 1 m2 simple loop. The predicted reduction of the noise floor with 2-4 dB (2 squares)   and 6 – 10 dB (4 squares) was observed in the 14MHz band since there the atmospheric noise is bellow the WSM loop  noise floor. Further more precise experiments should be performed to prove the effectiveness of the crossed loops.


The Amplifier

The noise floor of WSML is actually due to the very low level of the antenna loop current which becomes in order of the thermal noise current of the load resistor.  Using better, lower noise preamplifiers will not change drastically the loop noise floor (Fig.11). Better lower noise transistors with higher FT were simulated: BFR93(NF=1.9) , BFR96(NF=3.3)  and newer ones BFR520 (NF=1.6)  and BFR540 (NF=1.5) all with FT higher than  5 GHz. The resulting noise floor is almost the same just the bandwidth of the amplifier is increases when higher FT transistors are used in the output pair.

Then I  simulated also a differential  amplifier with 2 operational amplifiers as a current to voltage converter [1, 2, 12]  Unfortunately I do not have ready spice  models of suitable op. amp. (e.g.  OPA687, AD8099 etc.) the only suitable amplifier which was  available in the LTSpice library was LT6230-10 which is limited to 600MHz  with noise  density of 1nV/Hz 1/2 . This amplifier is low current one and is not suitable for wideband high dynamic range antenna amplifier. But its noise parameters are very good and can be used to evaluate the noise behavior. The results in the noise floor are similar to PN2222A amplifier except for frequency region 4 to 16 MHz where the OP amp amplifier has  lower noise floor. At frequency bellow 3 MHz the noise floor is higher (up to 6 dB). The explanation is that the input resistance of the op. amp  amplifier is very low at low frequencies but increases with frequency. The increased input resistance improves the signal-to-thermal noise ratio. The common base transistor amplifier has much more stable input resistance and at higher frequencies it is  much lower. I speculate that the ideal amplifier for a wideband loop will be an amplifier with input resistance always equal to let say 1/10  of  XL  i.e. amplifier which increases its input resistance with 6 dB/oct.  


Noise floor in other active loops published in the Net

I analyzed data from several amateur publications and  commercial products to which I have access [ 1,2,4,5,15,16,17,18,19]. It must be pointed out that very often,  the important figure of noise floor expressed in uV/m  is not given and there is no direct information about this most important active WSM loop  parameter. Some  authors present the noise figure of the amplifier which is of no use if other data are not given.  The several available noise floor figures are  <1dBuV/m @ 200Hz BW in [17]  and   -42dBuA/m (named sensitivity?)  in [16] .    Some of the authors have expressed the noise floor as “ accdeptable” [1,2,4] but in [5] the author definitely declares that WSM loop noise floor is above the atmospheric noise .

The antenna factor usually is given and its value is between 0 and 30 dB(meters-1). This is equivalent to effective height h of 0 to -30 dBmeters. In most of publication the non-linear distortions figures again are expressed in dBm. The non-linear parameters should also be expressed in dBuV/m  to have some meaningful figures.



 The main problem in the active WSM loops is the increased noise floor compared to other antennas.  The origin of the problem lies in the very small loop current  and very small load resistance which is needed to obtain  wideband flat frequency response. Thermal noise of the load resistance (which is the input resistance of the amplifier) is the main limitation factor. This limitation is fundamental. The large bandwidth and low noise floor in this small antenna  are antagonist factors.

Using very low noise input transistors will change almost nothing. The modeling shows that increasing the signal pickup resistor reduces the noise floor  but we loose the frequency flat antenna factor. Increasing the pickup resistor above certain limits  reduces the loop current and degrades noise floor. High pickup resistance also increases the influence of the electric part of the field which is manifested as deviation from the ideal small loop diagram.  

The main rules are: 

1. Only single turn loop s must be used.

3. The loop loss resistance is not important so the material can be aluminum instead of copper.
2. A circular form of the loop – the ratio L / Area should be minmized.

2. A “fat” conductor loop with low inductance or parallel loops should be constructed to reduce the inductance.  

5. Parallel crossed loops are promising.  With this technique loops with much bigger area, low inductance and high upper frequency can be constructed. At the same time they exhibit the radiation pattern of a very small loop.  In this way the wideband loop noise floor can be reduced to acceptable level for the shortwave frequencies.




Appendix II                 Parallel Crossed Loops



The name and history

 I have found very few publications in the Net for this theme. PA0SIM [1]   use for his wideband active antenna a loop which he called Alford loop (K6STI has described a loop with the same shape but with much larger size in QST article [8]). I found in the Net the following definition of Alford loop in IEC publication Antennas / Specific terms for antennas consisting of radiating conductors:

 an essentially omni-directional antenna consisting of four insulated conductors, each approximately one-half wavelength long, positioned in the form of a square in a horizontal plane and symmetrically fed by balanced lines at two diagonally opposite corners of the square”    

So I do not think that the term “Alford loop”  is suitable for this  type of loop. I will call them crossed parallel loops (CP loop). (English is not my native language and I do not know whether the term is very appropriate).

 Jan, PA0SIM pointed to the fact that his crossed loop has almost perfect  radiation pattern of a small loop instead of its larger size. C. Baum [11],  used CP loops for different goals but the basic idea is the same.  Similar CP loop called “Figure 8 magnetic loop antenna”  [6]  is suggested by PA0FRI  for transmitting loop. 


 Simple theory

The genesis of a crossed loop from a simple two parallel loops is shown on Fig. 15


Fig.15  The genesis of the crossed loop. Opening the loops reduces the equivalent

inductance and increases 2 times the area. They must be twisted so that the currents induced by the

 incident field are added.


This principle of crossed parallel loops can be generalized – the single  loop can be divided into several smaller loops with the same  total area.  They should be cross connected as shown in the Fig. 16 so that currents induced by the incident field are added. The main properties of these crossed loops are  that they have much lower equivalent inductance and increased short circuit current,  for the same area of a single loop. The radiation pattern of these loops is the same as the pattern of a “small loop”(Fig.18 – 20)




Fig.16  Different CP loops.  All odd points and all even points must be connected together.

The load is between odd and even  points.


 If we have n smaller loops with the same total area as the single big loop with inductance L and induced e.m.f  E,  then the equivalent circuit is shown on  Fig17.  

Fig.17   CP loop simplified equivalent circuit


For each small loop the inductance is L/n  (n times smaller than the inductance of a big loop). The induced e.m.f is E/n (n times smaller area). Obviously the short circuit current in small loop is equal to that of the big loop I (see Eq.4). Then the total equivalent current  is :

Ieq = n* I                                            (7)     

     and equivalent inductance is :

Leq = L / n2                                                   (8)

and we should expect n times decrease of the noise floor. Of course these formulas are very approximate. There is always some mutual coupling between loops  and the inductance of a loop with half area is not exactly L/2,  but  these simple  equations present the nature of the problem.


Numerical Simulation

More detailed analysis of the receiving currents in the crossed loop was performed with MMANA program. This program is convenient to analyze the transmitting antennas but here I will present a method to analyze these loops in receive mode. Most of the loops are with quad shape since it was easier for me to draw them with the wire editor.  The idea is to calculate the load resistor currents in different loops excited by a small dipole radiator placed in a fixed distance in the far field zone. 

 With the wire editor I placed in the far field at 80 m distance a simple vertical dipole radiator with length 1 m with the source at the dipole center. The dipole is in the direction of maximal loop sensitivity (they are in the same plane). The source in the loop was replaced with load resistor of 3 ohms (the input resistance of CB amplifier). To increase the accuracy the number of segments was set to be high (automatic tapering, DM1 = 3000, DM2= 800, SC=2,EC=1).  After the computation the currents in the loop induced by dipole radiation are very small and they are not displayed on the graphical screen. But these currents can be taken from “Table currents” menu in MMANA. The program creates  *csv file which contains the values of currents in all segments and can be exported in Excel for easier processing.  The currents are given in relative units. ( in *csv file “Magnitude” colon).

 The procedure is as follows:  first we run the program with vertical dipole as radiator with referent 1 m2 single quad loop. The resulting *csv file must be saved. Then we run the new loop  of interest  with vertical dipole as radiator keeping the program settings the same as in the previous case ( the distance, the number of segments, frequency  etc.). The new *.csv file with currents of the new antenna is saved and we can compare the currents that flow in the referent loop and in the new loop. These currents are induced by the same vertical radiator with the same current and at the same distance. We should compare only the currents in the wires where the load is connected.

  I think that this numerical experiment is quite accurate:   the dipole radiator  is with small size and the distance is sufficient  so the receiving loop is almost certainly placed in the far field zone (see [14]  for  determination of the near field zone for 1.7 m diam. loop) . The polarization of both antennas is vertical and the calculation is performed in the free space. The currents table gives currents in every segment of each wire.

MMANA modeling of different loops gives the following figures presented in Table 1



 Table 1  Results from MMANA simulations. The referent antenna is single quad loop with 1 m2 area.

 I is the current in 3 ohms load resistor Rload. I*L is ( I/Iref * L/Lref) and is a quantity which esimates the relative

 eqivalent area compared to the referent  loop.


The following conclusions can be drawn looking at the Table 1:

1. Notice that the current increase is not proportional to reduction of L for the crossed loops (the colon  “I*L”). As it can be seen the current increase is not as big as predicted by the simplified Eq.7. That means that the equivalent area of crossed loops is smaller than their geometric area. For other shapes and number  of crossed loops the reduction might be different.  Further experiments and theory are needed in this direction.

2. Notice that there is 4 dB gain reduction of 4 crossed loops compared to single loop which might be interpreted as slight increase of Rloss/Rradiation ratio of the crossed loop.  Advantages in using cross loops for transmitting is questionable.

 3. Increasing the distance between 2 parallel loops decreases the inductance but at the same time the radiation pattern changes and is not equivalent to a single small loop pattern. The optimal distance for the 1 m2 parallel loops is somewhere between 4 – 12 cm.

5.  All these parallel loops have  radiation pattern equivalent to a single very small loop.  (see also PA0SIM article). They preserve this radiation pattern to much higher frequencies than the simple single turn loop.  The numerical experiments show that approximately  0.1 wavelength rule must be applied to the partial loop length,  not to the sum of the lengths of the conductors of all loops. More over, above this 0.1 wavelength limit these loops still have small loop radiation pattern (see Fig.20). Their parallel  resonance frequency  is moved substantially upward.  This directly means that we can build loops with much larger area with radiation diagram properties of a very small loop.


As an example I will give  4-quads  crossed loop with 4 m2 total area. (2 x 2 m size, Fig. 13) This large loop has “small loop pattern”  up to 50 MHz .  The lower frequency response (Eq.6) is  0.46 MHz.  It has almost 13 dB larger current at 3.5MHz compared to “conventional” 1 m2 single quad loop.  




Fig. 18, 19,20  The radiation patterns of 4 m2  quad shape CP loop for elevation of 0 degrees.

The asymmetry in horizontal component (red) is due to small imperfections in wire drawings

especially around the feed points


At the same time a single quad loop with the same area of 4 m2   (quad side = 2 m)  at 3.5 MHz  has a pattern which is marginal  -  the loop perimeter is  already 0.1 wavelength.  The short circuit current is almost 3 times lower than  the current in 4-quads CP loop and at 14MHz the radiation pattern is quite different to  that of “small loop pattern”.




Fig. 21,22  The radiation patterns of 4 m2  quad shape single  loop for elevation of 0 degrees.



The most important properties of CP loops are the ability to built loops with large area and low inductance which still preserve the small loop radiation pattern. Their short circuit current is higher compared to a single turn loop with the same area. Their equivalent area is smaller than their geometric area. I could not find any analytic equations to obtain  the ralationship between filed inensity and induced voltage for the given geometry of these loops. There is a place for further experimental and theoretical investigations .

 The wideband properties of such loops  are almost 2 decades in frequency.  These loops are very suitable for design of active wideband SM loops.  




Appendix III      Band noise levels


Table 2



*     Day-time values or  when the band is closed

**    Night-time values or  when the band is opened


For reference, the  half-wave dipole at 14 MHz  will produce 50 uV voltage (S9)  at 75 ohms load  when field intensity is 16 uV/m.





1. Jan, PA0SIM ,  Broad Band Amplification,  http://www.pa0sim.nl/Broadband%20amplification.htm

2. Hagg Maarten, WL1030 Wideband loop antenna,  http://wl1030.com/content/

3. Lambert,  J A G3FNZ. A directional active loop receiving antenna System, , Radcom 1982 HF Antenna Collection p.106

4. Lass, Michael, DJ3VY; Jirmann, Dr. Jochen, DB1NV,  Elektrische/magnetische Empfangsantenne fur VLF bis HF(zwei Teile) 2-3 CQ-DL /1997

5. Lankford Dallas,  Amplified 1 And 4 Meter Square Untuned Loop Antennas, 5/14/2007, rev. 8/7/2007, http://www.kongsfjord.no/dl/dl.htm

6. Magnetic Loop  "MEIGHT" a Figure 8 Double Loop Antenna,  http://www.pa0fri.geerligs.com/

7. Trask Chris,   Bipolar Transistor Evaluation,  http://home.earthlink.net/~christrask/Bipolar%20Transistor%20Evaluation.pdf

8. The K6STI Receiving Loop, http://www.angelfire.com/md/k3ky/page45.html  (Original Article in QST for September, 1995 p. 33)  


9. Theobald Karl,  On the Properties of Loop Antennas,  http://www.ece.unm.edu/summa/notes/SSN/note4.pdf

10. Baum Carl E., Parameters of Some Electrically- Small Electromagnetic sensors, 1967,  http://www.ece.unm.edu/summa/notes/SSN/note38.pdf

11. Baum Carl E.,  Compact, Low Impedance Magnetic Antennas, 2002, Note 470 , Air Force Research Lab. http://www.ece.unm.edu/summa/notes/SSN/Note470.pdf

12. Bruno Marco, IK1ODO, Thinking about Ideal Loops, http://www.dxzone.com/cgi-bin/dir/jump2.cgi?ID=10845

13. Miron Douglas B., Small Antenna Design,  2006, Elsevier Inc. ISBN-13: 978-0-7506-7861-2

14. Belrose J. S., "Electrically Small Transmitting Loops," IEEE International Symposium on Antennas and Propagation, Washington, July 3-8, 2005.

Commercial sites

15. http://wellbrook.uk.com/ALA1530plus.html

16. http://www.ets-lindgren.com/page/?i=ELAntennas 

17. http://www.sat-schneider.de

18. http://www.usantennaproducts.com/products.html

19. www.comsistel.com


20. http://www.oe1ira.at/sl/loop.html

21. http://www.dxzone.com/catalog/Antennas/Magnetic_Loop/

22. http://home.earthlink.net/~christrask/techbibs.html,  Magnetic Loop Antenna References,  Chris Trask  

My  articles   

23. Levkov C.L. , Very Weak Signal Reception with Small Magnetic Loop Antenna,  http://www.lz1aq.signacor.com/docs/fa-eng/Weak_signals-mag_loop_engl.htm

24. Levkov C.L. , Receiving Magnetic Loop calculations spreadsheet. RX_Mag_loop.xls  




Sofia, Bulgaria, May 2010       Chavdar,  LZ1AQ


Revision 1.1 13 June 2011:       Minor  changes in the text for better clarification. On Fig.13,14  measurements lines are removed to avoid confusions that they are wires.

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